Optimization of composite pressure vessels with metal liner by adaptive response surface method
层状双金属氢氧化物
包装工程第44卷第19期·104·PACKAGING ENGINEERING2023年10月层状双金属氢氧化物/聚乙烯醇气体阻隔薄膜材料制备及性能研究张子怡，李梦冉，薛程，范婷婷，李欢欢，李中波*（安徽农业大学轻纺工程与艺术学院，安徽合肥230036）摘要：目的研发出一种具有优异氧气阻隔性能的柔性薄膜，其在食品包装领域具有良好的应用前景。
方法以具有生物降解性能的聚乙烯醇（PVA）为成膜基材，镁铝层状双金属氢氧化物（MgAl-LDH）为改性剂，柠檬酸为交联剂，采用流延法制备出具有优异气体阻隔性能的PVA/MgAl-LDH复合薄膜。
结果随着柠檬酸的含量的增加，复合薄膜的亲水性能逐渐增加，阻隔性能逐渐下降；随着复合薄膜中MgAl-LDH的含量的增加，复合薄膜的疏水性能和阻隔性能逐渐提高。
当复合薄膜中MgAl-LDH的质量分数为1.5%时，薄膜的力学性能最好，抗拉强度为42 MPa，断裂伸长率为16.7%，此MgAl-LDH质量分数下薄膜的气体阻隔性能也最优异，气体透过量为16 mL/(m2·24 h·0.1 MPa)。
结论柠檬酸的引入增加了薄膜内部亲水基团的数量，提升了复合薄膜的亲水性能。
MgAl-LDH可以减少PVA薄膜内部自由体积，提升PVA薄膜的力学性能和阻隔性能。
关键词：聚乙烯醇；镁铝层状双金属氢氧化物；柠檬酸；复合薄膜；阻隔性能中图分类号：TS206.4 文献标识码：A 文章编号：1001-3563(2023)19-0104-08DOI：10.19554/ki.1001-3563.2023.19.014Preparation and Properties of PVA/MgAl-LDH Gas Barrier FilmsZHANG Zi-yi, LI Meng-ran, XUE Cheng, FAN Ting-ting, LI Huan-huan, LI Zhong-bo*(College of Light Textile Engineering and Art, Anhui Agricultural University, Hefei 230036, China)ABSTRACT: The work aims to develop a flexible film with excellent oxygen barrier performance and good application prospects in the field of food packaging. The PVA/MgAl-LDH composite film with excellent gas barrier performance was prepared by the casting method with biodegradable polyvinyl alcohol (PVA) as the film-forming substrate, mag-nesium-aluminum layered bimetallic hydroxide (MgAl-LDH) as the modifier, and citric acid as the cross-linking agent.The experimental results showed that with the increase of citric acid content, the hydrophilic property of the composite film gradually increased and the barrier performance decreased gradually. With the increase of MgAl-LDH content in the composite film, the hydrophobic property and barrier property of the composite film gradually increased. When the content of MgAl-LDH in the composite film was 1.5%, the mechanical properties of the film were the best, with a ten-sile strength of 42 MPa and an elongation at break of 16.7%. The gas barrier performance of the film with this MgAl-LDH content was also the best, with a gas permeability of 16 mL/(m2·24 h·0.1 MPa). In addition, the introduc-tion of citric acid increases the number of hydrophilic groups inside the film, and the hydrophilic properties of the composite film are enhanced. MgAl-LDH can reduce the free volume inside the PVA film and enhance the mechanical收稿日期：2023-04-27基金项目：安徽省教育厅自然科学重点项目（2022AH050875）；安徽省科技重大专项（202103a06020005）；安徽省大学生创新创业项目（S202120364214）第44卷第19期张子怡，等：层状双金属氢氧化物/聚乙烯醇气体阻隔薄膜材料制备及性能研究·105·and barrier properties of the PVA film.KEY WORDS: polyvinyl alcohol; magnesium-aluminum layered bimetallic hydroxide; citric acid; composite film; bar-rier performance阻隔性薄膜指对气体、有机化合物等低分子量的化学物质具有非常低的透过性的薄膜。
海洋钻井平台压井管汇注乙二醇参数优化
2021年1月第37卷第1期石油工业技术监督Technology Supervision in Petroleum IndustryJan.2021Vol.37No.1海洋钻井平台压井管汇注乙二醇参数优化霍宏博1,2，张启龙2，李金泽2，张磊2，王文21.油气藏地质及开发工程国家重点实验室西南石油大学（四川成都610500）2.中海石油（中国）有限公司天津分公司（天津300459）摘要通过数值模拟，钻井管汇在放喷时具备天然气水合物形成条件，有可能堵塞节流阀，导致严重的事故。
实验研究证明天然气水合物形成的概率会随着注入乙二醇体积分数而变化，以此为依据，绘制乙二醇的注入参数图版，保持在压井过程中管汇中的乙二醇体积分数预防水合物形成。
对乙二醇体积分数对天然气水合物抑制效果进行实验研究，得到天然气井通过节流管汇进行放喷时的乙二醇推荐注入量，以及不同工况的注入参数、注入时机，避免管汇内达到天然气水合物的生产条件，保障井控安全。
关键词火成岩；井壁稳定；破岩机理Optimization of Glycol Injection Parameters of Kill Manifold on Offshore Drilling PlatformHuo Hongbo1,2,Zhang Qilong2,Li Jinze2,Zhang Lei2,Wang Wen21.Oil and Gas Reservoir Geology and Exploitation,Chengdu University of Technology(Chengdu,Sichuan610500,China)2.Tianjin Branch,CNOOC(China)Co.,Ltd.