First Parallel Results for a Finite-Element MHD Code on the T3D and

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微积分常用英文词汇(分章)

微积分常用英文词汇(分章)

英汉微积分词汇English-Chinese Calculus Vocabulary第一章函数与极限Chapter 1 Function and Limit高等数学higher mathematics集合set元素element子集subset空集empty set并集union交集intersection差集difference of set基本集basic set补集complement set直积direct product笛卡儿积Cartesian product象限quadrant原点origin坐标coordinate轴axisx 轴x-axis整数integer有理数rational number实数real number开区间open interval闭区间closed interval半开区间half open interval有限区间finite interval区间的长度length of an interval无限区间infinite interval领域neighborhood领域的中心center of a neighborhood领域的半径radius of a neighborhood左领域left neighborhood右领域right neighborhood映射mappingX到Y的映射mapping of X onto Y满射surjection单射injection一一映射one-to-one mapping双射bijection算子operator变化transformation函数function逆映射inverse mapping复合映射composite mapping自变量independent variable因变量dependent variable定义域domain函数值value of function函数关系function relation值域range自然定义域natural domain单值函数single valued function多值函数multiple valued function单值分支one-valued branch函数图形graph of a function绝对值absolute value绝对值函数absolute value function符号函数sigh function整数部分integral part阶梯曲线step curve当且仅当if and only if (iff)分段函数piecewise function上界upper bound下界lower bound有界boundedness最小上界least upper bound无界unbounded函数的单调性monotonicity of a function 单调增加的increasing单调减少的decreasing严格递减strictly decreasing严格递增strictly increasing单调函数monotone function函数的奇偶性parity (odevity) of a function 对称symmetry偶函数even function奇函数odd function函数的周期性periodicity of a function周期period周期函数periodic function反函数inverse function直接函数direct function函数的复合composition of function复合函数composite function中间变量intermediate variable函数的运算operation of function基本初等函数basic elementary function初等函数elementary function线性函数linear function常数函数constant function多项式polynomial分段定义函数piecewise defined function阶梯函数step function幂函数power function指数函数exponential function指数exponent自然指数函数natural exponential function对数logarithm对数函数logarithmic function自然对数函数natural logarithm function三角函数trigonometric function正弦函数sine function余弦函数cosine function正切函数tangent function半角公式half-angle formulas反三角函数inverse trigonometric function常数函数constant function双曲线hyperbola双曲函数hyperbolic function双曲正弦hyperbolic sine双曲余弦hyperbolic cosine双曲正切hyperbolic tangent反双曲正弦inverse hyperbolic sine反双曲余弦inverse hyperbolic cosine反双曲正切inverse hyperbolic tangent最优化问题optimization problems不等式inequality极限limit数列sequence of number复利compound interest收敛convergence收敛的convergent收敛于a converge to a发散divergence发散的divergent极限的唯一性uniqueness of limits收敛数列的有界性boundedness of a convergent sequence子列 subsequence函数的极限 limits of functions函数当x 趋于0x 时的极限 limit of functions as x approaches 0x单侧极限 one-sided limit左极限 left limit右极限 right limit单侧极限 one-sided limits渐近线 asymptote水平渐近线 horizontal asymptote分式 fractions商定律 quotient rule无穷小 infinitesimal无穷大 infinity铅直渐近线 vertical asymptote夹逼准则 squeeze rule (Sandwich theorem)单调数列 monotonic sequence高阶无穷小 infinitesimal of higher order低阶无穷小 infinitesimal of lower order同阶无穷小 infinitesimal of the same order等阶无穷小 equivalent infinitesimal多项式的次数 degree of a polynomial三次函数 cubic function函数的连续性 continuity of a function增量 increment函数在0x 连续 the function is continuous at 0x左连续 left continuous / continuous from the left右连续 right continuous / continuous from the right连续性 continuity不连续性 discontinuity连续函数 continuous function函数在区间上连续 function is continuous on an interval不连续点 discontinuity point第一类间断点 discontinuity point of the first kind第二类间断点 discontinuity point of the second kind初等函数的连续性 continuity of the elementary functions定义区间 defined interval最大值 global maximum value (absolute maximum)最小值 global minimum value (absolute minimum)零点定理 the zero point theorem介值定理 intermediate value theorem第二章 导数与微分Chapter 2 Derivative and Differential 速度velocity速率speed平均速度average velocity瞬时速度instantaneous velocity匀速运动uniform motion平均速度average velocity瞬时速度instantaneous velocity圆的切线tangent line of a circle割线secant line切线tangent line位置函数position function导数derivative求导法differentiation可导的derivable可导函数differentiable function光滑曲线smooth curve变化率rate of change函数的变化率问题problem of the change rate of a function导函数derived function导数定义域domain of derivative左导数left-hand derivative右导数right-hand derivative单侧导数one-sided derivatives在闭区间[a, b]上可导is derivable on the closed interval [a, b] 指数函数的导数derivative of exponential function幂函数的导数derivative of power function切线的斜率slope of the tangent line截距interceptsx 截距x-intercept直线的斜截式slope-intercept equation of a line点斜式point-slope form切线方程tangent equation焦点focus角速度angular velocity成本函数cost function边际成本marginal cost逐项求导法differentiation term by term积之导数derivative of a product商之导数derivative of a quotient链式法则chain rule隐函数implicit function显函数explicit function隐函数求导法implicit differentiation加速度acceleration二阶导数second derivative三阶导数third derivative高阶导数nth derivative / higher derivative莱布尼茨公式Leibniz formula对数求导法log- derivative参数parameter参数方程parametric equation相关变化率correlative change rata微分differential微分学differential可微的differentiable函数的微分differential of function自变量的微分differential of independent variable微商differential quotient逼近法approximation用微分逼近approximation by differentials间接测量误差indirect measurement error绝对误差absolute error相对误差relative error第三章微分中值定理与导数的应用Chapter 3 MeanValue Theorems of Differentials and the Application ofDerivatives均值定理mean value theorem罗尔定理Roll’s theorem费马引理Fermat’s lemma拉格朗日中值定理Lagrange’s mean value theorem驻点stationary point稳定点stable point临界点critical point辅助函数auxiliary function拉格朗日中值公式Lagrange’s mean value formula柯西中值定理Cauchy’s mean value theorem洛必达法则L’Hospital’s Rule不定式indeterminate form“0”型不定式indeterminate form of type “”泰勒中值定理Taylor’s mean value theorem 泰勒公式Taylor formula系数coefficient余项remainder term线性近似linear approximation拉格朗日余项Lagrange remainder term麦克劳林公式Maclaurin’s formula佩亚诺余项Peano remainder term阶乘factorial凹凸性concavity上凹(或下凸)concave upward (concave up)下凹(或向上凸的)concave downward (concave down) 拐点inflection point极值extreme value函数的极值extremum of function极大与极小值maximum and minimum values极大值local (relative) maximum最大值global (absolute) maximum极小值local (relative) minimum最小值global (absolute) minimum目标函数objective function收入函数revenue function斜渐进线slant asymptote曲率curvature弧微分arc differential平均曲率average curvature曲率园circle of curvature曲率中心center of curvature曲率半径radius of curvature渐屈线evolute渐伸线involute根的隔离isolation of root隔离区间isolation interval切线法tangent line method第四章不定积分Chapter 4 Indefinite Integrals 原函数primitive function / antiderivative积分integration积分学integral积分号sign of integration被积函数integrand积分变量integral variable积分常数constant of integration积分曲线integral curve积分表table of integrals换元积分法integration by substitution有理代换法rationalizing substitution三角代换法trigonometric substitutions分部积分法integration by parts分部积分公式formula of integration by parts有理函数rational function真分式proper fraction假分式improper fraction部分分式partial fractions三角积分trigonometric integrals第五章定积分Chapter 5 Definite Integrals曲线下方之面积area under a curve曲边梯形trapezoid with曲边curve edge窄矩形narrow rectangle曲边梯形的面积area of trapezoid with curved edge积分下限lower limit of integral积分上限upper limit of integral积分区间integral interval分割partition黎曼和Riemannian sum积分和integral sum可积的integrableSimpson 法则逼近法approximation by Simpson’s rule梯形法则逼近法approximation by trapezoidal rule矩形法rectangle method曲线之间的面积area between curves积分中值定理mean value theorem of integrals函数在区间上的平均值average value of a function on an interval 牛顿-莱布尼茨公式Newton-Leibniz formula微积分基本公式fundamental formula of calculus微积分基本定理fundamental theorem of calculus变量代换change of variable换元公式formula for integration by substitution递推公式recurrence formula反常积分improper integral反常积分发散the improper integral is divergent反常积分收敛the improper integral is convergent无穷限的反常积分improper integral on an infinite interval无界函数的反常积分improper integral of unbounded functions瑕点flaw绝对收敛absolutely convergent第六章定积分的应用Chapter 6 Applications of the Definite Integrals 元素法the element method面积元素element of area平面plane平面图形的面积area of a plane figure直角坐标(又称“笛卡儿坐标”)Cartesian coordinates / rectangular coordinates x 坐标x-coordinate坐标轴coordinate axes极坐标polar coordinates极轴polar axis极点pole圆circle扇形sector抛物线parabola椭圆ellipse椭圆的轴axes of ellipse蚌线conchoid外摆线epicycloid双纽线lemniscate蚶线limacon旋转体solid of revolution, solid of rotation旋转体的面积volume of a solid of rotation旋转椭球体ellipsoid of revolution, ellipsoid of rotation曲线的弧长arc length of a curve可求长的rectifiable光滑smooth功work水压力water pressure引力gravitation变力variable force第七章空间解析几何与向量代数Chapter 7 Space Analytic Geometry and Vector Algebra纯量(标量)scalar向量vector自由向量free vector单位向量unit vector零向量zero vector相等equal平行parallel平行线parallel lines向量的线性运算linear operation of vector加法addition减法subtraction数乘运算scalar multiplication三角形法则triangle rule平行四边形法则parallelogram rule交换律commutative law结合律associative law分配律distributive law负向量negative vector三角不等式triangle inequality对角线diagonal差difference余弦定理(定律)law of cosines空间space空间直角坐标系space rectangular coordinates坐标平面coordinate plane卦限octant向量的模modulus of vector定比分点definite proportion and separated point中点公式midpoint formula等腰三角形isosceles triangle向量a与b的夹角angle between vector a and b方向余弦direction cosine方向角direction angle投影projection向量在轴上的投影projection of a vector onto an axis向量的分量components of a vector对称点symmetric point数量积(点积,内积)scalar product (dot product, inner product)叉积(向量积,外积)cross product (vector product, exterior product) 混合积mixed product锐角acute angle流体fluid刚体rigid body角速度angular velocity平行六面体parallelepiped平面的点法式方程point-norm form equation of a plane法向量normal vector平面的一般方程general form equation of a plane三元一次方程three-variable linear equation平面的截距式方程intercept form equation of a plane两平面的夹角angle between two planes点到平面的距离distance from a point to a plane空间直线的一般方程general equation of a line in space方向向量direction vector直线的点向式方程point-direction form equations of a line直线的对称式方程symmetric form equation of a line方向数direction number直线的参数方程parametric equations of a line两直线的夹角angle between two lines垂直perpendicular垂直线perpendicular lines直线与平面的夹角angle between a line and a planes 平面束pencil of planes平面束的方程equation of a pencil of planes行列式determinant系数行列式coefficient determinant曲面方程equation for a surface球面sphere球体spheroid球心ball center轨迹方程locus equation旋转轴rotation axis旋转曲面surface of revolution母线generating line圆锥面cone顶点vertex半顶角semi-vertical angle旋转双曲面revolution hyperboloids旋转单叶双曲面revolution hyperboloids of one sheet 旋转双叶双曲面revolution hyperboloids of two sheets 柱面cylindrical surface, cylinder圆柱circular cylinder圆柱面cylindrical surface准线directrix抛物柱面parabolic cylinder二次曲面quadric surface截痕法method of cut-off mark椭圆锥面elliptic cone椭球面ellipsoid双曲面hyperboloid单叶双曲面hyperboloid of one sheet双叶双曲面hyperboloid of two sheets旋转椭球面ellipsoid of revolution抛物面paraboloid椭圆体ellipsoid椭圆抛物面elliptic paraboloid旋转抛物面paraboloid of revolution双曲抛物面hyperbolic paraboloid马鞍面saddle surface椭圆柱面elliptic cylinder双曲柱面hyperbolic cylinder抛物柱面parabolic cylinder空间曲线space curve交线intersection curve空间曲线的一般方程general form equations of a space curve空间曲线的参数方程parametric equations of a space curve螺线spiral / helix螺矩pitch投影柱面projecting cylinder第八章多元函数微分法及其应用Chapter 8 Differentiation of Functions of Several Variables and Its Application 一元函数function of one variable二元函数binary function邻域neighborhood去心邻域noncentral neighborhood方邻域square neighborhood圆邻域circular neighborhood内点interior point外点exterior point边界点frontier point, boundary point聚点point of accumulation导集derived set开集open set闭集closed set连通集connected set开区域open region闭区域closed region有界集bounded set无界集unbounded setn维空间n-dimensional space多元函数function of several variables二重极限double limit多元函数的连续性continuity of function of several variables连续函数continuous function不连续点discontinuity point一致连续uniformly continuous偏导数partial derivative对自变量x的偏导数partial derivative with respect to independent variable x高阶偏导数partial derivative of higher order二阶偏导数second order partial derivative混合偏导数hybrid partial derivative全微分total differential偏增量partial increment偏微分partial differential全增量total increment可微分differentiable必要条件necessary condition充分条件sufficient condition叠加原理superposition principle全导数total derivative中间变量intermediate variable隐函数存在定理theorem of the existence of implicit function 光滑曲面smooth surface曲线的切向量tangent vector of a curve法平面normal plane向量方程vector equation向量值函数vector-valued function切平面tangent plane法线normal line方向导数directional derivative等高线level curve梯度gradient数量场scalar field梯度场gradient field向量场vector field势场potential field引力场gravitational field引力势gravitational potential曲面在一点的切平面tangent plane to a surface at a point曲线在一点的法线normal line to a surface at a point无条件极值unconditional extreme values鞍点saddle point条件极值conditional extreme values拉格朗日乘数法Lagrange multiplier method拉格朗日乘子Lagrange multiplier经验公式empirical formula最小二乘法method of least squares均方误差mean square error第九章重积分Chapter 9 Multiple Integrals重积分multiple integrals二重积分double integral可加性additivity累次(逐次)积分iterated integral体积元素volume element二重积分变量代换法change of variable in double integral极坐标表示的面积area in polar coordinates扇形的面积area of a sector of a circle极坐标二重积分double integral in polar coordinates三重积分triple integral直角坐标系中的体积元素volume element in rectangular coordinate system 柱面坐标cylindrical coordinates柱面坐标系中的体积元素volume element in cylindrical coordinate system 球面坐标spherical coordinates球面坐标系中的体积元素volume element in spherical coordinate system 剥壳法shell method圆盘法disk method反常二重积分improper double integral曲面的面积area of a surface质心center of mass静矩static moment密度density形心centroid转动惯量moment of inertia参变量parametric variable第十章曲线积分与曲面积分Chapter 10 Line (Curve) Integrals and Surface Integrals对弧长的曲线积分line integrals with respect to arc length第一类曲线积分line integrals of the first type对坐标的曲线积分line integrals with respect to x, y, and z第二类曲线积分line integrals of the second type有向曲线弧directed arc单连通区域simple connected region复连通区域complex connected region路径无关path independence格林公式Green formula顺时针方向clockwise逆时针方向counterclockwise区域边界的正向positive direction of region boundary第一类曲面积分surface integrals of the first type旋转曲面的面积area of a surface of a revolution对面积的曲面积分surface integrals with respect to area有向曲面directed surface对坐标的曲面积分surface integrals with respect to coordinate elements第二类曲面积分surface integrals of the second type有向曲面之元素element of directed surface高斯公式gauss formula拉普拉斯算子Laplace operator拉普拉斯变换Laplace transform格林第一公式Green’s first formula通量flux散度divergence斯托克斯公式Stokes formula环流量circulation旋度rotation (curl)第十一章无穷级数Chapter 11 Infinite Series一般项general term部分和partial sum收敛级数convergent series余项remainder term等比级数geometric series几何级数geometric series公比common ratio调和级数harmonic series柯西收敛准则Cauchy convergence criteria, Cauchy criteria for convergence 正项级数series of positive terms达朗贝尔判别法D’Alembert test柯西判别法Cauchy test交错级数alternating series绝对收敛absolutely convergent条件收敛conditionally convergent柯西乘积Cauchy product函数项级数series of functions发散点point of divergence收敛点point of convergence收敛域convergence domain和函数sum function幂级数power series幂级数的系数coefficients of power series阿贝尔定理Abel Theorem收敛半径radius of convergence收敛区间interval of convergence幂级数的导数derivative of power series泰勒级数Taylor series麦克劳林级数Maclaurin series二项展开式binomial expansion近似计算approximate calculation舍入误差round-off error (rounding error)欧拉公式Euler’s formula魏尔斯特拉斯判别法Weierstrass test三角级数trigonometric series振幅amplitude角频率angular frequency初相initial phase矩形波square wave谐波分析harmonic analysis直流分量direct component基波fundamental wave二次谐波second harmonic三角函数系trigonometric function system傅立叶系数Fourier coefficient傅立叶级数Fourier series周期延拓periodic prolongation正弦级数sine series余弦级数cosine series奇延拓odd prolongation偶延拓even prolongation傅立叶级数的复数形式complex form of Fourier series第十二章微分方程Chapter 12 Differential Equation解微分方程solve a differential equation常微分方程ordinary differential equation (ODE)偏微分方程partial differential equation (PDE)微分方程的阶order of a differential equation微分方程的解solution of a differential equation微分方程的通解general solution of a differential equation初始条件initial condition微分方程的特解particular solution of a differential equation初值问题initial value problem微分方程的积分曲线integral curve of a differential equation 可分离变量的微分方程variable separable differential equation 隐式解implicit solution隐式通解implicit general solution衰变系数decay coefficient衰变decay齐次方程homogeneous equation一阶线性方程linear differential equation of first order非齐次non-homogeneous齐次线性方程homogeneous linear equation非齐次线性方程non-homogeneous linear equation常数变易法method of variation of constant暂态电流transient state current稳态电流steady state current伯努利方程Bernoulli equation全微分方程total differential equation积分因子integrating factor高阶微分方程differential equation of higher order悬链线catenary高阶线性微分方程linear differential equation of higher order自由振动的微分方程differential equation of free vibration强迫振动的微分方程differential equation of forced oscillation串联电路的振荡方程oscillation equation of series circuit二阶线性微分方程second order linear differential equation线性相关linearly dependence线性无关linearly independence二阶常系数齐次线性微分方程second order homogeneous linear differential equation with constant coefficient二阶变系数齐次线性微分方程second order homogeneous linear differential equation with variable coefficient特征方程characteristic equation无阻尼自由振动的微分方程differential equation of free vibration with zero damping固有频率natural frequency简谐振动simple harmonic oscillation, simple harmonic vibration微分算子differential operator待定系数法method of undetermined coefficient共振现象resonance phenomenon欧拉方程Euler equation幂级数解法power series solution数值解法numerical solution勒让德方程Legendre equation微分方程组system of differential equations常系数线性微分方程组system of linear differential equations with constant coefficient。