(Tianjin300459,China)Abstract Numerical simulation shows that the drilling manifold has the formation conditions of natural gas hydrate during blowout, which may block the throttle valve,resulting in loss of well control means and serious accidents.The experimental study shows that the probability of gas hydrate formation will change with the injected glycol concentration.Based on this,the injection parameter chart of ethylene glycol is drawn to keep the glycol concentration in the manifold during well killing to prevent hydrate formation.The experi⁃mental study on the inhibition effect of ethylene glycol concentration on natural gas hydrate was carried out.The recommended injec⁃tion amount of ethylene glycol,injection parameters and injection timing under different working conditions are obtained when the natu⁃ral gas well is blowout through the choke manifold,so as to avoid reaching the production conditions of natural gas hydrate formation in the manifold and ensure the safety of well control.Key words igneous rock;wellbore instability;rock breaking mechanism霍宏博,张启龙,李金泽,等.海洋钻井平台压井管汇注乙二醇参数优化[J].石油工业技术监督,2021,37(1):27-30.Huo Hongbo,Zhang Qilong,Li Jinze,et al.Optimization of glycol injection parameters of kill manifold on offshore drilling platform [J].Technology Supervision in Petroleum Industry,2021,37(1):27-30.0引言天然气水合物在低温、高压状态下生成，也叫可燃冰，它在陆地冻土区与深海区被视为一种新型清洁能源[1-3]，近期中国的成功开发已引起世界石油行业重视，但天然气水合物堵塞节流压井管汇将对钻井安全产生严重的负面影响[4-8]。
搅拌摩擦焊的工艺参数
Trans. Nonferrous Met. Soc. China 22(2012) 1064í1072Correlation between welding and hardening parameters offriction stir welded joints of 2017 aluminum alloyHassen BOUZAIENE, Mohamed-Ali REZGUI, Mahfoudh AYADI, Ali ZGHALResearch Unit in Solid Mechanics, Structures and Technological Development (99-UR11-46),Higher School of Sciences and Techniques of Tunis, TunisiaReceived 7 September 2011; accepted 1 January 2011Abstract: An experimental study was undertaken to express the hardening Swift law according to friction stir welding (FSW) aluminum alloy 2017. Tensile tests of welded joints were run in accordance with face centered composite design. Two types of identified models based on least square method and response surface method were used to assess the contribution of FSW independent factors on the hardening parameters. These models were introduced into finite-element code “Abaqus” to simulate tensile tests of welded joints. The relative average deviation criterion, between the experimental data and the numerical simulations of tension-elongation of tensile tests, shows good agreement between the experimental results and the predicted hardening models. These results can be used to perform multi-criteria optimization for carrying out specific welds or conducting numerical simulation of plastic deformation of forming process of FSW parts such as hydroforming, bending and forging.Key words: friction stir welding; response surface methodology; face centered central composite design; hardening; simulation; relative average deviation criterion1 IntroductionFriction stir welding (FSW) is initially invented and patented at the Welding Institute, Cambridge, United Kingdom (TWI) in 1991 [1] to improve welded joint quality of aluminum alloys. FSW is a solid state joining process which was therefore developed systematically for material difficult to weld and then extended to dissimilar material welding [2], and underwater welding [3]. It is a continuous and autogenously process. It makes use of a rotating tool pin moving along the joint interface and a tool shoulder applying a severe plastic deformation [4].The process is completely mechanical, therefore welding operation and weld energy are accurately controlled. B asing on the same welding parameters, welding joint quality is similar from a weld to another.Approximate models show that FSW could be successfully modeled as a forging and extrusion process [5]. The plastic deformation field in FSW is compared with that in metal cutting [6í8]. The predominant deformation during FSW, particularly in vicinities of thetool, is expected to be simple shear, and parallel to the tool surface [9]. When the workpiece material sticks to the tool, heat is generated at the tool/workpiece contact due to shear deformation. The material becomes in paste state favoring the stirring process within the thermomechanically affected zone, causing a large plastic deformation which alters micro and macro structure and changes properties in polycrystalline materials [10].The development of the mechanical behavior model, of heterogeneous structure of the welded zone, is based on a composite material approach, therefore it must takes into account material properties associated with the different welded regions [11]. The global mechanical behavior of FSW joint was studied through the measurement of stress strain performed in transverse [12,13] and longitudinal [14] directions compared with the weld direction. Finite element models were also developed to study the flow patterns and the residual stresses in FSW [15]. B ased on all these models, numerical simulations were performed in order to investigate the effects of welding parameters and tool geometry on welded material behaviors [16] to predict the feasibility of the process on various shape parts [17].Corresponding author: Mohamed-Ali REZGUI; E-mail: mohamedali.rezgui@ DOI: 10.1016/S1003-6326(11)61284-3Hassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í1072 1065 However, the majority of optimization studies of theFSW process were carried out without being connectedto FSW parameters.In the present study, from experimental andmodeling standpoint, the mechanical behavior of FSWaluminum alloy 2017 was examined by performingtensile tests in longitudinal direction compared with theweld direction. It is a matter of identifying the materialparameters of Swift hardening law [18] according to theFSW parameters, so mechanical properties could bepredicted and optimized under FSW operating conditions.The strategy carried out rests on the response surfacemethod (RSM) involving a face centered centralcomposite design to fit an empirical models of materialparameters of Swift hardening law. RSM is a collectionof mathematical and statistical technique, useful formodeling and analysis problems in which response ofinterest is influenced by several variables; its objective isto optimize this response [19]. The diagnostic checkingtests provided by the analysis of variance (ANOV A) suchas sequential F-test, Lack-of-Fit (LoF) test, coefficient ofdetermination (R2), adjusted coefficient of determination(2adjR) are used to select the adequacy models [20].2 Experimental2.1 Welding processThe aluminum alloy 2017 chosen for investigationhas good mechanical characteristics (Table 1), excellentmachinability and formability, and is mostly used ingeneral mechanics applications from high strengthsuitable for heavy-duty structural parts.Table 1 Mechanical properties of aluminum alloy 2017Ultimate tensile strength/MPaYieldstrength/MPaElongation/%Vickershardness427 276 22 118 The experimental set up used in this study was designed in Kef Institute of Technology (Tunisia). A 7.5 kW powered universal mill (Momac model) with 5 to 1700 r/min and welding feed rate ranging from 16 to 1080 mm/min was used. Aluminum alloy 2017 plate of6 mm in thickness was cut and machined into rectangular welding samples of 250 mm×90 mm. Welding test was performed using two samples in butt-configuration, in contact along their larger edge, fixed on a metal frame which was clamped on the machine milling table.To ensure the repeatability of the FSW process, clamping torque and flatness surface of the plates to be welded are controlled for each welding test. At the end of welding operation, around 80 s are respected before the withdrawal of the tool and the extracting of the welded parts. In this experimental study, we purpose to screen theeffects of three operating factors, i.e. tool rotational speed N, tool welding feed F and diameter ratio r, on hardening parameters from Swift’s hardening law such as strength coefficient (k), initial yield strain (İ0) and hardening exponent (n). The ratio (r=d/D) of pin diameter (d) to shoulder diameter (D), is intended to optimize the tool geometry [21í23]. The welding tool is manufactured from a high alloy steel (Fig. 1).Fig. 1 FSW tool geometry (mm)Preliminary welding tests were performed to identify both higher