First Results from the KASCADE Air-Shower Experiment

First Results from the KASCADE Air-Shower Experiment

a r X i v :a s t r o -p h /9703182v 1 27 M a r 1997FIRST RESULTS FROMTHE KASCADE AIR-SHOWER EXPERIMENT ∗K.-H.Kampert a,b ,W.D.Apel a ,K.Bekk a ,E.Bollmann a ,H.Bozdog c ,I.M.Brancus c ,M.Brendle d ,A.Chilingarian e ,K.Daumiller b ,P.Doll a ,J.Engler a ,M.F¨o ller a ,H.J.Gils a ,R.Glasstetter a ,A.Haungs a ,D.Heck a ,J.H¨o randel a ,H.Keim a ,J.Kempa c ,H.O.Klages a ,J.Knapp b ,H.J.Mathes a ,H.J.Mayer a ,H.H.Mielke a ,D.M¨u hlenberg a ,J.Oehlschl¨a ger a ,M.Petcu c ,U.Raidt d ,H.Rebel a ,M.Roth a ,G.Schatz a ,H.Schieler a ,G.Schmalz a ,T.Thouw a ,J.Unger a ,B.Vulpescu c ,G.J.Wagner d ,J.Weber a ,J.Wentz a ,T.Wibig f ,T.Wiegert a ,D.Wochele a ,J.Wochele a ,J.Zabierowski f ,S.Zagromski a ,and B.Zeitnitz a,b—KASCADE Collaboration —aInstitut f¨u r Kernphysik,Forschungszentrum Karlsruhe,D-76021Karlsruhe,Germany,bInstitut f¨u r Experimentelle Kernphysik,Universit¨a t Karlsruhe,D-76021Karlsruhe,Germany,cInstitute of Physics and Nuclear Engineering,RO-7690Bucharest,Romania,dPhysikalisches Institut,Universit¨a t T¨u bingen,D-72076T¨u bingen,Germany,eCosmic Ray Division,Yerevan Physics Institute,Yerevan 36,Armenia,fInst.for Nuclear Studies and Dept.of Exp.Physics,University of Lodz,PL-90950Lodz,PolandA new extensive air shower (EAS)experiment has been installed at the laboratory site of the Forschungszentrum Karlsruhe.The major goal of the experiment is to determine the chem-ical composition in the energy range around and above the knee of the primary cosmic ray spectrum.An important advantage of the installation is the capability to simultaneously mea-sure the electromagnetic,muonic and hadronic components of EAS event-by-event,thereby reducing systematic uncertainties to a large extend.Data taking with a large part of the experiment has started at the end of 1995with further installations continuing during 1996.First preliminary results are presented.1INTRODUCTIONDespite the fact that ultra-high energy cosmic rays (UHE-CR)are known for decades,their sources and the acceleration mechanism are still under debate.Mainly for reasons of the required power the dominant acceleration sites are generally believed to be supernova remnants in the Sedov phase.Naturally,this leads to a power law spectrum as is observed experimentally.Detailed examination suggests that this process is limited to E/Z <∼1015eV.Curiously,theCR spectrum steepens at approx.5×1015eV,indicating that the ‘knee’may be related to the upper limit of acceleration.A change in the CR propagation with decreasing galacticFigure 1:Schematic layout of the KASCADE experi-ment.KASCADE Central DetectorFigure 2:Schematic layout of the central detector sys-tem of KASCADE.containment has also been considered.A key observable for understanding the origin of the knee and distinguishing the SN acceleration model from other proposed mechanisms 1,is given by the mass composition of CR particles and by possible variations across the knee.Unfortunately,beyond the knee little is known about the CR’s other than their energy spectrum.Direct measurements using detector systems on satellites,space craft or high altitude balloons cannot provide the required data with sufficient statistics because of limited detector area and exposure time 2,3.Experiments at ground level do not suffer from these problems since they can cover large areas,measure for extended time periods,and also take advantage of the magnifying effect of the atmosphere.The latter is because sufficiently high energy CR particles initiate extensive air showers which spread out over large areas at observation level.Sampling detector systems with typical coverages of less than one percent can be used for registration of such showers.However,this indirect method of detection bears a number of serious difficulties in the interpretation of the data and requires detailed modeling of the shower development and detector responses.It is well known,that a number of characteristics of EAS depends on the energy per nucleon of the primary nucleus,notably the ratio of electron to muon numbers,the energy of the hadrons in the shower,the shapes of the lateral distributions of the various components of the shower,etc.The basic concept of the KASCADE experiment 4is to measure a large number of these parameters for each individual event in order to determine both the energy and mass of the primary particles.2LAYOUT AND STATUS OF THE EXPERIMENTKASCADE (Kahower Crray Degrid of13m spacing forming a detector array of200×200m2.Each station contains2or4 scintillation detectors for the electron/photon component with a total area of(1.6m2)3.2m2. Energy deposits equivalent to2000m.i.p.can be detected with a threshold of0.25m.i.p.The 3.2m2muon detector of a station is located below a shield of20X0thickness.It consists of4 pieces of plastic scintillator,90×90×3cm3each,read out by green wavelength shifter bars on all edges with a total of4phototubes.The supply and electronic readout of the detectors in the stations is organized in16clusters of16stations each(see Fig.1).These clusters act as small independent air shower arrays.The main part of the central detector system(Fig.2)is thefinely segmented hadron calorime-ter.It consists of a20×16m2iron stack arranged into9horizontal slabs with a total absorber thickness corresponding to more than11nuclear interaction lengths.A total of10,000ionization chambersfilled with the room temperature liquid tetramethylsilane(TMS)is used for the mea-surement of energy in the gaps5.The chambers are made of50×50×1cm3stainless steel boxes and are read out by4independent central electrodes of25×25cm2size.Thus,the readout of the calorimeter amounts to40,000electronic channels spread out over2,500m2.Thefine segmentation allows for a separation of hadrons with distances as low as50cm.The detectors have a dynamic range of104limited only by the amplifier chain and its performance ensures a very stable operation over many years.The top layer of ionization chambers is shielded against the electromagnetic component of EAS by12cm of iron and additional5cm of lead.The energy sum of the hadrons in the core of a1PeV shower can be determined with a resolution of8%.Individual hadrons with energies larger than20GeV are reconstructed.A prototype of the calorimeter has shown stable operation for about3years and has provided interesting results6,7.In the third gap from the top of the iron stack(shielded by∼30X0)a layer of456 scintillation detectors is placed to trigger the readout of the calorimeter and other components of the experiment and to measure the arrival times of hadrons.In addition,the trigger layer acts as a muon detector,allowing to determine the lateral-and time distributions of muons above a threshold of about0.4GeV.Underneath the calorimeter,two layers of multiwire proportional chambers(MWPCs)are used to measure muon tracks above an energy threshold of2GeV with an angular accuracy of about1.0◦.North of the central detector a50m long and5.5m wide tunnel has been added to the experiment.In this tunnel600m2of limited-streamer tubes will be used in three layers for tracking of muons under a shielding of18X0,corresponding to an energy threshold of0.8GeV. The tracking accuracy will be around0.5◦.The detector8will have an effective area of about 150m2for the determination of the size and lateral distribution of the muon component and will –for sufficiently large showers–enable approximate determination of the mean muon production height by means of triangulation.Shower simulations with the CORSIKA9code show,that this observable provides another piece of information about the mass of the primary particle.Data taking has started in late1995with large parts of the experiment in stand-alone mode.Correlated data are being collected since April1996with100m2area of the calorimeter operational at the beginning.By now the read-out area has been doubled.The remaining part of the calorimeter and the muon tunnel are expected to start operation in1997.At present,trigger thresholds of the array,trigger plane,and top-cluster are adjusted to limit the total trigger rate to∼1Hz.In the near future this number will be increased to approx.10Hz thereby lowering the effective energy threshold to∼1013eV for specific events.3PRELIMINARY RESULTSOwing to the ongoing installation and calibration work during normal working hours and data taking during nights and over weekends only,analysis is still in a preliminary stage and only a small fraction of the data available could be analyzed.Typically,about half a million of showers-104-104e n e r g y d e p o s i t [M e V /m 2]a r r i v a l t i m e [n s ]Figure 3:Example of an EAS as observed by the elec-tron/gamma detectors of the array.In the two parts,each column represents the energy deposit and the ar-rival time of the shower front,respectively.Recon-structed shower parameters arelisted.log N ei n t e g r a l f l u x /m 2 /s /s r10-510-610-710-810-910-10Figure 4:Event rate as a function of reconstructed shower size for EAS in the zenith angle range 15◦to25◦.per week are collected during this mode of operation.Figure 3shows as an example a shower as registered by the electron/gamma detectors of the array.In the upper part the deposited energies and in the lower part the corresponding arrival times of the same event are shown for each detector station.Parameters resulting from the analysis such as electron number N e ,core position,shower direction,and age are given in the figure.It is obvious from the distributions that these numbers can be determined to high accuracy.The lateral distribution of all charged particles in the shower is analyzed using a NKG function which fits the data nicely within the typical range of our measurement,say 10-200m.The muon signals are analyzed in a similar way,however,due to electromagnetic punch through close to the shower core,this measurement is at present restricted to radii larger than 40m.When we plot the event rate as a function of the reconstructed electron size of the showers in the zenith angle range 15◦to 25◦(see Fig.4)we find a distinct change in the slope near log N e =5.5.These data correspond to only one week of measurement.Both,the position of the break in the spectrum as well as the spectral indices below and above the knee are well in agreement with expectations from earlier experiments.Presently,these data are analyzed in much more detail to carefully correct for effects like trigger thresholds,array efficiency,trigger biases,etc.and to investigate their systematic uncertainties.Simultaneous reconstruction of the electron-and muon size will enable us to determine42 TeV Hadronic Shower Core in KASCADE Calorimeter Figure5:Pattern of signals for a shower core as seen in the3rd layer of the calorimeter.Each box represents the signal of an individual ionization chamber,i.e.the total size of thefigure corresponds to10×16m2.The energy of the shower corresponds to3·1015eV.Total Hadronic Energy (TeV) CountsperBin-2-1101011010101010Hadron-Rate ( s-1 ) Trigger-Rate(θ<24o)(s-1)0.0250.050.0750.10.1250.150.1750.20.225Figure6:Top:)Distribution of the total hadronic energy per EAS above the trigger threshold10.The line shows a power-lawfit with an index of−2.62±0.09.Bottom:)Observed experimental trigger-and hadron rate in comparison to expectations from differ-ent hadronic interaction models(see text for details).their ratio event-by-event.This provides a parameter which has proven large sensitivity to the primary composition.Details of the electron and muon lateral distributions are also studied to get a better understanding of the basic properties of air showers.The influence of atmospheric parameters to the ground level observables of EAS has been calculated and the results will be checked in the ongoing analysis.A unique feature of KASCADE is its large hadronic calorimeter.Measuring the properties of the shower core along with the information from the electron and muon detectors at larger distances will substantially improve the sensitivity to the chemical composition particularly at energies below the knee.Furthermore,the low trigger threshold of approx.1013eV for proton in-duced showers provides a window of significant overlap with direct CR measurements where both the energy-and mass spectrum are known to a reasonable precision.The comparison of EAS and direct measurements will thus serve as a vital test of the hadronic interaction(and atmospheric shower propagation)models.Even in the energy range accessible to operating colliders,up to an equivalent laboratory energy of1.6·1015eV,our knowledge of hadronic interactions is very limited because collider experiments do not cover the very forward fragmentation region.This region is most important to model the hadronic development of EAS and it can be studied by using the calorimeter data itself.Similarly,very energetic single hadrons not accompanied by an air shower can reach ground level after only very few hadronic interactions.Again,their rate as a function of energy is very sensitive to the average hadronic inelasticity and to the inelasticcross section.Here,we report only on veryfirst data on hadronic shower cores10.Figure5shows as an example a two-dimensional pattern of energy deposition in the3rd layer of the calorimeter.This information is available for each of the8readout planes and is used to identify hadron tracks through the calorimeter.Simulations show that the tracking efficiency for E h≥100GeV is larger than90%of for shower energies below1015eV10.In the event shown,the total hadronic energy,as measured by the calorimeter,was42TeV and the energy of the primary particle,as reconstructed from the array data,was about3×1015eV. The multiplicity of reconstructed hadrons in some events exceeds100and the total hadronic energy sum spectrum is plotted in Fig.6(top).The data are well described by a power-law with an index close to that of the primary spectrum.The lateral distribution of hadrons is found toflatten with increasing shower size.In order to quantitatively compare the observed experimental trigger and reconstructed hadron rates with model predictions,detailed simulations have been performed by using composition and energy distributions of primary CR’s as input. These simulated data were fed through the same chain of programs as used for real data and some of the results are shown in Fig.6(bottom).The still preliminary analysis indicates that even small variations of the inelastic cross section used in the model calculations lead to strong effects in the expected rates.Furthermore,none of the models seems to be able to reproduce both the trigger rate(multiplicity≥6in the trigger layer)and the reconstructed hadron rate simultaneously.Although,more detailed studies are required to settle this problem,the data demonstrate the power to experimentally test hadronic interaction models in the very forward region.4CONCLUSIONSThe installation of the KASCADE experiment is nearing completion and data taking with a large part of the experiment has started.Preliminary data of the array and central detector look very promising.No reliable results of composition can be given at the time of writing this report. Mandatory for such an analysis is to prove that(i)the detector and reconstruction methods are understood in detail,and(ii)the hadronic interaction models and atmospheric shower simulations are well under control.An example of such kind of analysis has been discussed briefly.In parallel,multiparameter analyses are under development to infer the composition from the different components of the experiment.References1.A.P.Szabo and R.J.Protheroe,Astropart.Phys.2,375(1994).2.D.M¨u ller et al.,Astrophys.J.374,356(1990).3.M.Ichimura et al.,Phys.Rev.D48,1949(1993).4.H.O.Klages et al.,Proc.9th ISVHECR,Karlsruhe1996,Nucl.Phys.B(Proc.Suppl.)5.H.H.Mielke et al.,Nucl.Instr.Methods A360,367(1995).6.H.H.Mielke et al.,J.Phys.G20,637(1994).7.H.Kornmayer et al.,J.Phys.G21,439(1995).8.P.Doll et al.,Nucl.Instr.Methods A367,120(1995).9.J.N.Capdevielle et al.,Kernforschungszentrum Karlsruhe,Report KfK4998(1992)10.J.Unger,Doctoral Thesis,University of Karlsruhe(1997)Total Hadronic Energy (TeV)C o u n t s p e r B i n-2-123410101101010101051。