and lower levels of each considered factors. These limits are fixed from visual inspections of the external morphology and cross sections of the welded joints with no macroscopic defects such as surface irregularities, excessive flash, and lack of penetration or surface-open tunnels. However, among these limits one is not sure to have a safe welded joint so often, but they show great potential on defect avoidance. Figure 2 shows some external macroscopic defects observed beyond the limit levels established for each factor. Table 2 lists the processing factors as well as levels assigned to each, and Table 3 shows the fixed levels for other factors needed to success the welding tests.A face centered central composite design, which comes under the RSM approach, with three factors was used to characterize the nature of the welded joints by determining hardening parameters. In this design the star points are at the center of each face of the factorial space (Į=±1), all factors are run at three levels, which are í1, 0, +1 in term of the coded values (Table 4). The experiment plan has been run in random way to avoid systematic errors.2.2 Tensile testsThe tensile tests are performed on a Testometric’s universal testing machines FSí300 kN. The tensile test specimens (ASME E8Mí04) proposed for characterizing the mechanical behavior of the FSW joint, were cut inHassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í10721066Fig. 2 Types of macroscopic defectsTable 2 Levels for operating parameters for FSW processFactorLow level (í1) Center point (0) High level(+1)N /(r·min í1) 653 910 1280 F /(mm·min í1)67 86 109r /%33 39 44Table 3 Welding parametersPin height/ mm Shoulder diameter/ mm Small diameter pin/mm Tool’s inclination angle/(°) Penetrationdepth of shoulder/mm5.3 18 4 30.78longitudinal direction compared with the weld direction, so that active zone is enclosed in the central weld zone (Fig. 3). Figure 4 shows the tensile specimens after fracture.Ultimately, it is a matter of experimental evaluation of hardening parameters of the behavior of FSW joints (k , İ0, n ) according to Swift’s hardening law:n k )(p 0H H V (1)These parameters are required to identify the plastic deformation aptitude of the FSW joints. They are also needed for numerical simulations of forming operations on welded plates. The hardening parameters have been calculated by least square method (LSM) from the stressüstrain curves data. Table 4 shows the experimental design as well as dataset performance characteristics according to the FSW parameters of aluminum Alloy 2017.3 Experimental results3.1 Development of mathematical modelsAlthough the basic principles of FSW are very simple, it involves complex phenomena related to thermo-mechanical and metallurgical transformation that causes strong microstructural heterogeneities in the welded zone. From an energy standpoint, welding process is generated by converting mechanical energy provided by FSW tool into other types of energy such as heat, plastic deformation and microstructural transformations. The nonlinear character of these different dissipation forms can justify research for nonlinear prediction models whose accuracy generally depends on the order of the models relating the responses to welding parameters. For this reason, we chose the RSM which is helpful in developing a suitable approximation for the true functional relationships between quantitative factors (x 1, x 2, Ă, x k ) and the response surface or response functions Y (k , İ0, n ) that may characterize the nature of the welded joints as follows:r 21),,,(e x x x f Y k (2)Hassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í10721067Table 4 Face centered central composite design for FSW of aluminum alloy 2017Factors levelCoded Actual Hardening parameterTypeStandard orderN F r N /(r·m í1)F /(mm·min í1)r /% k /MPan İ0/%1 í1 í1 í165367 33629.7 0.3296 0.00202 1 í1 í1 1280 67 33 654.7 0.4514 0.0035 3 í1 1 í1 653109 33 587.8 0.3712 