英语语法Verb and Verb Phrase

英语语法Verb and Verb Phrase
I believe we have met before.
Jim knows Chinese.
Notes
The above-mentioned stative can sometimes be used dynamically.
1) The verb “be” and the verb “have” are in most cases used as stative verbs, but when “be” is not used as a linking verb and “have” is not used in the sense of “possession”, they are dynamic verbs and therefore admit of the progressive aspect, eg: He is being foolish (=is acting foolishly). We’re having a wonderful time (= are enjoying ourselves).
He resembles his father. / He is resembling his father (= is becoming more and more like his father) as the years go by.
This camera costs 140 dollars. / This mistake is costing us dearly (=is bring great injury to us).
people.
c) The third subclass includes verbs that refer to a sense perception, such as hear, see, feel, taste, smell, etc:

基于ANSYS的刚性导轨结构动态仿真说明书

基于ANSYS的刚性导轨结构动态仿真说明书

Dynam i c S i mulat i on of R i g i d Gu i de Structure Based on ANSYSZHANG Xin1,a and WANG Zhe21Anhui University of Science and Technology, Huainan Anhui, China2Anhui University of Science and Technology, Huainan Anhui, ChinaAbstract. In order to reflect the varying law of the deflection of the rigid guide when therelative motion occur between the rigid guide and the cage roller, transient dynamic simulationis carried out for the commonly used calculation model of rigid guide and bunton by ANSYS.Simulation of the horizontal force through a section of the guide evenly, and the deflectioncurves of each model are obtained. It is found that the deflection of the simply supported beammodel is the largest, and the three-span continuous beam model have similar peak spans in eachspan with the spatial grid model, but the spatial grid model has obvious fluctuation with thehorizontal force.1 IntroductionRigid guide is an important part of shaft equipment. At present, the simple beam model and the three-span continuous beam model is still widely used in the calculation of bending resistance of the guide, and the influence of the space structure composed of guide and bunton is not taken into account. The bending moment of the force point is too large, so that the design value tends to be conservative[1]. But the research on the difference of deflection of each model under the action of the moving load is still blank.In this paper, the transient dynamic simulation of these three models under the action of the moving load is carried out by ANSYS to get the deflection changes in the midpoint. Then export the data to MATLAB, so the curves of the variation of deflection in each span about the simple beam model, three-span equal-span continuous beam model and spatial grid model under the moving load are presented. It has a certain guiding significance for the structural design calculation of rigid guide and bunton.2 Calculation Model of Rigid Guide and BuntonThe dynamic load transmitted by the hoisting conveyance be resisted by rigid guide and bunton in the hoisting process, the guide structure has an important impact on the safety and reliability of the hoisting conveyance[2]. The design and calculation of guide now, the majority consider static function at one point. However, in most of the hoisting process the role of the horizontal force is not stage but continuous, so considering the load through the rigid guide at a uniform speed, a variety of rigid guide a ZHANGXin:***************.cndeflection curve calculation model is necessary. In the stage of uniform hoisting of the hoisting conveyance, it is assumed that the transverse horizontal force acting on the guide by the cage roller does not change, so the simply supported beam model, three-span continuous beam model and spatial grid model can be built in Figure 1. The force of the cage roller on the guide is simplified as a force perpendicular to the beam, the relative motion of the cage roller and the guide into a uniform translation is simplified as a force along the axis of the beam.Figure 1.Three Simulation Models.In the simple supported beam model, both ends of the guide are considered to be hinged; both ends of the three-span continuous beam model are considered to be hinged, and the middle two nodes are regarded as rigid contact3 Calculation of Mid-Span Deflection of ModelFor the maximum deflection of the simple beam model and the three-span continuous beam model, according to the mechanics of materials and the use of building structure statics to get its formula. In the simply supported beam model, the maximum deflection occurs when the load is applied to the mid-span nodes; in the three-span continuous beam model, the maximum deflection occurs when loads are applied to the three mid-span joints respectively[3].Equations of the maximum deflection of the simply supported beam model:इ௠௔௫=−௟ி௟య(1)ସ଼ாூEquations of the maximum deflection of the three-span continuous beam model:इ௠௔௫=−ܭ×ி௟య(2)ଵ଴଴ாூThe meaning of each parameter:• F is the force;• ݈is the length of the single-layer canal (ie, the distance between the canopy beam layer);• E is the elastic modulus of the material;• I is the section moment of inertia;• K is the maximum deflection calculation factor obtained by the look-up table.According to the actual data:F= 8000N݈= 4mE =2.06 × 10 MP(3)ܫ=஻ுయି௕௛యଵଶIn the mid-span of the first span and the third span in the three-span continuous beam:K = 1.458 (4) In the second span.:K = 1.146 (5) So the following data can be calculated:The maximum deflection of the simply supported beam model is:इ௠௔௫=−1.57mm(6) The maximum deflection of the three-span continuous beam is:The mid-span of the first and third span:इ௠௔௫=−1.12mm(7) The mid-span of the second span:इ௠௔௫=−0.86mm (8) However, it is not easy to calculate the deflection of each span in the spatial grid structure. In order to obtain the deflection of the spatial grid structure under the moving load, it is necessary to carry on the finite element simulation analysis.4 Finite Element Simulation Analysis4.1 Define MaterialsAccording to the design data of a mine, both sides of the guide are arranged in parallel. The length of the guide is 12 m, two guides are located 1.8 m apart, the length of the bunton is 4.86 m, the span of bunton is 4 m, the short beam length of the connecting guide and bunton in the spatial grid model is 0.1 m. Materials are Q235 cold-formed square steel, cross-sectional size of 180 × 180 × 10.According to the above data beam, the analysis model is established in ANSYS, set the modulus of elasticity for 2.06×10ହܯܲ, poisson's ratio is 0.3, the density is 7800kg/݉ଷ, choose the BEAM188 three-dimensional beam element.4.2 Meshing, Applying Constraints and LoadsThe size of the global control element is 0.1m, and the guide length 12m used to apply the load is divided into 120 elements with 121 nodes. For both ends of the hinge point, constrain the X, Y, Z direction of displacement; for the model of spatial grid structure, constrain the UX, UZ, RO TX, RO TY, RO TZ degrees of freedom of the short beam at the junction of the guide and the bunton; constrain the UX, UY, UZ degrees of freedom at both ends of the bunton. The spatial grid structure is shown in Figure 2. In this paper, we use the * DO loop to apply the load to the 121 nodes of the guide in order to simulate the relative motion between the guide and the cage roller by using the method of moving load in the vehicle-bridge analysis model[4-5].Figure 2.Spatial Grid Structure Model Meshing and Constraints.According to the data, the pre-tightening force of the Y direction of the cage roller is 8000N, the speed of the uniform speed is 8m/s. Assuming the uniform speed does not impact on the guide, defining the moving load P is 8000N, along the Y axis negative direction, and the moving speed is 8m / s, along the X axis positive direction.4.3 Simulation ResultsThe NSO L function is used to extract the displacement value of the Y direction of the simple supported beam, the displacement values of the three mid-span nodes in the Y direction of the three-span continuous beam model and the spatial grid model. Then export the data to MATLAB, take the time as the X axis, the displacement as the Y axis, draws the displacement - time curve, as shown inFigure 3Figure parison of Mid-Span Deflection of Each Model.5 Result AnalysisAccording to the simulation results, the maximum deflection values in each span of the simply supported beam model, three-span continuous beam model and spatial grid model are shown in Table 1.Table 1. Maximum deflection values in each span(mm).First Mid-span Second Mid-span Third Mid-spanSimulat -ion Theoret-icalDeviati-onSimulat-ionTheoret-icalDeviati-onSimulat-ionTheoret-icalDeviati-onSimplySupportedBeam-1.64-1.570.07Three-spanContinuousBeam-1.15-1.120.03-0.90-0.860.04-1.15-1.120.03Spatial GridModel-0.93-0.92-0.93It can be seen from Table 1 that when the calculation model of guide and bunton is calculated according to the simple supported beam, its mid-span deflection will be much larger than that of three-span continuous span beam and spatial grid model. So it is necessary to increase the cross-sectional area of the guide or the use of higher bending stiffness of the material, thereby increasing costs[6].At the same time,it can be seen from the table that the maximum deflection of the mid-span of the simple beam model and the three span continuous beam model are basically the same as the theoretical calculation result.The deflections of the three-span continuous beam model and the spatial grid model are similar at the maximum. However, according to the comparison of mid-span deflection curves, the mid-span deflection of the three-span continuous beam is relatively gentle, but the mid-span deflection of the spatial grid model is more violent, which is bound to produce vibration, impact on the stability of the guide structure6 Conclusion• Finite element simulation deviation within the allowable range. So the finite element method can be used to simulate the spatial structure of the guide structure;• The deflection of the simply supported beam model is much greater than that of the three-span continuous beam and spatial grid model. The maximum deflection in each span is similar to the three-span continuous beam model when calculated by the space grid model;• Compared with the three-span continuous beam model, when the space grid structure is used, the mid-span deflection of each span is more violent under the moving load. In the design calculation of the tank, to take into account this situation, to avoid fatigue damage.• Compared with the theoretical calculation, the finite element method is more consistent with the actual working conditions, especially for the analysis of complex moving loads, the use of finite element simulation can provide the necessary reference for the design and calculation. AcknowledgementsThis research was supported by the Key Project of Natural Science Foundation for Anhui University (No.KJ2015ZD019).References1.Wang Dongquan,Shi Tiansheng,Liu Zhiqiang and Guo Jinpu. Method for Calculating theStructure of Rigid Shaft Equipment of Deep Mine. Journ al of Chin a Un iversity of Min in g& Technology. 26(1):5̚8,(1997)2.Qin Qiang,QI Xiao-nan,Ding Jian-guo and Jian Hui. Analysis on Shaft Guide Equipment Quality.Coal Mine Machinery .36(6):168-170,(2015).3.Guo Zhenxi,Zhang Shuyi.Static Caculation Handbook for Practical Strucyure. China MachinePress. 4:320-322,(2009)4.Ge Junying. Analysis of Bridge Structure Based on ANSYS. China Railway Publishing House.8:150-156,(2007).5.SANMANI F S,PELLICANO F.Vibration reduction on beams subiected to moving loads usinglinear and nonlinear dynamic aborbers[J].Journal of Sound and Vibration. 325:742̚754,(2009) 6.Jiang Yuqiang. Research on Nonlinar Coupling Characteristcs and Condition Assessment ofVertical Steel Guide System. China University of Mining and Technology.(2011).。

对数索伯里夫不等式:曲率和海森张量的不同角色

对数索伯里夫不等式:曲率和海森张量的不同角色

Log-Sobolev Ineqaulities:Different Roles ofRic and Hess ∗Feng-Yu WangDepartment of Mathematics,University of Wales Swansea,Singleton Park,SA28PP,UKEmail:F.Y.Wang@October 24,2007AbstractLet P t be the diffusion semigroup generated by L :=∆+∇V on a completeconnected Riemannian manifold with Ric ≥−(σ2ρ2o +c )for some constants σ,c >0and ρo the Riemannian distance to a fixed point.It is shown that P t is hypercontrac-tive,or the log-Sobolev inequality holds for the associated Dirichlet form,provided −Hess V ≥δholds outside of a compact set for some constant δ>(1+√2)σ√d −1.This indicates,at least in finite dimensions,that Ric and −Hess V play quite dif-ferent roles for the log-Sobolev inequality to hold.The supercontractivity and theultracontractivity are also studied.AMS subject Classification:60J60,58G32.Keywords:Log-Sobolev inequality,Ricci curvature,Riemannian manifold,diffusion semi-group.1IntroductionLet M be a d -dimensional completed connected non-compact Riemannian manifold and V ∈C 2(M )such that Z := M e V (x )d x <∞,where d x is the volume measure on M .Let µ(d x )=Z −1e V (x )d x.Then P t ,the semigroup of the diffusion process generated by L :=∆+∇V ,is symmetric in L 2(µ).It is well-known by the Bakry-Emery criterion that (see [4])(1.1)Ric −Hess V ≥K ∗Supported in part by NNSFC(10121101),the 973-Project in China and RFDP(20040027009).for some constant K>0implies the Gross log-Sobolev inequality[15](1.2)µ(f2log f2):=Mf2log f2dµ≤Cµ(|∇f|2),µ(f2)=1,f∈C1(M)for C=2/K.This result was extended by Chen and the author[10]to the situation that Ric−Hess V is uniformly positive outside a compact set.In the case that Ric−Hess V is bounded below,sufficient concentration conditions ofµfor(1.2)to hold are presented in[20,1,21].Obviously,in a condition on Ric−Hess V the Ricci curvature and−Hess V play the same role.What can we do when Ric−Hess V is unbounded below?It seems very hard to confirm the log-Sobolev inequality with an unbounded below condition of Ric−Hess V.So,in this paper we try to clarify the roles of Ric and−Hess V in the study of the log-Sobolev inequality.Let usfirst recall the gradient estimate of P t,which is a key point in the above references to prove the log-Sobolev inequality.Let x t be the L-diffusion process starting at x,and let v∈T x M.Due to Bismut[6] and Elworthy-Li[12],under a reasonable lower bound condition of Ric−Hess V,one has∇P t f,v =E ∇f(x t),v t ,t>0,f∈C1b(M),where v t∈T xtM solves the equationD t v t:=//−1t→0dd t//t→0v t=−(Ric−Hess V)#(v t)for//t→0:T xtM→T x M the associated stochastic parallel displacement,and(Ric−Hess V)#(v t)∈T xtM with(Ric−Hess V)#(v t),X :=(Ric−Hess V)(v t,X),X∈T xtM.Thus,for the gradient of P t,which is a short distance behavior of the diffusion process,a condition on Ric−Hess V appears naturally.On the other hand,however,Ric and−Hess V play very different roles for long distance behaviors.For instance,Letρo be the Riemannian distance function to afixed point o∈M.If Ric≥−k and−Hess V≥−δfor some k≥0,δ∈R,the Laplacian comparison theorem impliesLρo≤k(d−1)cothk/(d−1)ρo+δρo.So,for largeρo the Ric lower bound leads to a bounded term while that of−Hess V provides a linear term.The same phenomena appears to the formula on distance of coupling by parallel displacement(cf.[3,(2.3),(2.4)]),which implies the above Bismut-Elworthy-Li formula by letting the initial distance tend to zero(cf.[16]).Here,k≥0is essential for our framework since the manifold has to be compact if Ric is bounded below by a positive constant.Since the log-Sobolev inequality is always available on bounded regular domains,it is more likely a long distance behavior of the diffusion process.Thus,we would conclude that Ric and −Hess V take different roles to ensure the validity of the log-Sobolev inequality.Indeed,it has been observed by the author [21]that (1.2)holds for some C >0provided Ric is bounded below and −Hess V is uniformly positive outside a compact set.So,for the validity of the log-Sobolev inequality,the positivity of −Hess V is a dominative condition,which allows the Ricci curvature has arbitrary negative constant lower bound,and hence allows Ric −Hess V to be globally negative.The first aim of this paper is to search for the weakest possibility of curvature lower bound for the log-Sobolev inequality to hold under the condition(1.3)−Hess V ≥δoutside a compact setfor some constant δ>0.This condition is reasonable as the log-Sobolev inequality implies µ(e λρ2o )<∞for some λ>0,see e.g.[2,18].According to the following Theorem 1.1and Example 1.1,we conclude that under (1.3)the optimal curvature lower bound condition for (1.2)to hold is(1.4)Ric ≥−(c +σ2ρ2o )for some constants c,σ>0.More precisely,let θ0>0be the smallest positive constant such that for any connected complete non-compact Riemannian manifold M and V ∈C 2(M ),the conditions (1.3)and (1.4)with δ>σθ0√d −1implies Z <∞and (1.2)for some C >0.Due to Theorem 1.1and Example 1.1below,we conclude thatθ0∈[1,1+√2].The exact value of θ0is however unknown.Recall that P t is called supercontractive if P t 2→4<∞for all t >0while ultracon-tractive if P t 2→∞<∞for all t >0(see [11]).In the present framework these two properties are stronger than the hypercontractivity: P t 2→4≤1for some t >0,which is equivalent to (1.2)due to Gross [15].Theorem 1.1.Assume that (1.3)and (1.4)hold for some constants c,δ,σ>0with δ>(1+√2)σ√d −1.Then (1.2)holds for some C >0.Further more,P t is supercontractive if and only if µ(exp[λρ2o ])<∞for all λ>0,while it is ultracontractive if and only if P t exp[λρ2o ] ∞<∞for all t,λ>0.Example 1.1.Let M =R 2be equipped with the rotationally symmetric metricd s 2=d r 2+ re kr 2 2d θ2under the polar coordinates (r,θ)∈[0,∞)×S 1at 0,where k >0is a constant.Then (see e.g.[14])Ric =−d 2d r2(r e kr 2)r e kr =−4k −4k 2r 2.Thus,(1.4)holds for σ=2k.Next,take V =−δ2ρ2o .By the Hessian comparison theorem and the negativity of the sectional curvature,we obtain (1.3).Since d =2ande V (x )d x =r e kr 2−δr 2/2d r d θ,one has Z <∞if and only if δ>2k =σ√d −1.Therefore,θ0≥1.Following the line of [20,21],the key point in the proof of Theorem 1.1will be a proper Harnack inequality of type(P t f (x ))α≤C α(t,x,y )P t f α(y ),t >0,x,y ∈M for any nonnegative f ∈C b (M ),where α>1is a constant and C α∈C ((0,∞),M 2)is a positive function.Such an inequality was established in [20]for Ric −Hess V bounded below and extended in [3]to a more general situation with Ric satisfying (1.4).The Harnack inequality presented in [3]contains a leading term exp[ρ(x,y )4],which is however too large to be integrability w.r.t.µ×µunder our conditions.So,to prove Theorem 1.1,we shall present a sharper Harnack inequality in Section 3by refining the coupling method introduced in [3](see Proposition 3.1below).This inequality,together with the concentration of µensured by (1.3)and (1.4),will imply the hypercontractivity of P t .To establish this new Harnack inequality,some necessary preparations are presented in Section 2.Finally,Theorem 1.1is extended in Section 4to the case that −Hess V ≥Φ◦ρo outside a compact set for an increasing positive function Φwith Φ(r )↑∞as r ↑∞.2PreparationsWe first study the concentration of µby using (1.3)and (1.4),for which we need to estimate Lρo from above according to [5]and references within.Lemma 2.1.If (1.3)and (1.4)hold then there exists a constant C 1>0such that(2.1)Lρ2o≤C 1(1+ρo )−2 δ−σ√d −1 ρ2oholds outside cut(o ),the cut-locus of o .If moreover δ>σ√d −1then Z <∞and µ(e λρ2o )<∞for all λ<12(δ−σ√d −1).Proof.By (1.4)and the Laplacian comparison theorem,∆ρo ≤ (c +σ2ρ2o )(d −1)coth(c +σ2ρ2o )/(d −1)ρo holds outside cut(o ).Thus,outside cut(o )one has∆ρ2o ≤2ρo (c +σ2ρ2o )(d −1)coth (c +σ2ρ2o )/(d −1)ρo +2≤2d +2ρo (c +σ2ρ2o )(d −1),(2.2)where the second inequality follows from the fact thatr cosh r ≤(1+r )sinh r,r ≥0.On the other hand,for x /∈cut(o )and U the unit tangent vector along the unique minimal geodesic form o to x ,by (1.3)there exists a constant c 1>0independent of x such that∇V,∇ρo (x )= ∇V,U (o )+ρo (x )0Hess V (U,U )( s )d s ≤c 1−δρo (x ).Combining this with (2.2)we prove (2.1).Finally,let δ>σ√d −1and 0<λ<12(δ−σ√d −1).By (2.1)we haveL e λρ2o ≤λe λρ2o C 1(1+ρo )−2 δ−σ√d −1 ρ2o +4λρ2o≤c 2−c 3ρ2o eλρ2o for some constants c 2,c 3>0.By [5,Proposition 3.2],this implies Z <∞andMρ2o e λρ2o d µ≤c 2c 3<∞.Lemma 2.2.Let x t be the L -diffusion process with x 0=x ∈M.If (1.3)and (1.4)hold with δ>σ√d −1,then for any δ0∈(σ√d −1,δ)there exists a constant C 2>0such thatE exp (δ0−σ√d −1)24 T 0ρo (x t )2d t ≤exp C 2T +14(δ0−σ√d −1)ρo (x )2 ,T >0,x ∈M.Proof.By Lemma 2.1,we haveLρ2o ≤C −2(δ0−σ√d −1)ρ2o outside cut(o )for some constant C >0.Then the Itˆo formula for ρo (x t )due to Kendall[17]implies that(2.3)d ρ2o (x t )≤2√2ρo (x t )d b t + C −2(δ0−σ√ρ2o (x t ) d t holds for some Brownian motion b t on R.This implies that the L-diffusion process is non-explosive so thatT n:=inf{t≥0:ρo(x t)≥n}→∞as n→∞.For anyλ>0and n≥1,it follows from(2.3)thatE exp2λδ0−σ√d−1T∧T nρ2o(x t)d t≤eλρ2o(x)+CλT E exp2√2λT∧T nρo(x t)d b t≤eλρ2o(x)+CλTE exp16λ2T∧T nρ2o(x t)d t1/2.Thus,takingλ=18(δ0−σ√d−1)we obtainE exp14δ0−σ√d−12 T∧T nρ2o(x t)d t≤exp14δ0−σ√d−1ρ2o(x)+C2Tfor some C2>0.Then the proof is completed by letting n→∞.Finally,we recall the coupling argument introduced in[3]for establishing the Harnack inequality of P t.Let T>0and x=y∈M befixed.Then the L-diffusion process starting from x can be constructed by solving the following Itˆo stochastic differential equationd I x t=√2Φt d B t+∇V(x t)d t,x0=x,where d I is the Itˆo differential on manifolds introduced in[13](see also[3]),B t is the d-dimensional Brownian motion,andΦt is the horizontal lift of x t onto the orthonormal frame bundle O(M).To construct another diffusion process y t starting from y such that x T=y T,as in[3] we add an additional drift term to the equation(as explained in[3,Section3],we may and do assume that the cut-locus of M is empty):d I y t=√2P xt,y tΦt d B t+∇V(y t)d t+ξt U(x t,y t)1{t<τ}d t,y0=y,where P xt,y t is the parallel transformation along the unique minimal geodesic from x t toy t,U(x t,y t)is the unit tangent vector of at y t,ξt≥0is a smooth function of X t to be determined,andτ:=inf {t ≥0:x t =y t }is the coupling time.Since all terms involved in the equation are regular enough,there exists a unique solution y t .Furthermore,since the additional term containing 1{t<τ}vanishes from the coupling time on,one has x t =y t for t ≥τdue to the uniqueness of solutions.Lemma 2.3.Assume that (1.3)and (1.4)hold with δ≥2σ√d −1.Then there existsa constant C 3>0independent of x,y and T such that x T =y T holds for ξt :=C 3+2σ√d −1ρo (x t )+ρ(x,y )T.Proof.According to Section 2in [3],we have(2.4)d ρ(x t ,y t )= I (x t ,y t )+ ∇V,∇ρ(·,y t ) (x t )+ ∇V,∇ρ(x t ,·) (y t )−ξt d t,t <τ,whereI Z (x t ,y t )=d −1i =1 ρ(x t ,y t )0 |∇U J i |2− R (U,J i )U,J i ( s )d s for R the Riemann curvature tensor,U the unit tangent vector of the minimal geodesic:[0,ρ(x t ,y t )]→M from x t to y t ,and {J i }d −1i =1the Jacobi fields along which,togetherwith U ,consist of an orthonormal basis of the tangent space at x t and y t and satisfyJ i (y t )=P x t ,y t J i (x t ),i =1,...,d −1.LettingK (x t ,y t )=sup {c +σ2ρ2o },we obtain from (1.4)and [22,Theorem 2.14](see also [9,8])that(2.5)I (x t ,y t )≤2 K (x t ,y t )(d −1)tanh ρ(x t ,y t )2 K (x t ,y t )/(d −1) .Moreover,(1.3)implies∇V,∇ρ(·,y t ) (x t )+ ∇V,∇ρ(x t ,·) (y t )= ρ(x t ,y t )Hess V (U,U )( s )d s ≤c 1−δρ(x t ,y t )for some constant c 1>bining this with (2.4),(2.5)and ξt =C 3+2σ√d −1ρo (x t )+ρ(x,y )T,we arrive at d ρ(x t ,y t )≤ 2 K (x t ,y t )(d −1)+c 1−δρ(x t ,y t )−C 3−2σ√d −1ρo (x t )−ρ(x,y )Td t for t <τ.Noting that K (x t ,y t )≤ c +σ2ρo (x t )+ρ(x t ,y t ) 2 1/2≤√c +σ ρo (x t )+ρ(x t ,y t ) and δ≥2σ√d −1,one has2 K (x t ,y t )(d −1)−δρ(x t ,y t )−2σ√d −1ρo (x t )≤2 c (d −1).Thus,when C 3≥c 1+2 c (d −1)we haved ρ(x t ,y t )≤−ρ(x t ,y t )T,t <τ.This implies that τ≤T and hence,x T =y T .3Harnack inequality and proof of Theorem 1.1We first prove the following Harnack inequality using results in Section 2.Proposition 3.1.Assume that (1.3)and (1.4)hold with δ>(1+√2)σ√d −1.Thenthere exist C >0and α>1such that(3.1)(P T f (y ))α≤(P T f α(x ))exp CT ρ(x,y )2+C (T +ρo (x )2) holds for all x,y ∈M,T >0and nonnegative f ∈C b (M ).Proof.According to Lemma 2.3,we takeξt =C 3+2σ√d −1ρo (x t )+ρ(x,y )Tsuch that τ≤T and x T =y T .LetR =exp 1√2 τ0 P x t ,y t Φt d B t ,ξt U (x t ,y t ) −14 τ0ξ2t d t .By the Girsanov theorem,the H¨o lder inequality,and noting that x T =y T ,we have P T f (y )=E [f (y T )R ]=E [f (x T )R ]≤(P T f α(x ))1/α(E R α/(α−1))(α−1)/α.That is,(3.2)(P T f (y ))α≤(P T f α(x ))(E R α/(α−1))α−1.Since for any exponential integrable martingale M t and any β>1one has(3.3)E e βM t −β2 M t =E e βM t −β2p 2 M t ·e β(βp −1)2 M t ≤ e βp (βp −1)2(p −1)M t (p −1)/p ,p >1,by taking β=α/(α−1)we obtain(3.4)(E R α/(α−1))α−1≤ E exp pα(pα−α+1)8(p −1)(α−1)2 T 0ξ2t d t (α−1)(p −1)/p ,p >1.Since δ>(1+√2)σ√d −1,we may take δ0∈((1+√2)σ√d −1,δ),small ε >0andlarge C 4>0,independent of T,x and y ,such thatξ2t = C 3+2σ√o (x t )+ρ(x,y )T 2≤(1−ε ) C 4+C 4ρ(x,y )2T 2+2(δ0−σ√d −1)2ρo (x t )2 holds.Moreover,since(3.5)lim p ↓1lim α↑∞pα(pα−α+1)8(p −1)(α−1)2=18,there exist p,α>1such thatpα(pα−α+1)8(p −1)(α−1)2 T 0ξ2t d t ≤C 4T +C 4ρ(x,y )2T +(δ0−σ√d −1)24 T 0ρo (x t )2d bining this with (3.4)and Lemma 2.2,we obtain (E R α/(α−1))α−1≤exp C 5T +C 5ρ(x,y )T+C 5ρo (x )2 ,T >0,x ∈M for some constant C 5>0.This completes the proof by taking large enough T >0such that C 5≤T ε.Proof of Theorem 1.1.By Proposition 3.1,let α>1and C >0such that (3.1)holds.Since δ>σ√d −1,we may take T >0such that C T ≤ε:=18δ−σ√d −1 .Then for any nonnegative f ∈C b (M )with µ(f α)=1,it follows from (3.1)that1= M P T f α(x )µ(d x )≥(P T f (y ))α M e −ερ(x,y )2−C (1+ρo (x )2)µ(d x )≥(P T f (y ))α {ρo ≤1}e −ε(1+ρo (y ))2−2C µ(d x )≥ε (P T f (y ))αexp[−2ερo (y )2],y ∈Mfor some constant ε >0.Thus,M(P T f (y ))2αµ(d y )≤1ε M e 4ερo (y )2µ(d y )<∞according to Lemma 2.1.This implies thatP T L α(µ)→L 2α(µ)<∞.Therefore,the log-Sobolev inequality (1.2)holds for some constant C >0due to the uniformly positively improving property of P t (see the proof of [21,Theorem 1.1]and[1]).Finally,due to the Harnack inequality (3.1),the assertions on supercontactivity and ultracontractivity follow from the proof of [19,Theorem 2.3]4Extension to general negative curvature lower bounds In this section we work with a stronger lower bound condition on −Hess V :(4.1)−Hess V ≥Φ◦ρo holds outside a compact subset of M,for a positive increasing function Φwith Φ(r )↑∞as r ↑∞.We aim to search for reasonable conditions on positive increasing function Ψsuch that(4.2)Ric ≥−Ψ◦ρoimplies the supercontractivity and/or ultracontractivity.Theorem 4.1.If (4.2)and (4.1)hold for some increasing positive functions Φand Ψsuch that(4.3)lim r →∞Φ(r )=lim r →∞( r 0Φ(s )d s )2Φ(r )=∞,(4.4) Ψ(r +t )(d −1)≤θ rΦ(s )d s +12 t/20Φ(s )d s +C,r,t ≥0for some constants θ∈(0,1/(1+√2))and C >0.Then P t is supercontractive.If furthermore (4.5)∞1d s √s √r0Φ(u )d u<∞,then P t is ultracontractive.More precisely,forΓ1(r ):=1√r√r 0Φ(s )d s,Γ2(r ):=∞rd s√s√sΦ(u )d u,r >0,(4.5)implies(4.6) P t 2→∞≤expc +c t1+Γ−11(c/t )+Γ−12(t/c ) <∞,t >0for some constant c >0andΓ−11(s ):=inf {t ≥0:Γ1(t )≥s },s ≥0.Proof.(a)Replacing c +ρ2o by Ψ◦ρo and noting that Hess V ≤−Φ◦ρo for large ρo ,theproof of Lemma 2.1implies (4.7)Lρ2o ≤c 1(1+ρo )−2ρoρoΦ(s )d s −Ψ◦ρo (d −1)for some constant c 1>bining this with (4.4)and noting that 1ρoρoΦ(s )d s →∞as ρo →∞,we conclude that for any λ>0L e λρ2o ≤C −2λρo √21+√2e λρ2o ρo0Φ(s )d s +4λ2ρ2oe λρ2o ≤C +C (λ)−λρo e λρ2o ρoΦ(s )d s,(4.8)where C >0is a universal constant andC (λ):=sup r>0r e λr 24λ2r −λ(1+√2)2 rΦ(s )d s=sup r 2≤Γ−114(1+√2)2λ r e λr2 4λ2r −λ(1+√2)2 r0Φ(s )d s ≤4λ2Γ−11 4(1+√2)2λ exp λΓ−11 4(1+√2)2λ≤exp 4λ+2λΓ−11 4(1+√2)2λ <∞.(4.9)Therefore,Z <∞and (4.10)µ(e λρ2o )<∞,λ>0.(b)By (4.4),(4.7)and Kendall’s Itˆo formula [17]as in the proof of Lemma 2.2,we haved ρ2o (x t )≤2√o (x t )d b t + C 1−2√2ρo (x t)(1+ε)1+√2 ρo (x t )Φ(s )d s d t for some constants ε,C 1>0,where x t and b t are in the proof of Lemma 2.2.Let(4.11)ϕ(r )=r0d s√s√sΦ(u )d u,r ≥0.We arrive atd ϕ◦ρ2o (x t )≤2√2ρo (x t )ϕ ◦ρ2o (x t )d b t +4ρ2o (x t )ϕ ◦ρ2o (x t )d t+ϕ ◦ρ2o (x t ) C 1−2√2ρo (x t)(1+ε)1+√2 ρo (x t )0Φ(s )d s d t.From (4.3)we see thatρo ϕ ◦ρ2o ϕ ◦ρ2o ρo 0Φ(s )d s≤Φ◦ρo 2( ρo 0Φ(s )d s )2which goes to zero as ρo →∞.Then there exists a constant C 2>C 1such thatd ϕ◦ρ2o (x t )≤2√2ρo (x t )Φ(s )d sd b t +C 2d t −2√21+√2 ρo (x t )0Φ(s )d s 2d t.This implies that for any λ>0E exp2√2λ1+√2 T 0 ρo (x t )Φ(s )d s 2d t ≤e C 2λT +λϕ◦ρ2o (x )E exp 2√2λ T 0ρo (x t )0Φ(s )d s d b t ≤eC 2λT +λϕ◦ρ2o (x )E exp 16λ2Tρo (x t )Φ(s )d s 2d t 1/2.Takingλ=√28(1+√2),we arrive at(4.12)E exp12(1+√2)2Tρo(x t)Φ(s)d s2d t≤e2C2T+ϕ◦ρ2o(x)√2/8(1+√2).(c)Letγ:[0,ρ(x t,y t)]→M be the minimal geodesic from x t to y t,and U its tangent unit vector.By(4.2)we have∇V,∇ρ(·,y t) (x t)+ ∇V,∇ρ(x t,·) (y t)=ρ(x t,y t)0Hess V(U s,U s)d s≤−ρ(x t,y t)/2Φ(s)d s.(4.13)To understand the last inequality,we assume,for instance,thatρo(x t)≥ρo(y t)so that by the triangle inequality,ρo(γs)≥ρo(x t)−s≥ρ(x t,y t)/2−s,s∈[0,ρ(x t,y t)/2].For the coupling constructed in Section3,one concludes from(4.13)and the proof of Lemma2.3that(4.14)dρ(x t,y t)≤2K(x t,y t)(d−1)+C3−ρ(x t,y t)/2Φ(s)d s−ξtd t,t<τholds for some constant C4>0,whereK(x t,y t):=supΨ◦ρo≤Ψ(ρo(x t)+ρ(x t,y t))and is the minimal geodesic from x t to y bining this(4.4)and(4.14),we obtaindρ(x t,y t)≤C4+2θρo(x t)Φ(s)d s−ξtd t,t<τ.So,takingξt=C4+2θρo(x t)0Φ(s)d s+ρ(x,y)T,we arrive atdρ(x t,y t)≤−ρ(x,y)Td t,t<τ.This impliesτ≤T and hence x T=y T a.s.Combining(4.4)with(3.4)and(3.5)we conclude that for the present choice ofξt there existα,p,C5>1such thatE Rα/(α−1) p/(p−1)≤E exp12(1+√2)2Tρ(x t)Φ(s)d s2d t+C5T+C5Tρ(x,y)2.Combining this with(4.12)and(3.2)we obtain(4.15)(P T f(y))α≤(P T fα(x))expCT+CTρ(x,y)2+Cϕ◦ρ2(x)holds for someα,C>1,any positive f∈C b(M)and all x,y∈M,T>0.(d)For any positive f∈C b(M)withµ(fα)=1,(4.15)implies that(P T f(y))αB(o,1)exp−CT−CTρ(x,y)2−Cϕ2(x)µ(d x)≤1.Therefore,there exists a constant C >0such that(4.16)(P T f(y))α≤expC (1+T)+CTρ(y)2,y∈M,T>0.Combining this with(4.10)we obtainP T α→pα<∞,T>0,p>1.This is equivalent to the supercontactivity by the Riesz-Thorin interpolation theorem and P t 1→1=1.Thus,thefirst assertion holds.(e)To prove(4.6),it suffices to consider t∈(0,1]since P t 2→∞is decreasing in t>0. So,below we assume that T≤1.By(4.16)and the fact that(P2T f)α≤P T(P T f)α,we have(4.17) P2T α→∞≤ P T e2C ρ2o/T ∞e C (1+T),T>0.So,by the Riesz-Thorin interpolation theorem and P t 1→1=1,for the ultracontractivity it suffices to show that(4.18) P T eλρ2o ∞<∞,λ,T>0.SinceΦis increasing,it is easy to check thatη(r):=√r√rΦ(s)d s,r≥0is convex,and so is s→sη(log sλ)forλ>0.Thus,it follows from(4.8)and the Jenseninequality thathλ,x(t):=E eλρ2o(x t)<∞,x0=x∈M,λ,t>0andd+d thλ,x(t)≤C+C(λ)−λhλ,x(t)η(λ−1log hλ,x(t)),t>0.This implies(4.18)provided(4.5)holds.This can be done by considering the following two situations.(1)Since hλ,x(t)is decreasing providedλhλ,x(t)η(λ−1log hλ,x(t))>C+C(λ),ifλhλ,x(0)η(λ−1log hλ,x(0))≤2C+2C(λ)thenhλ,x(t)≤sup{r≥1:λrη(λ−1log r)≤2C+2C(λ)}≤1λ(2C+2C(λ))+Cfor some constant C >0.(2)Ifλhλ,x(0)η(λ−1log hλ,x(0))>2C+2C(λ),then hλ,x(t)is decreasing in t up totλ:=inf{t≥0:λhλ,x(t)η(λ−1log hλ,x(t))≤2C+2C(λ)}.Indeed,d+ d t hλ,x(t)≤−λ2hλ,x(t)η(λ−1log hλ,x(t)),t≤tλ.Thus,∞hλ,x(T∧tλ)d rrη(λ−1log r)≥λ2(T∧tλ).This is equivalent toΓ2(λ−1log hλ,x(T∧tλ))≥12(T∧tλ).Hence,hλ,x(T∧tλ)≤expλΓ−1212(T∧tλ).Since it is reduced to case(1)if T>tλby regarding tλas the initial time,in conclusion we havesup x∈M hλ,x(T)≤maxexpλΓ−12T/2,C +1λ(2C+2C(λ)).Therefore,(4.6)follows from(4.17),(4.9)withλ=2C /T,and the Riesz interpolation theorem.Finally,we note that a simple example for conditions in Theorem4.1to hold isΦ(s)=sα−1,Ψ(s)=εs2αforα>1and small enoughε>0.In this case P t is ultracontractive withP t 2→∞≤exp[c(1+t−(α+1)/(α−1))],t>0for some c>0.References[1]S.Aida,Uniformly positivity improving property,Sobolev inequalities and spectralgap,J.Funct.Anal.158(1998),152–185.[2]S.Aida,T.Masuda and I.Shigekawa,Logarithmic Sobolev inequalities and exponen-tial integrability,J.Funct.Anal.126(1994),83–101.[3]M.Arnaudon,A.Thalmaier,F.-Y.Wang,Harnack inequality and heat kernel esti-mates on manifolds with curvature unbounded below,Bull.Sci.Math.130(2006),no.3,223–233.[4]D.Bakry,D.and M.Emery,Hypercontractivit´e de semi-groupes de diffusion,C.R.Acad.Sci.Paris.S´e r.I Math.299(1984),775–778.[5]V.I.Bogachev,M.R¨o ckner and Feng-Yu Wang,Elliptic equations for invariant mea-sures onfinite and infinite dimensional manifolds,J.Math.Pures Appl.80:2(2001), 177–221.[6]J.M.Bismut,Large Deviations and the Malliavin Calculus,Boston:Birkh¨a user,MA,1984.[7]J.Cheeger,M.Gromov and M.Taylor,Finite propagation speed,Laplace operator,and geometry of complete Riemannian manifolds,J.Diff.Geom.17(1982),15–53.[8]Mu-Fa Chen and F.-Y.Wang,Application of coupling method to thefirst eigenvalueon manifold,Sci.Sin.(A),1994,37(1):1–14.[9]M.Cranston,Gradient estimates on manifolds using coupling,J.Funct.Anal.99(1991),110–124.[10]M.-F.Chen and F.-Y.Wang,Estimates of logarithmic Sobolev constant:an improve-ment of Bakry-Emery criterion,J.Funct.Anal.144(1997),287–300.[11]E.B.Davies and B.Simon,Ultracontractivity and heat kernel for Schr¨o dinger oper-ators and Dirichlet Laplacians,J.Funct.Anal.59(1984),335–395. [12]K.D.Elworthy and X.-M.Li,Formulae for the derivatives of heat semigroups,J.Funct.Anal.125(1994),252–286.[13]M.Emery,Stochastic calculus in manifolds,Springer-Verlag,Berlin,1989.With anappendix by P.-A.Meyer.[14]R.E.Greene and Hong-Xi Wu,Function Theory on Manifolds Which Possess a Pole,Lecture Notes in Math.699,Springer-Verlag,1979.[15]L.Gross,Logarithmic Sobolev inequalities,Amer.J.Math.97(1976),1061–1083.[16]E.P.Hsu,Logarithmic Sobolev inequalities on path spaces over Riemannian mani-folds,Comm.Math.Phys.189(1997),9–16.[17]W.S.Kendall,The radial part of Brownian motion on a manifold:a semimartingaleproperty,Ann.Probab.15(1987),no.4,1491–1500.[18]M.Ledoux,Concentration of measure and logarithmic Sobolev inequalities,S´e minairede Probabilit´e s,XXXIII,120–216,Lecture Notes Math.1709,Springer,Berlin,1999.[19]M.R¨o ckner and F.-Y.Wang,Harnack and functional inequalities for generalizedMehler semigroups,J.Funct.Anal.203(2003),237–261.[20]F.-Y.Wang,Logarithmic Sobolev inequalities on noncompact Riemannian manifolds,Probability Theory Relat.Fields109(1997),417–424.[21]F.-Y.Wang,Logarithmic Sobolev inequalities:conditions and counterexamples,J.Operator Theory46(2001),183–197.[22]F.-Y.Wang,Functional Inequalities,Markov Properties,and Spectral Theory,SciencePress,Beijing/New York,2005.。

无老师Toefl词汇红宝书正式版

无老师Toefl词汇红宝书正式版

无老师 Toefl 词汇红宝书—— 7天搞定托福单词内容说明:1本书完全免费放出,一共 1600左右个单词均为 100分必会单词!既然每个人在准备托福考试的时候都需要背单词,那么单词书就是一项基础性服务,基础性服务就应该免费!我们都需要空气,但是有人向我们收呼吸费么?电费和水费在欧洲很多国家也是不收的。

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为了提高新托福考试在这本单词书中的排位,本书在统计之前就已经将新托福的文章按照两次进行计算,保证考友们背的单词,是最鲜活的单词。

3这本《无老师 Toefl 词汇红宝书》在单词统计结束之后,由无老师亲自筛选, 将我们都很熟悉的单词比如说 apple 、 the 这样的单词全部去掉。

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4由于这本《无老师 Toefl 词汇红宝书》的单词,是按照从高到低的次序来进行排列的, 因此极大的满足了不同考友的个性化需要。

如果你需要考到 100分以上 , 那么你要把所有单词都背过,但是你如果仅需要考 80分,那么出现频率为 3次的单词你就可以不背,因为被考到的几率相对偏小。

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防止产生疲劳感。

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7单词书为了保证原汁原味,将单词在托福考试之中最常出现的形式作为默认显示方式列出, (括号之中的内容为单词的原型8托福考试要求最为贴近生活,国内考试的考试目的完全不同,因此国内考试会涉及到的很多意项,在托福考试当中不会考到。

Navier--Stokes

A fully parallel mortarfinite element projectionmethod for the solution of the unsteadyNavier–Stokes equationsA.BEN ABDALLAH and J.-L.GUERMONDAbstract.This paper describes the parallel implementationof a mortarfinite-element projection method to compute in-compressible viscousflows.The basic idea in the derivation ofthis method is that the appropriate functional setting for pro-jection methods must accommodate two different spaces forrepresenting the two velocityfields calculated in the viscousand incompressible half steps of the method.The velocity cal-culated in the viscous step is chosen in the space constrainedby the mortar elements;that is,a weak continuity through thesubdomain interfaces is enforced,whereas in the projectionstep,the weak continuity is relaxed.As a result,the projec-tion step is fully parallel.The numerical solutions of a seriesof test problems in two dimensions calculated by the pro-posed method compare quite satisfactorily with the referencesolutions.1INTRODUCTIONThe projection method of Chorin[4,5]and Temam[14](seealso[13]and[12])is the most frequently employed techniquefor the numerical solution of the primitive variable Navier–Stokes equations.This method is based on a peculiar time-discretization of the equations governing viscous incompress-ibleflows,in which the viscosity and the incompressibility ofthefluid are dealt within two separate steps.A functional analytical setting which properly accounts for thedifferent character of the equations of the two half-steps hasbeen proposed recently by Guermond[8,9]and Guermond-Quartapelle[10].The aim of this work is to describe the par-allel implementation of afinite-element projection methodwhich fully exploits the different mathematical structure ofthe two half-steps.The spatial discretization is based on amortarfinite-element approximation.In thefirst step,the vis-cous velocity is approximated by means of the mortarfinite element technique,whereas in the second step the constraint(3) In the sequel we assume that,are smooth solutions of the problem above and that at the initial time all the compatibility conditions implied by the required smoothness are satisfied. For instance,such conditions are satisfied if the initial datum is zero and the source term is regularized at.c1996A.Ben Abdallah and J.-L.Guermond ECCOMAS96.Published in1996by John Wiley&Sons,Ltd.2.2The spatial discretizationThe mortar element technique have been developed by Bernardi, Maday and Patera[1],[2].In this section we recall some as-pects of this technique and we formulate our time dependent Stokes problem within this discrete setting.We assume that we have at hand a partition of intonon-overlapping polygonals:and(4) For sake of simplicity we assume also that is two-dimensional, though the fractional step technique we develop is dimension independent.We restrict ourself to polygonal sub-domains. Furthermore,we assume that the decomposition of is ge-ometrically conformal;that is to say,the intersection of two subdomains is an edge,a vertex or empty.This hypothesis simplifies the implementation of the technique but is not a limitation of the mortar method.The interface between sub-domain and is denoted by.For each subdomain,we define a regular mixed tri-angulation(e.g.-iso-or see Girault-Raviart [6]or Brezzi[3]for other details).We denote by andthe linear spaces spanned by the velocity and the pressure triangulation of respectively.Note that we do not require the grids of each subdomains to match;the weak continu-ity through the subdomains’interfaces is enforced by mortar functions.We denote by the space of the mortar func-tions associated to the interface;for a clear definition of this space we refer to[1].The space of the mortar functions is defined by(5) For a function in we denote by the components of in.We now define,,the subspace of so that(6) where denotes the trace operator from onto .The space is equipped with the followingscalar product:(7) We also introduce the scalar product so that(8)We use this scalar product to define the dual norm of;the dual of equipped with the dual norm is hereafter denoted by.Finally,we define the projection onto.The pressure will be approximated in so that(9)is equipped with the scalar product(10) Let us also introduce the continuous bilinear formI R,so that for all in,(11) It can be shown that is coercive with respect to the norm of.(12) We associate with the linear continuous operatorso that,for all in,we have.We now introduce the continuous bilinear formI R so that(13) We associate with the continuous linear operatorand its transpose so that for every couple in we haveand.It can be shown that is onto;that is to say,there is a constant (independent of)so that(14) In the functional framework defined above,the spatially dis-cretized time-dependent Stokes problem can be reformulated as follows.For andfind and so that:The problem(15)can be shown to be well posed.We hereafter assume that the solution of this semi-discretized problem con-verges in the appropriate sense to that of(3);the convergence analysis is very classical.In the following we are interested only in approximating the time-dependent problem by means of a projection technique.3THE FRACTIONAL-STEPPROJECTION ALGORITHMS3.1The discrete settingIn order to uncouple the incompressibility constraint from the time evolution problem,we are led to introduce additional tools(see[8][9]for other details).We define thefinite dimensional linear space so that(1) We equip with the norm of and we denote this norm by.It is clear that is a subspaceof(in terms of linear space)and we denote by the continuous injection of into.Actually,is composed of the functions of which are weakly continuous across the subdomains’interfaces.We introduce another discrete version of the divergence op-erator;let be so that(2) The relation between and is brought to light by Proposition1is an extension of,and.A consequence of this proposition is that is also nec-essarily onto,for is onto.As a consequence,if we set ,we have a discrete counterpart of the classical decomposition:Corollary1We have the orthogonal decomposition:(3) 3.2The projection schemeWe introduce a partition of the time interval:for where,and define two series of approximate velocities and and one series of approximate pressures so that(5)The series is initialized by and assuming that the series is initialized by .Remark3.1.The problem(4)is well posed since is-elliptic.The problem(5)is also well posed thanks to corollary 1:indeed the couple is the decompo-sition of in;i.e.,where is the orthogonal projection of onto. Remark3.2.Note that since no weak continuity through the subdomains’interfaces is enforced on and,the projection problem(5)reduces to a series of completely independent problems that can be solved in parallel. Remark3.3.In practice the projected velocity is eliminated from the algorithm as follows(see[8]).Replace in(4)by its definition which is given by(5)at the-th time step;note that ,as already mentioned.In(5),is eliminated by applying to thefirst equation and by noting thatis an extension of.The algorithm which is implemented reads,for,(7) Remark3.4.Higher accuracy in time can be obtained if we replace the two-level backward Euler step offirst order by a backward three-level Euler step of second order as follows(9) Of course,the algorithm can be implemented in a more conve-nient form by eliminating the end-of-step velocity,as follows:(11) It can be shown that for afixed mesh size,this algorithm yields second order accuracy in time in the natural norms defined below.3.3Stability and convergence analysisThe projection algorithm introduced above is stable in the following sense:(12)Section Title3 A.Ben Abdallah and J.-L.Guermondwhere is a function of the data of the problem. The fact that the projection step is parallel is paid by the fact that the discrete gradient operator is not optimally stable; indeed if we denote by an interpolation operator on, we only haveof type(3) where is a mass matrix.This system is solved iteratively by means of a conjugate gradient preconditioned bywhere is the lumped mass matrix.4.2ImplementationThe code is written in FORTRAN90and uses the MPI message passing library.It is run on a CRAY-T3D which has128Dec Alpha processors.Each processor can deliverbut,still now,because of hardware imple-mentation(mutilated memory caches),hardly of the peak can be used.(recall that T3D is an ex-perimental machine,hopefully,these problems will be solved with the T3E).4.3Test problemsIn order to illustrate the second order algorithm described above,(10)-(11),we provide convergence tests on a test prob-lem.We consider the following exact solution on the square ,We have chosen linear functions in space to avoid spending much time on error calculation.The domain is divided into sixteen subdomains as shown infigure2.Fore sake of simplicity,we used structured grid on subdomains.We solve the time-dependent Stokes problem on the time interval with a source term corresponding to our chosen solution.Infigure3,we have reported the errors on the velocity in the norms and as functions of the time step for different global mesh sizes.As expected we observe a second order slope for moderate but we can see that the estimation constant seems to be dependent of in the rate of.This result is not surprising since we have proven convergence of order for thefirst order scheme(6)-(7);hence,convergence in time of orderfor(10)-(11)seems reasonable.(but has yet to be proven). The error on pressure in the norm of is re-ported as a function of infigure4.The same second order slope and mesh size dependency as that obtained on the ve-locity are observed on the pressure.To illustrate the mesh size influence on the convergence, we have reported infigure5the errors on both velocity and pressure as functions of while is kept equal to .We note a second order slope on the velocity in the norm.First order slope is obtained in thenorm(practically we obtained better than first order for the term in is still dominant).The same observations can be made for the pressure.δt10−310−210−1100101ErrorsonUSTOKES ProblemErrors on the velocity UFigure3.andversus.δt10−310−210−1100101ErrorsonpSTOKES ProblemErrors on the pressure pFigure4.versus.Section Title5 A.Ben Abdallah and J.-L.Guermondh10−310−210−110E r r o r sSTOKES Problem( δt = c h 3/2, c=0.8192 )Figure 5.,andversuswith.4.4Speed-UpThe numerical tests reported in this section were performedwith different numbers of processors for a global mesh size(nodes)and with .In table1,we can see for different numbersof processors the elapse time for one time step iteration,the mono-processor equivalent time ,the elapse time and the number of Conjugate Gradient iterations (resp.the time and the number of Preconditioned Conjugate Gradient iterations)for one prediction (resp.projection)step.At firstsight,we can notice that the algorithm has almost the right speed-up (from to we have a globalspeed-up of).But if we look at the projection step we notice better results;recall that this step amounts to solve a Poisson problem.If we look at the prediction step,where the communications between processors occur,the speed-up be-tween and (resp.and )is about(resp.).Actually,if we consider the speed-up for one CG iteration of the prediction step we obtain (resp.).There are two reasons for this.First,in the prediction step,the linear system is solved by means of a Conjugate Gradi-ent algorithm which is not preconditioned.As a result,the total number of iterations that is needed to reach convergence is dependent of both the problem size and (the conditionnumber ofdepends on ).The second reason is that the cost of one CG iteration is not of order but rather between and (we use sparse matrix techniques,see forinstance [7]).The efficiency rate has not been calculated since the problem is too big to be solved on one single processor ().Table 1.Time inventory for one time step iteration.166.198.4 4.2765 1.88932 3.2102.3 2.36820.838641.7111.51.35940.398[9]J.-L.Guermond,Sur l’approximation des e´quations de Navier–Stokes instationnaires par une me´thode de projection,C.R.Acad.Sc.Paris,Se´rie I,319,1994,887–892.[10]J.-L.Guermond and L.Quartapelle,On the approximation ofthe unsteady Navier–Stokes equations byfinite element projec-tion methods,LIMSI report95-14,submitted to Numer.Math.[11]O.Pironneau,Me´thode des´le´mentsfinis pour lesfluides,RMA7,Masson,1988.[12]L.Quartapelle,Numerical Solution of the IncompressibleNavier–Stokes Equations,ISNM113,Birkha¨user,Basel,1993.[13]R.Temam,Navier–Stokes Equations,Studies in Mathematicsand its Applications,2,North-Holland,1977.[14]R.Temam,Une me´thode d’approximation de la solution dese´quations de Navier–Stokes,Bull.Soc.Math.France,98,1968,115–152.Section Title7 A.Ben Abdallah and J.-L.Guermond。

信号完整性和电源完整性分析

An Integrated Signal and Power Integrity Analysis for Signal Traces Through the Parallel Planes Using Hybrid Finite-Element andFinite-Difference Time-Domain TechniquesWei-Da Guo,Guang-Hwa Shiue,Chien-Min Lin,Member,IEEE,and Ruey-Beei Wu,Senior Member,IEEEAbstract—This paper presents a numerical approach that com-bines the?nite-element time-domain(FETD)method and the?-nite-difference time-domain(FDTD)method to model and ana-lyze the two-dimensional electromagnetic problem concerned in the simultaneous switching noise(SSN)induced by adjacent signal traces through the coupled-via parallel-plate structures.Applying FETD for the region having the source excitation inside and FDTD for the remaining regions preserves the advantages of both FETD ?exibility and FDTD ef?ciency.By further including the transmis-sion-line simulation,the signal integrity and power integrity is-sues can be resolved at the same time.Furthermore,the numer-ical results demonstrate which kind of signal allocation between the planes can achieve the best noise cancellation.Finally,a com-parison with the measurement data validates the proposed hybrid techniques.Index Terms—Differential signaling,?nite-element and?nite-difference time-domain(FETD/FDTD)methods,power integrity (PI),signal integrity(SI),simultaneous switching noise(SSN), transient analysis.I.I NTRODUCTIONI N RECENT years,considerable attention has been devotedto time-domain numerical techniques to analyze the tran-sient responses of electromagnetic problems.The?nite-differ-ence time-domain(FDTD)method proposed by Yee in1966 [1]has become the most well-known technique becauseit pro-vides a lot of attractive advantages:direct and explicit time-marching scheme,high numerical accuracy with a second-order discretization error,stability condition,easy programming,and minimum computational complexity[2].However,it is often in-ef?cient and/or inaccurate to use only the FDTD method to dealManuscript received March3,2006;revised November6,2006.This work was supported in part by the National Science Council,Republic of China,under Grant NSC91-2213-E-002-109,by the Ministry of Education under Grant93B-40053,and by Taiwan Semiconductor Manufacturing Company under Grant 93-FS-B072.W.-D.Guo,G.-H.Shiue,and R.-B.Wu are with the Department of Electrical Engineering and Graduate Institute of Communication Engi-neering,National Taiwan University,10617Taipei,Taiwan,R.O.C.(e-mail: f92942062@.tw;d9*******@.tw;rbwu@.tw).C.-M.Lin is with the Packaging Core Competence Department,Advanced Assembly Division,Taiwan Semiconductor Manufacturing Company,Ltd., 30077Taiwan,R.O.C.(e-mail:chienmin_lin@).Color versions of one or more of the?gures in this paper are available online at .Digital Object Identi?er10.1109/TADVP.2007.901595with some speci?c structures.Hybrid techniques,which com-bine the desirable features of the FDTD and other numerical schemes,are therefore being developed to improve the simula-tion capability in solving many realistic problems.First,the FDTD(2,4)method with a second-order accuracy in time and a fourth-order accuracy in space was incorporated to tackle the subgridding scheme[3]and a modi?ed form was employed to characterize the electrically large structures with extremely low-phase error[4].Second,the integration with the time-domain method of moments was performed to analyze the complex geometries comprising the arbitrary thin-wire and inhomogeneous dielectric structures[5],[6].Third,the?exible ?nite-element time-domain(FETD)method was introduced locally for the simulation of structures with curved surfaces [6]–[8].With the advent of high-speed digital era,the simultaneous switching noise(SSN)on the dc power bus in the multilayer printed circuit boards(PCBs)causes paramount concern in the signal integrity and power integrity(SI/PI)along with the electromagnetic interference(EMI).One potential excitation mechanism of this high-frequency noise is from the signal traces which change layers through the via transition[9]–[11]. In the past,the transmission-line theory and the two-dimen-sional(2-D)FDTD method were combined successfully to deal with the parallel-plate structures having single-ended via transition[12],[13].Recently,the differential signaling has become a common wiring approach for high-speed digital system designs in bene?t of the higher noise immunity and EMI reduction.Nevertheless,for the real layout constraints,the common-mode currents may be generated from various imbal-ances in the circuits,such as the driver-phase skew,termination diversity,signal-path asymmetries,etc.Both the differential-and common-mode currents can in?uence the dc power bus, resulting in the SSN propagating within the planes.While applying the traditional method to manage this case,it will need a much?ner FDTD mesh to accurately distinguish the close signals transitioning through the planes.Such action not only causesthe unnecessary waste of computer memory but also takes more simulation time.In order to improve the computa-tional ef?ciency,this paperincorporates theFETD method to the small region with two or more signal transitions inside,while the other regions still remain with the coarser FDTD grids.While the telegrapher’sequations of coupled transmission lines are further introduced to the hybrid FETD/FDTD techniques,the1521-3323/$25.00?2007IEEEFig.1.A typical four-layer differential-via structure.SI/PI co-analysis for differential tracesthrough the planes can be accomplished as demonstrated in Section II and the numerical results are shown in Section III.For a group of signal vias,the proposed techniques can also tell which kind of signal alloca-tion to achieve the best performance as presented in Section III. Section IV thus correlates the measurement results and their comparisons,followed by brief conclusions in Section V.II.S IMULATION M ETHODOLOGYA typical differential-via structure in a four-layer board is il-lustrated in Fig.1.Along the signal-?ow path,the whole struc-ture is divided into three parts:the coupled traces,the cou-pled-via discontinuities,and the parallel plates.This section will present how the hybrid techniques integrate the three parts to proceed with the SI/PI co-simulation.At last,the stability consideration and computational complexity of the hybrid tech-niques are discussed as well.A.Circuit SolverWith reference to Fig.2,if the even/odd mode propagation coef?cients and characteristic impedances are given,it is recog-nized that the coupled traces can be modeled by the equivalent ladder circuits,and the lossy effects can be well approxi-mated with the average values of individual and over the frequency range of interest.The transient signal propagation is thus characterized by thetelegrapher’s equations with the cen-tral-difference discretization both in time and space domains. The approach to predict the signal propagation through the cou-pled-via discontinuities is similar to that through the coupled traces except for the difference of model-extracting method.To characterize the coupled-via discontinuities as depicted in Fig.1,the structure can be separatedinto three segments:the via between the two solid planes,and the via above(and under)the upper(and lower)plane.Since the time delay of signals through eachsegment is much less than the rising edge of signal,the cou-pled-via structure can be transformed into a SPICE passive net-work sketched in Fig.3by full-wave simulation[14],where represents the voltage of SSN induced by the current on Ls2. By linking the extracted circuit models of coupled-via disconti-nuities,both the top-and bottom-layer traces together with suit-able driving sources and load terminations,the transient wave-forms throughout the interconnects are then characterized and can be used for the SI analyses.Fig. 2.The k th element of equivalent circuit model of coupled transmission lines.Fig.3.Equivalent circuit model of coupled-via structures.B.Plane SolverAs for the parallel-plate structure,because the separation between two solid planes is much smaller than the equiva-lent wavelength of signals,the electromagnetic?eld inside is supposed to be uniform along the vertical direction.Thence, the2-D numerical technique can be applied to characterize the SSN effects while the FETD method is set for the small region covering the signal transitions and the FDTD scheme is constructed in the most regular regions.The FETD algorithm[15]starts from Maxwell’s two curl-equations and the vector equation is obtained byin(1)where and denote the electric?eld and current density,re-spectively,in the lossless volume.Applying the weak-form formulation or the Galerkin’s procedure to(1)gives(2) where is the weighting function that can be arbitrarily de-?ned.In use of the?nite-element method,the variational for-mula is thus discretized to implement the later numerical com-putation.In the present case,the linear basis function is chosen to express the?elds inside eachtriangular element.After taking the volume integration over each element and assembling theFig.4.FEM mesh in the source region and its interface with the FDTD grids.integrals from all the elements,(2)can be simpli?ed into a ma-trix form of(3) where and are the coef?cient vectors of electric?eld andcurrent density,respectively.In addition,the values of all matrix elements in(3)are formulated asand(4)For the mesh pro?le as illustrated in Fig.4,the FETD re-gion is chosen to be a block replacing the prime FDTD region into which the via transition penetrates.This is an initial value problem in time with the previous and being the initial conditions aswell as the boundary value problem in space with being Dirichlet boundary condition.To solve the initial value problem in(3),the time derivative of electric?eld is approximated by the central difference,that is(5) As for the electric?eld in the second term of(3),it can be for-mulated by the Newmark–Beta scheme[16]to be read as(6)Fig.5.Simulation?owchart of hybrid FETD and FDTD techniques to perform the SI/PI co-analysis for the coupled-via structure as illustrated in Fig.1.Moreover,in the triangular elements with the via transition inside,the term in(3)as expressed bygrid area(7)is needed to serve asthe excitation of the parallel-plate structure with the current shown in Fig.3through the via structure between Layers2and3.It is worth noting that the via transition should be placed on the bary-center of each triangular element to achieve better accuracy.The hand-over schemefor the?eld in the overlapped region of FDTD and FETD can be depicted in Fig.5.Given the boundary ?eld calculated by the FDTD algorithm atthe time step ,all the?eld in the FETD region can be acquired through the matrix solution of(3).The SSN voltage in Fig.3 is then determined by(8)where is the averaging value of nodal electric-?elds enclosing the via transition,and is the separation between the planes.Once and at the FETD mesh nodes(node 1,2,3,and4in Fig.4)become available,together with the ob-tained voltage/current values from the circuit solver andelectric/ magnetic?elds of the FDTD region,the hybrid time-marching scheme for the next time step can be implemented and so on.As a result of using the integrated schemes,the current, arisen from the input signal through the via structure,can have the ability to induce the voltage noise propagating within theFig. 6.Physical dimensions of coupled traces and via pair.(a)Top view (Unit=mil).(b)Side view.parallel plates.After a period of time,owing to the plane reso-nanceand return path,the induced noise will causethe unwanted voltage?uctuation on the coupled traces by the presence of the ?nite SSN voltage.C.Stability Problem and Computational ComplexityIt is not dif?cult to manifest that the FETD algorithm is un-conditionally stable.Substituting(5),(6),and(7)into(3)yields the following difference equation:(9) where(10) the superscript“1”denotes the matrix inverse and the factorgrid areaWithout loss of generality,the time-stepping scheme in(9)is restated as(11)Applying the-transform technique to(11)and solving for ,de?ned as the-transform of,the result reads(12)along with the dependent,de?ned as the-transform of in(11).Regardless of the time step,it can be easily de-duced that the poles of(12)is just on the unit circle of plane. This proves that the time marching by(9)is absolutely stable. The stability condition of these hybrid techniques is thus gov-erned by the transmission-line theory and the FDTD algorithm in the regular region,which are already known.Concerning the computational complexity,because of the consistence of simulation engines used for the circuit solver,parison of differential-mode S-parameters from HFSS simulation and the equivalent circuit as depicted in Fig.3.the only work is to compare the ef?ciency of the hybrid FETD/FDTD technique with that of the traditional FDTD method.In use of only the FDTD scheme for cell discretization, the grid size should be chosen at most the spacing between the adjacent via transitions.However,as depicted in Fig.4, the hybrid techniques adopting the FEM mesh for the source region exhibit the great talent to segment the whole plane with the coarser FDTD grids.Owing to the sparsity of the FETD matrices in(4)and the much smaller number of unknowns,the computational time needed for each FETD operation can be negligible.The complexity of the hybrid techniques is therefore dominated by the FDTD divisions in the regular region.It is ev-ident that the total simulation time of the2-D FDTD algorithm is,where denotes the number of the division in the whole space[7].The coarser the FDTD grids,the smaller the number of the grids and unknowns.Hence,the present hybrid techniques can preserve high accuracy without sacri?cing the computational ef?ciency.III.N UMERICAL R ESULTSA.Coupled via TransitionConsider the geometry in Fig.1but with the coupled-via structure being2cm away from the center of parallel plates, which is set as the origin of the–plane.The size of the plane is1010cm and the separation between the two metal planes is20mils(0.05cm).The physical dimensions of the coupled traces and via pair are depicted in Fig.6.After extracting the -parameters from the full-wave simulation,their equivalent circuit models of coupled-via structures as sketched in Fig.3 can be thus constructed.In Fig.7,it is found that the differen-tial-mode-parameters of equivalent circuit models are in good agreement with those from the HFSS simulations[14]and the extracted parasitic values of inductive and capacitive lumped-el-ements are also listed in the attached table.The top-layer coupled traces are driven by differential Gaussian pulses with the rise time of100ps and voltage ampli-tude of2V while the traces are terminated with the matchedFig.8.Simulated TDR waveforms on the positive-signaling trace.(a)Late-time response for the signal skew of10ps excluding the multire?ection phe-nomenon of common-mode signal.(b)Late-time response while no signal skew.TABLE IC OMPARISON OF C OMPUTATIONAL C OMPLEXITY B ETWEEN THE T WO M ETHODS(T IME D URATION=2:5ns)(CPU:Intel P43.0GHz,RAM:2GHz)loads at their ends.For simplicity,the transmission-line losses are not considered in the following analyses for the transient responses.By using the same mesh discretization as illustrated in Fig.4,the resultant segmentation for the plane con?nes the ?exible FEM mesh in the vicinity of via transitions and the coarser FDTD division with the size of22mm elsewhere. Employing the perfect magnetic conductors for boundary conditions of the parallel-plate structure,the simulated TDR waveforms with and without the signal skew on the posi-tive-signaling trace are presented in Fig.8.In comparison of hybrid FETD/FDTD techniques and?ner FDTD method with center-to-center via spacing(0.66mm)as the grid size,the simulation results are in good agreement.Note that the voltage ?uctuation before900ps is induced by the incident signal passing through the coupled-via structure while the occurrence of late-time response is accompanied by the parallel-plate resonances.As for the signal skew of10ps,the voltage level of late-time response is found to be greater than that of no signal skew because of the existence of common-mode currents produced by the timing skew of differential signals.Moreover,the simulation time of both methods should be pro-portional to the number of grids multiplied by the total time steps.As the physical time duration is?xed,the decreaseof the FDTD division size would correspond to the increase of the total Fig.9.Parallel plane with three current sources inside.(a)3-D view.(b)Zoom-in view of three sources on the plane in(a).(c).FETD/FDTD mesh discretization.Fig.10.Simulated noise waveforms at the preallocated probe in reference to Fig.9(a).time steps.Consequently,asshown in Table I,it is demonstrated that the computational ef?ciency of the hybrid techniques is in-deed much better than that of the?ner FDTD method.B.Multiple Source TransitionIn addition to a pair of differential-via structure,there can be a group of signaling vias distributed in the various regions of planes.Considering the parallel-plate structure in Fig.9(a), three current sources are distributed around the center(0,0) and a probe is located at(1mm,9mm)to detect the voltage noise induced on the planes.The FEM meshes for the source region and the interface with the FDTD region are shown inFig.11.Parallel-plate structure with two differential pairs of current sources inside in reference to Fig.9(a).(a)Two differential pairs of sources on the plane in Fig.9(a).(b)FETD/FDTD mesh discretization.parison of the simulated noise waveforms between three casesof differential-sources on the plane as in Fig.9(a).Fig.9(c).The current sources are Gaussian pulses with the rise time of100ps and different current amplitudes of0.5,0.25, and0.3A.With the same settings of boundary conditions,the simulated voltage noise waveforms at the preallocated probe re-ferred to Fig.9(a)are presented in Fig.10.It is indicated that the hybrid FETD/FDTD techniques still reservesthe great accuracyin predicting the traveling-wave behavior of plane noise.In the modern digital systems,many high-speed devices employ the multiple differential-traces for the purpose of data transmission.These traces are usually close to each other and may simultaneously penetrate the multilayered planes through via transitions.Hence,it is imperious for engineers to know how to realize the best power integrity by suitably arranging the positions of differential vias.Reconsidering the parallel plates in Fig.9(a),instead,two dif-ferential-current sources around the center and the probe is re-located at(25mm,25mm)as shown in Fig.11along with their corresponding mesh pro?le.After serving for the same Gaussian pulses as input signals,the simulated waveforms at Fig.13.At time of400ps,the overall electric-?eld patterns of three cases of differential-source settings in reference to Fig.12.(a)Case1:one pair of dif-ferential sources.(b)Case2:two pairs of differential sources with the same polarity.(c)Case3:two anti-polarity pairs of differential sources.the probe are presented in Fig.12while three cases of source settings are pared with the noise waveform of one pair of differential sources,the signal allocations of mul-tiple differential-sources diversely in?uencethe induced voltage noise.For the more detailed understanding,Fig.13displays the overall electric-?eld patterns at the time of400ps for three casesFig.14.Speci?cations and measurement settings of test board.(a)Top view.(b)Side view.parisons between the simulated and measured waveforms at both the TDR end and the probe as in Fig.14.(a)The TDR waveforms.(b)The waveforms at the probe.of differential-source settings on the plane.Note that the out-ward-traveling electric?eld of Case3(the differential-sources with antipolarity)is the smallest?uctuation since the appear-ance of two virtual grounds provided by the positive-and-nega-tive polarity alternates the signal allocation.IV.E XPERIMENTAL V ERIFICATIONIn order to verify the accuracy of hybrid techniques,a test board was fabricated and measured by TEK/CSA8000B time-domain re?ectometer.The designed test board comprises the single-ended and differential-via structures,connecting with the corresponding top-and bottom-layer traces.The design speci?-cations and measurement settings of test board are illustrated in Fig.14.To perform the time-domain simulation,the launching voltage sources are drawn out of re?ectometer.As the driving Fig.16.Frequency-domain magnitude of the probing waveforms corre-sponding to Fig.15(b)and the plane resonances.signals pass through the differential vias,the parallel-plate structure is excited,incurring the SSN within the ter, the quiet trace will suffer form this voltage noise through the single-ended via transition.After extracting the equivalent circuit models of coupled-via structures and well dividing the parallel plates,the SI/PI co-analysis for test board can be achieved.Simulation results are compared with the measure-ment data as shown in Fig.15accordingly.As observed in Fig.15(a),the differential signals have the in-ternal skew of about30ps and the bulgy noise arising at about 500ps is due to the series-wound connector usedin the measure-ment.The capacitive effect of via discontinuities is occurred at about900ps,while the deviations between the simulation and measurement are attributed to the excessive high-frequency loss of input signals.For the zoom-in view of probing waveforms as in Fig.15(b),it is displayed that the comparison is still in good agreement except for the lossy effect not included in the time-domain simulation.Applying the fast Fourier transform, the frequency-domain magnitude of probing waveforms is ob-tained in Fig.16.In addition to the similar trend of time-domain simulation and measurement results,the peak frequencies cor-respond to the parallel-plate resonances of test board exactly. Hence,the exactitude of the proposed hybrid techniques can be veri?ed.V.C ONCLUSIONA hybrid time-domain technique has been introduced and applied successfully to perform the SI/PI co-analysis for the differential-via transitions in the multilayer PCBs.The signalpropagation on the differential traces is characterized by the known telegrapher’s equations and the parallel-plate structure is discretized by the combined FETD/FDTD mesh schemes.The coarser FDTD segmentation for most of regular regions inter-faces with an unconditionally stable FETD mesh for the local region having the differential-via transitions inside.In use of hybrid techniques,the computational time and memory requirement are therefore far less than those of a traditional FDTD space with the?ner mesh resolution but preserve the same degrees of numerical accuracy throughout the simulation.In face of the assemblages of multiple signal transitions in the speci?c areas,the hybrid techniques still can be adopted by slightly modifying the mesh pro?les in the local FETD re-gions.Furthermore,the numerical results demonstrate that the best signal allocation for PI consideration is positive-and-nega-tive alternate.Once the boundary conditions between the FETD and FDTD regions are well de?ned,it is expected that the hy-brid techniques have a great ability to deal with the more real-istic problems of high-speed interconnect designs concerned in the signal traces touted through the multilayer structures.R EFERENCES[1]K.S.Yee,“Numerical solution of initial boundary value problemsinvolving Maxwell’s equations in isotropic media,”IEEE Trans.Antennas Propag.,vol.AP-14,no.3,pp.302–307,May1966.[2]K.S.Kunz and R.J.Luebbers,The Finite Difference Time DomainMethod for Electromagnetics.Boca Raton,FL:CRC,1993,ch.2,3.[3]S.V.Georgakopoulos,R.A.Renaut,C.A.Balanis,and C.R.Birtcher,“A hybrid fourth-order FDTD utilizing a second-order FDTD subgrid,”IEEE Microw.Wireless Compon.Lett.,vol.11,no.11,pp.462–464,Nov.2001.[4]M. F.Hadi and M.Piket-May,“A modi?ed FDTD(2,4)scheme formodeling electrically large structures with high-phase accuracy,”IEEETrans.Antennas Propag.,vol.45,no.2,pp.254–264,Feb.1997.[5] A.R.Bretones,R.Mittra,and R.G.Martin,“A hybrid technique com-bining the method of moments in the time domain and FDTD,”IEEEMicrow.Guided Wave Lett.,vol.8,no.8,pp.281–283,Aug.1998.[6] A.Monorchio, A.R.Bretones,R.Mittra,G.Manara,and R.G.Martin,“A hybrid time-domain technique that combines the?nite element,?-nite difference and method of moment techniques to solve complexelectromagnetic problems,”IEEE Trans.Antennas Propag.,vol.52,no.10,pp.2666–2674,Oct.2004.[7]R.-B.Wu and T.Itoh,“Hybrid?nite-difference time-domain modelingof curved surfaces using tetrahedral edge elements,”IEEE Trans.An-tennas Propag.,vol.45,no.8,pp.1302–1309,Aug.1997.[8] D.Koh,H.-B.Lee,and T.Itoh,“A hybrid full-wave analysis of via-hole grounds using?nite-difference and?nite-element time-domainmethods,”IEEE Trans.Microw.Theory Tech.,vol.45,no.12,pt.2,pp.2217–2223,Dec.1997.[9]S.Chun,J.Choi,S.Dalmia,W.Kim,and M.Swaminathan,“Capturingvia effects in simultaneous switching noise simulation,”in Proc.IEEEpat.,Aug.2001,vol.2,pp.1221–1226.[10]J.-N.Hwang and T.-L.Wu,“Coupling of the ground bounce noise tothe signal trace with via transition in partitioned power bus of PCB,”in Proc.IEEE pat.,Aug.2002,vol.2,pp.733–736.[11]J.Park,H.Kim,J.S.Pak,Y.Jeong,S.Baek,J.Kim,J.J.Lee,andJ.J.Lee,“Noise coupling to signal trace and via from power/groundsimultaneous switching noise in high speed double data rates memorymodule,”in Proc.IEEE pat.,Aug.2004,vol.2,pp.592–597.[12]S.-M.Lin and R.-B.Wu,“Composite effects of re?ections and groundbounce for signal vias in multi-layer environment,”in Proc.IEEE Mi-crowave Conf.APMC,Dec.2001,vol.3,pp.1127–1130.[13]“Simulation Package for Electrical Evaluation and Design(SpeedXP)”Sigrity Inc.,Santa Clara,CA[Online].Available:[14]“High Frequency Structure Simulator”ver.9.1,Ansoft Co.,Pittsburgh,PA[Online].Available:[15]J.Jin,The Finite Element Method in Electromagnetics.New York:Wiley,1993,ch.12.[16]N.M.Newmark,“A method of computation for structural dynamics,”J.Eng.Mech.Div.,ASCE,vol.85,pp.67–94,Jul.1959.Wei-Da Guo was born in Taoyuan,Taiwan,R.O.C.,on September25,1981.He received the B.S.degreein communication engineering from Chiao-TungUniversity,Hsinchu,Taiwan,R.O.C.,in2003,andis currently working toward the Ph.D.degree incommunication engineering at National TaiwanUniversity,Taipei,Taiwan,R.O.C.His research topics include computational electro-magnetics,SI/PI issues in the design of high-speeddigital systems.Guang-Hwa Shiue was born in Tainan,Taiwan,R.O.C.,in1969.He received the B.S.and M.S.de-grees in electrical engineering from National TaiwanUniversity of Science and Technology,Taipei,Taiwan,R.O.C.,in1995and1997,respectively,and the Ph.D.degree in communication engineeringfrom National Taiwan University,Taipei,in2006.He is a Teacher in the Electronics Depart-ment of Jin-Wen Institute of Technology,Taipei,Taiwan.His areas of interest include numericaltechniques in electromagnetics,microwave planar circuits,signal/power integrity(SI/PI)and electromagnetic interference (EMI)for high-speed digital systems,and electrical characterization of system-in-package.Chien-Min Lin(M’92)received the B.S.degreein physics from National Tsing Hua University,Hsinchu,Taiwan,R.O.C.,the M.S.degree in elec-trical engineering from National Taiwan University,Taipei,Taiwan,R.O.C.,and the Ph.D.degree inelectrical engineering from the University of Wash-ington,Seattle.He was with IBM,where he worked on the xSeriesserver development and Intel,where he worked onadvanced platform design.In January2004,he joinedTaiwan Semiconductor Manufacturing Company, Ltd.,Taiwan,as a Technical Manager in packaging design and assembly vali-dation.He has been working on computational electromagnetics for the designs of microwave device and rough surface scattering,signal integrity analysis for high-speed interconnect,and electrical characterization of system-in-package.Ruey-Beei Wu(M’91–SM’97)received the B.S.E.E.and Ph.D.degrees from National Taiwan Univer-sity,Taipei,Taiwan,R.O.C.,in1979and1985,respectively.In1982,he joined the faculty of the Departmentof Electrical Engineering,National Taiwan Univer-sity,where he is currently a Professor and the De-partment Chair.He is also with the Graduate Instituteof Communications Engineering established in1997.From March1986to February1987,he was a Vis-iting Scholar at the IBM East Fishkill Facility,NY. From August1994to July1995,he was with the Electrical Engineering Depart-ment,University of California at Los Angeles.He was also appointed Director of the National Center for High-Performance Computing(1998–2000)and has served as Director of Planning and Evaluation Division since November2002, both under the National Science Council.His areas of interest include computa-tional electromagnetics,microwave and millimeter-wave planar circuits,trans-mission line and waveguide discontinuities,and interconnection modeling for computer packaging.。

(整理)汽车安全气囊碰撞有限元分析外文翻译

FINITE ELEMENT ANALYSIS OF AUTOMOBILE CRASH SENSORS FOR AIRBAG SYSTEMSABSTRACTAutomobile spring bias crash sensor design time can be significantly reduced by using finite element analysis as a predictive engineering tool.The sensors consist of a ball and springs cased in a plastic housing.Two important factors in the design of crash sensors are the force-displacement response of the sensor and stresses in the sensor springs. In the past,sensors were designed by building and testing prototype hardware until the force-displacement requirements were met. Prototype springs need to be designed well below the elastic limit of the ing finite element analysis, sensors can be designed to meet forcedisplacement requirements with acceptable stress levels. The analysis procedure discussed in this paper has demonstrated the ability to eliminate months of prototyping effort.MSC/ABAQUS has been used to analyze and design airbag crash sensors.The analysis was geometrically nonlinear due to the large deflections of the springs and the contact between the ball and springs. Bezier 3-D rigid surface elements along with rigid surface interface (IRS) elements were used to model ball-to-springcontact.Slideline elements were used with parallel slideline interface (ISL) elements for spring-to-spring contact.Finite element analysis results for the force-displacement response of the sensor were in excellent agreement with experimental results.INTRODUCTIONAn important component of an automotive airbag system is the crash sensor. Various types of crash sensors are used in airbag systems including mechanical,electro-mechanical, and electronic sensors. An electro-mechanical sensor (see Figure 1) consisting of a ball and two springs cased in a plastic housing is discussed in thispaper. When the sensor experiences a severe crash pulse, the ball pushes two springs into contact completing the electric circuit allowing the airbag to fire. Theforce-displacement response of the two springs is critical in designing the sensor to meet various acceleration input requirements. Stresses in the sensor springs must be kept below the yield strength of the spring material to prevent plastic deformation in the springs. Finite element analysis can be used as a predictive engineering tool to optimize the springs for the desired force-displacement response while keeping stresses in the springs at acceptable levels.In the past, sensors were designed by building and testing prototype hardware until the forcedisplacement requirements were met. Using finite element analysis, the number of prototypes built and tested can be significantly reduced, ideally to one, which substantially reduces the time required to design a sensor. The analysis procedure discussed in this paper has demonstrated the ability to eliminate months of prototyping effort.MSC/ABAQUS [1] has been used to analyze and design airbag crash sensors. The analysis was geometrically nonlinear due to the large deflections of the springs and the contact between the ball and springs. Various contact elements were used in this analysis including rigid surface interface (IRS) elements, Bezier 3-D rigid surface elements, parallel slide line interface (ISL) elements, and slide line elements. The finite element analysis results were in excellent agreement with experimental results for various electro-mechanical sensors studied in this paper.PROBLEM DEFINITIONThe key components of the electro-mechanical sensor analyzed are two thin metallic springs (referred to as spring1 and spring2) which are cantilevered from a rigid plastic housing and a solid metallic ball as shown in Figure 1. The plastic housing contains a hollow tube closed at one end which guides the ball in the desired direction. The ball is held in place by spring1 at the open end of the tube. When the sensor is assembled, spring1 is initially displaced by the ball which creates a preload on spring1. The ball is able to travel in one direction only in this sensor and this direction will be referredto as the x-direction (see the global coordinate system shown in Figure 2) in this paper. Once enough acceleration in the x-direction is applied to overcome the preload on spring1, the ball displaces the spring. As the acceleration applied continues to increase, spring1 is displaced until it is in contact with spring2. Oncethe sensor to perform its function within the airbag system.FINITE ELEMENT ANALYSIS METHODOLOGYWhen creating a finite element representation of the sensor, the following simplifications can be made. The two springs can be fully restrained at their bases implying a perfectly rigid plastic housing. This is a good assumption when comparing the flexibility of the thin springs to the stiff plastic housing. The ball can be represented by a rigid surface since it too is very stiff as compared to the springs. Rather than modeling the contact between the plastic housing and the ball, all rotations and translations are fully restrained except for the xdirection on the rigidsurface representing the ball. These restraints imply that the housingwill have no significant deformation due to contact with the ball. These restraints also ignore any gaps due to tolerances between the ball and the housing. The effect of friction between the ball and plastic is negligible in this analysis.The sensor can be analyzed by applying an enforced displacement in the x-direction to the rigid surface representing the ball to simulate the full displacement of the ball. Contact between the ball and springs is modeled with various contact elements as discussed in the following section. A nonlinear static analysis is sufficient to capture the force-displacement response of the sensor versus using a more expensive and time consuming nonlinear transient analysis. Although the sensor is designed with a ball mass and spring stiffness that gives the desired response to a given acceleration, thereis no mass associated with the ball in this static analysis. The mass of the ball can be determined by dividing the force required to deflect the springs by the acceleration input into the sensor.MeshThe finite element mesh for the sensor was constructed using MSC/PATRAN [2]. The solver used to analyze the sensor was MSC/ABAQUS. The finite element mesh including the contact elements is shown in Figure 2. The plastic housing was assumed to be rigid in this analysis and was not modeled. Both springs were modeled with linear quadrilateral shell elements with thin shell physical properties. The ball was assumed to be rigid and was modeled with linear triangular shell elements with Bezier 3-D rigid surface properties.To model contact between the ball and spring1, rigid surface interface (IRS) elements were used in conjunction with the Bezier 3-D rigid surface elements making up the ball. Linear quadrilateral shell elements with IRS physical properties were placed on spring1 and had coincident nodes with the quadrilateral shell elements making up spring1. The IRS elements were used only in the region of ball contact.To model contact between spring1 and spring2, parallel slide line interface (ISL) elements were used in conjunction with slide line elements. Linear bar elements with ISL physical properties were placed on spring1 and had coincident nodes with the shell elements on spring1. Linear bar elements with slide line physical properties were placed on spring2 and had coincident nodes with the shell elements making up spring2.MaterialBoth spring1 and spring2 were thin metallic springs modeled with a linear elastic material model. No material properties were required for the contact or rigid surface elements.Boundary ConditionsBoth springs were assumed to be fully restrained at their base to simulate a rigid plastichousing. An enforced displacement in the x-direction was applied to the ball. The ball wasfully restrained in all rotational and translational directions with the exception of the xdirection translation. Boundary conditions for the springs and ball are shown in Figure 2.DISCUSSIONTypical results of interest for an electro-mechanical sensor would be the deflected shape of the springs, the force-displacement response of the sensor, and the stress levels in the springs. Results from an analysis of the electro-mechanical sensor shown in Figure 2 will be used asfull ball travel. Looking at the deflected shape of the springs can provide insight into the performance of the sensor as well as aid in the design of the sensor housing.Stresses in the springs are important results in this analysis to ensure stress levels in the springs are at acceptable levels. Desired components of stress can be examined through various means including color contour plots. One of the most important results from the analysis is the force-displacement response for the sensor shown in Figure 4. From this force-displacement response, the force required to push spring1 into contact with spring2 can readily be determined. This force requirement can be used with a given acceleration to determine the mass required for the ball. Based on these results, one or more variations of several variables such as spring width, spring thickness, ball diameter, and ball material can be updated until the force-displacement requirements are achieved within a desired accuracy.A prototype of the sensor shown in Figure 2 was constructed and tested to determine its actual force-displacement response. Figure 4 shows the MSC/ABAQUS results along with the experimental results for the force-displacement response of the sensor. There was an excellent correlation between finite element and experimental results for this sensor as well asfor several other sensors examined. Table 1 shows the difference in percent between finite element and experimental results including force at preload on spring1, force at spring1-tospring2 contact, and force at full ball travel for two sensor configurations. Sensor A in Table 1 is shown in Figure 1. Sensor B in Table 1 is based on the sensor shown in Figure 2.The sensor model analyzed in this paper was also analyzed with parabolic quadrilateral and bar elements to ensure convergence of the solution.Force-displacement results converged to less than 1% using linear elements. The stresses in the springs for this sensor converged to within 10% for the linear elements. The parabolic elements increased solve time by more than an order of magnitude over the linear elements. With more complex spring shapes, a denser linear mesh or parabolic elements used locally in areas of stress concentrations would be necessary to obtain more accurate stresses in the springs.Notes: 1. Sensor A results are based on 1 prototype manufactured and tested. Sensor Bexperimental results are based on the average of 20 prototypesmanufacturedand tested.2. No experimental data for force at full ball travel for Sensor A.3. %Difference=(FEA Result - Experimental Result)/Experimental ResultCONCLUSIONSMSC/ABAQUS has been used to analyze and design airbag crash sensors. The finite element analysis results were in excellent agreement with experimental results for several electromechanical sensors for which prototypes were built and tested. Using finite element analysis, sensors can be designed to meet force-displacement requirements with acceptable stress levels. The analysis procedure discussed in this paper has demonstrated the ability to eliminate months of prototyping effort. This paper has demonstrated the power of finite element analysis as a predictive engineering tool even with the use of multiple contact element types.汽车安全气囊系统撞击传感器的有限单元分析摘要:汽车弹簧碰撞传感器可以利用有限单元分析软件进行设计,这样可以大大减少设计时间。

有限元仿真的英语

有限元仿真的英语Finite Element SimulationThe field of engineering has seen a remarkable evolution in recent decades, with the advent of advanced computational tools and techniques that have revolutionized the way we approach design, analysis, and problem-solving. One such powerful tool is the finite element method (FEM), a numerical technique that has become an indispensable part of the modern engineer's toolkit.The finite element method is a powerful computational tool that allows for the simulation and analysis of complex physical systems, ranging from structural mechanics and fluid dynamics to heat transfer and electromagnetic phenomena. At its core, the finite element method involves discretizing a continuous domain into a finite number of smaller, interconnected elements, each with its own set of properties and governing equations. By solving these equations numerically, the finite element method can provide detailed insights into the behavior of the system, enabling engineers to make informed decisions and optimize their designs.One of the key advantages of the finite element method is its abilityto handle complex geometries and boundary conditions. Traditional analytical methods often struggle with intricate shapes and boundary conditions, but the finite element method can easily accommodate these complexities by breaking down the domain into smaller, manageable elements. This flexibility allows engineers to model real-world systems with a high degree of accuracy, leading to more reliable and efficient designs.Another important aspect of the finite element method is its versatility. The technique can be applied to a wide range of engineering disciplines, from structural analysis and fluid dynamics to heat transfer and electromagnetic field simulations. This versatility has made the finite element method an indispensable tool in the arsenal of modern engineers, allowing them to tackle a diverse array of problems with a single computational framework.The power of the finite element method lies in its ability to provide detailed, quantitative insights into the behavior of complex systems. By discretizing the domain and solving the governing equations numerically, the finite element method can generate comprehensive data on stresses, strains, temperatures, fluid flow patterns, and other critical parameters. This information is invaluable for engineers, as it allows them to identify potential failure points, optimize designs, and make informed decisions that lead to more reliable and efficient products.The implementation of the finite element method, however, is not without its challenges. The process of discretizing the domain, selecting appropriate element types, and defining boundary conditions can be complex and time-consuming. Additionally, the accuracy of the finite element analysis is heavily dependent on the quality of the input data, the selection of appropriate material models, and the proper interpretation of the results.To address these challenges, researchers and software developers have invested significant effort in improving the finite element method and developing user-friendly software tools. Modern finite element analysis (FEA) software packages, such as ANSYS, ABAQUS, and COMSOL, provide intuitive graphical user interfaces, advanced meshing algorithms, and powerful post-processing capabilities, making the finite element method more accessible to engineers of all levels of expertise.Furthermore, the ongoing advancements in computational power and parallel processing have enabled the finite element method to tackle increasingly complex problems, pushing the boundaries of what was previously possible. High-performance computing (HPC) clusters and cloud-based computing resources have made it possible to perform large-scale, multi-physics simulations, allowing engineers to gain deeper insights into the behavior of their designs.As the engineering field continues to evolve, the finite element method is poised to play an even more pivotal role in the design, analysis, and optimization of complex systems. With its ability to handle a wide range of physical phenomena, the finite element method has become an indispensable tool in the modern engineer's toolkit, enabling them to push the boundaries of innovation and create products that are more reliable, efficient, and sustainable.In conclusion, the finite element method is a powerful computational tool that has transformed the field of engineering. By discretizing complex domains and solving the governing equations numerically, the finite element method provides engineers with detailed insights into the behavior of their designs, allowing them to make informed decisions and optimize their products. As the field of engineering continues to evolve, the finite element method will undoubtedly remain a crucial component of the modern engineer's arsenal, driving innovation and shaping the future of technological advancement.。

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First Parallel Results for a Finite-Element MHD Codeon the T3D and T3EAlice E. Koniges, X. Xu, and P. Covello, Lawrence Livermore National Laboratory,Livermore, CA 94550Steve Plimpton, Sandia National Laboratory, MS 1111 Albuquerque, NM 87185-1111and the NIMROD TEAMkoniges@ABSTRACT:NIMROD is a finite-element based magnetic fusion energy code. The code achieves parallelism by spatially decomposing the problem into an unstructured collection of structured blocks. The algorithm yields excellent scaling on both the T3D and T3E with the latter yielding a performance improvement factor of approximately 4. KEYWORDS: Applications, finite-element, T3D, T3E, MHDIntroductionNIMROD is a finite-element based magnetohydrodynamic (MHD) fusion energy code. The code is being developed by a team of scientists who are physically located at several different laboratories. Information on the team and the team process is contained in the NIMROD web pages . The focus of parallelization of the NIMROD code is based on the computationally intensive physics kernel. This kernel is written so as to run without modification on single processors or any platform that supports a MPI message-passing style of programming. This includes workstations, traditional vector supercomputers, and essentially all current-generation massively parallel machines. In this paper, we describe how the NIMROD kernel is structured to enable efficient parallelization. We present timings on several parallel machines including the T3D at LLNL, T3E's at NERSC and UT Austin, and the C90 at NERSC.Parallel DecompositionNIMROD represents the poloidal simulation plane as a collection of adjoining grid blocks; the toroidal discretization is pseudo-spectral. Within a single poloidal block the grid is topologically regular to enable the usual 2-D stencil operations to be performed efficiently. Blocks join each other in such a way that individual grid lines are continuous across block boundaries. Within these constraints, quite general geometries can be gridded, and parallelization is achieved by assigning one or more blocks (with their associated toroidal modes) to each processor. In parallel, the only interprocessor communication that is then required is to exchange values for block-edge or block-corner grid points shared by other processors. For general block connectivity, this operation requires irregular, unstructured interprocessor communication. We pre-compute the communication pattern and then exchange values asynchronously. This enables the block-connection operation to execute efficiently and scalably on any number of processors. NIMROD uses implicit time stepping to model long-timescale events and thus requires a robust iterative solver. To date, an explicit time-stepping routine and an iterative solver using conjugate gradient techniques have been implemented and tested in parallel for NIMROD. The iterative method uses simple diagonal (Jacobi) scaling as a matrix preconditioner. A second method (currently under parallel development) directly inverts the portion of the matrix residing on each block as a preconditioning step. Both iterative solvers perform their computations on ablock-wise basis and thus work in parallel using the block-connection formalism described above. We present timings that illustrate the performance and convergence of both techniques as a function of (1) the number of blocks used to grid the poloidal plane and (2) the number of processors used.Figure 1 shows the NIMROD Code system.The NIMROD Physics KernelThe Nimrod physics kernel is based on solving the nonlinear, two-fluid dynamical equations for electrons and ions simultaneosly with Maxwell's equations. For this approximation, we assume that the ions and electrons have Maxwellian distribution functions and can thus be described as interacting fluids. This approach misses purely kinetic effects such as those related to Landau damping and finite Larmor radius, but includes all the cold plasma wave branches such as Langmuir oscillations, cyclotron, hybrid, and whistler waves, as well as low frequency Alfvén and sound waves[1]. Collisionless, as well as resistive, reconnection is also described by this model. The NIMROD code is presently being developed to solve the equations of such a model in three-dimensional toroidal geomery and time.Spatial DiscretizationSpatial discretization in the poloidal plane is accomplished with finite elements and a non-orthogonal Eulerian grid. The toroidal coordinate is treated with a dealiased, pseudospectral representation and Fast Fourier transforms (FFTs). The non-orthogonal poloidal grid consists primarily of unstructured blocks of structured quadrilaterals (RBLOCKs). In the poloidal plane using the RBLOCK representation, the dependent variables are approximated with bi-linear elements, and metric elements are treated as bi-cubic splines. In the core of the plasma the grid is chosen to be closely aligned with the initial axisymmetric (n = 0) flux surfaces. (Occasional regridding may be required as the axisymmetric component evolves.) Non-conforming RBLOCKs can be joined with blocks of unstructured triangular elements (TBLOCKs). A TBLOCK is also introduced to represent the region around the magnetic axis, thus avoiding the coordinate singularity inherent in pure flux coordinates. The initial choice to avoid the singularity while avoiding bottle necks in the parallel decomposition was to overlay a patch of RBLOCKS at the axis. This is shown in Figure 3. This led to numerical inaccuracies, however, and is being replaced by a pie-shaped collection of triangle elements, a TBLOCK, as shown in Figure 4.Figure 3 shows initial rectangular patch.Figure 4 shows latest version with pie-shaped collection of triangular elements at the magnetic axis. Extensive numerical analysis of the spatial and temporal discretization described here has shown that this formulation is free of spectral pollution and the point-to-point "red-black" mode. Details of this analysis are given in Ref. 2. Parallel PerformanceNIMROD has been designed from the beginning to be used on state-of-the-art massively parallel computing platforms. This is significantly different from many other application codes which were ported to the MPP after years of use on a serial (often with vector processors) machine. Collections of RBLOCK or TBLOCK elements can be assigned to different CPUs. Communication between blocks is required primarily for the matrix multiply and the dot product phases of the CG solver. The pre-conditioner for the CG solver uses diagonal scaling on each RBLOCK or TBLOCK. Plans are underway to introduce more sophisticated preconditioning methods for nonlinear problems. Nearly ideal performance scalings with increases in problem size and number of CPUs have been obtained on both the T3D andT3E computers. More details of these scalings are given in the viewgraph pages. A comparison of T3D/E performance with the Cray C90 is given in Figures 5 and 6.In all cases shown here, the code has not been optimized for a given machine. Optimization for the MPP machines will be performed after a majority of the non-linear physics effects are included. Reference 4 describes some general procedures for optimization on T3D/E-like architectures. The final figures give a scaled speed-up comparison of the T3D and the T3E.Here, scaled speed-up is speedup divided by problem size. We find that the T3E is roughly a factor of 4 faster which is identical to the performance improvement predicted by the specifications of the T3E which has a faster processor and allows for chaining of operations. The larger cache on the T3E may also contribute to the performance improvement. Scalability is virtually linear for both machines. Additional details can be found in the viewgraphs for the oral version of this presentation.AcknowledgmentsWork at LLNL for DOE under Contract W7405-ENG-48.The DoE MICS Office supported SNL work on solvers and parallelization for the NIMROD project.Computer time provided by NERSC, LLNL, and Univ. Texas, Austin.References1. D. Schnack, et al., An Overview of the NIMROD Code, Proc. International Workshop on Nonlinear and Extended MHD, Madison WI, April 30-May 2, 1997.3. A. H. Glasser, et al., "Numerical Analysis of the NIMROD Formulation", Proc. International Workshop on Nonlinear and Extended MHD, Madison WI, April 30-May 2, 1997.4. A. E. Koniges and K.R. Lind, "Parallelizing Code for Real Applications on the T3D", Computers in Physics 9, 39 (1995). Author BiographyAlice Koniges is Leader of Multiprogrammatic and Institutional Computing Research at the Lawrence Livermore National Laboratory in Livermore, Ca.Lawrence Livermore National LaboratoryFor information about this page, please contact Alice Koniges, koniges@.DisclaimersLast modified May 22, 1997.UCRL-MI-127382Table of Contents | Author Index | CUG Home Page | Home。

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