0.0025 4 1 1 í1 1280 109 33 689.2 0.4856 0.00555 í1 í1 1 653 67 44 642.3 0.4524 0.00256 1 í1 1128067 44 218.6 0.2447 0.0015 7 í1 1 1 653 109 44 685.5 0.4885 0.0035 Factorialdesign8 1 1 1 1280 109 44 332.5 0.3405 0.00209 0 0 0 91086 39 624.9 0.4257 0.0025 10 0 0 0 910 86 39 639.9 0.4292 0.0025 11 0 0 0 910 86 39 640.9 0.4011 0.0020 Center point12 0 0 0 910 86 39 598.6 0.3960 0.0023 13 í1 0 0 653 86 39 690.6 0.4748 0.0027 14 1 0 0 128086 39 505.6 0.3909 0.0030 15 0 í1 091067 39499 0.3317 0.001716 0 1 0 910 109 39 545.6 0.4157 0.0026 17 0 0 í1 910 86 33 672.1 0.4385 0.0027 Star point18 0 019108644 509.7 0.41750.0019Fig. 3 Tensile test specimens (ASME E8Mí04) cut in longitudinal direction compared with weld direction (mm)Fig. 4 Tensile specimens after fractureThe residual error term (e r ) measures theexperimental errors. Such relationship was developed as quadratic polynomial under multiple regression form [19,20]:¦¦¦ r 20e x x b x b x b b Y j i ij i ii i i (3)where b 0 is an intercept or the average of response; b i , b ii , and b ij represent regression coefficients. For the three factors, the selected polynomial could be expressed as:2332222113210r b F b N b r b F b N b b YFr b Nr b NF b 231312 (4)In applying the RSM, the independent variable Y was viewed as surface to which a mathematical model was fitted. The adequacy of the developed model was tested using the analysis of variance (ANOV A) which quantifies the amount of variation in a process and determines if it is significant or is caused by random noise.3.2 Mathematic model of hardening parametersTable 5 lists the coefficients of the best linear regression models. All selected parameters (N , F , r ) for k and İ0 are statistically significant (P-value less than 0.05) at the 95% confidence level. However, for the response n , the term b 3r having a P-value=0.0654>0.05 is not statistically significant at the 95% confidence level even though the term b 13Nr is statistically significant. Consequently, b 3(r ) is kept in the model to improve the Lack-of-Fit test (Table 6). Furthermore, only theHassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í10721068Table 5 Coefficients of regression models for hardening parametersStrength coefficient (k) Hardeningcoefficient(n) Initial yield strain (İ0) CoefficientEst. SEP-value Est SE P-valueEst/10í4 SE/10í4 P-value b0 610.39,48<10í4 0.422 0.0073 <10-4 22.8 1.010 <10-4 b1 í83.58.48<10í4 í0.020 0.0065 0.0091 2.30 0.912 0.0267 b2 19.68.480.0410.0290.00650.00084.900.9120.0002b3 í84.58.48<10í4 í0.013 0.0065 0.0654 í4.80 0.912 0.0002 b11 5.561.3670.0009b22 í61.812.720.0005í0.0310.00980.009b33b12b13 í112.99.48<10í4 í0.074 0.0073 <10-4 -8,75 1.010 <10-4 b23R2 95.90% 92.38% 92.84%2adjR 94.19% 89.21% 89.86% SE of est. 30.7 0.021 2.9×10í4Est: Estimate; SE: Standard Error; SE of est.: Standard error of estimateTable 6 ANOV A for hardening parametersk n İ0Source of variationSS Df P-Value SS Df P-Value SS/10í7 Df P-Value Model 263946.0 5 <10í4 0.062357 5 <10í4 129.324 5 <10í4Residual 11296.4 12 0.005140912 9.97 12Lack-of-Fit 10130.4 9 0.2065 0.00428669 0.3678 8.295 9 0.3723 Pure error 1166.07 3 0.0008543 3 1.675 3 Total correction 275243.017 0.06749817 139.294 17 DW-value 1.31 1.42 2.26DW: Durbin-Watson statistic; SS: Sum of squares; D f: Degree of freedominteraction (Nír) is statistically significant on the three responses (Fig. 5). According to the adjusted R2 statistic, the selected models explain 94.19%, 89.21% and 89.86% of the variability in k, n and İ0 respectively.The ANOV A (Table 6) for the hardening parameter shows that all models (k, n, İ0) represent statistically significant relationships between the variables in each model at the 99% confidence level (P-value<10í4). The Lack-of-Fit test confirms that these models (k, n, İ0) are adequate to describe the observed data (P-value>0.05) at the 95% confidence level. The DW statistic test indicates that there is probably not any serious autocorrelation in their residuals (DW-value>1.4). The normal probability plots of the residuals suggest that the error terms, for these models, are indeed normally distributed (Fig. 6). The response surface models in terms of coded variables (Eqs. (5)í(7)) are shown in Fig. 7.k=610.3–83.5 N+19.6 F–84.5 r –61.8 F2–112.9 Nr(5) n=0.422–0.020 N+0.029 F–0.013 r–0.031 F2–0.074 Nr(6) İ0=22.8+2.3 N+4.90 F–4.80 r+5.56 N2–8.75 Nr(7) Fig. 5 Interaction plots of Nír (rotational speedídiameter ratio): (a) Strength coefficient k; (b) Hardening coefficient n;(c) Initial yield strain İ0Hassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í1072 1069Fig. 6 Normal probability plots for residual: (a) Strength coefficient k; (b) Hardening coefficient n; (c) Initial yield strain İ04 Validation of identified modelsValidation tests of the identified models were performed through comparative study between the experimental models (EM) of tensile tests and the computed responses given by numerical simulations of the same tests (Fig. 8). The computed responses, expressed in the form of tension and elongation, wereFig. 7 Response surfaces plots: (a) Strength coefficient k;(b) Hardening coefficient n; (c) Initial yield strain İ0 established by examining welded joints having an elastoplastic behavior in accordance with the Swift hardening law (Eq. (1)). These computed responses were deduced from the numerical simulations using the finite element code Abaqus/Implicit, in which the introduced elastoplastic behavior was obtained from the least square hardening models (LSHM) (Table 4) and the response surface hardening models (RSHM) (Table 5). The highest deviations (<10%), between EM and computed response, were recorded with the RSHM. Increasing deviations, as shown in Fig. 8, is due to the effect of combining damage with plastic strains accumulatedHassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í10721070Fig. 8 Relationship between tension and elongation: Confrontation between experimental model (EM), and computed responses (LSHM, RSHM) for three experimental testsduring the onset of localized necking.The relative average deviation criterion (EM/LSHM ]) between the experimental data and the numerical predictions of tensions, was used to assess the quality of the identified models.¦¸¸¹·¨¨©§'' '2exp num exp exp/num )()()(1i i i L F L F L F N] (8)where N is the number of experimental measurements,F exp (ǻL i ) and F num (ǻL i ) are respectively the experimental and predicated tensions relating to the i-th elongation ǻL i . Figure 9 illustrates that the relative average deviation of EM/LSHM (EM/LSHM ]) ranges between 1.64% and 6.75% while the relative average deviation of EM/RSHM (EM/RSHM ]) ranges between 4.52% and 9.32%.Fig. 9 Distribution of relative average deviations for most representative experimental testsFor the deviation within limits fluctuating between 4.52% and 6.75% the estimated models (LSHM and RSHM) are comparable. This applies particularly to welded joints characterized by a strength coefficient (k ), ranging from 520 to 610 MPa and a hardening exponent (n ) ranging between 0.30 and 0.45.5 DiscussionIn this study we evaluated, using RSM, the effect of FSW parameters such as tool rotational speed, welding feed rate and diameter ratio of pin to shoulder on the plastic deformation aptitudes of welded joints. The performed analysis highlights the incontestable significant effects of rotational speed (N ), welding feed rate (F ) and the interaction (Nír ) between rotational speed and diameters ratio on hardening parameters (k , n , İ0) according to Swift law. The established models show that tool diameter ratio has a linear effect only on (k ) and (İ0), it does not have any quadratic effect. They also show that rotational speed has a quadratic effect solely on (İ0); while welding feed rate has a quadratic effect on both (k ) and (n ).In addition, numerical simulation of tensile tests of welded joints has been made possible through the predictive models (LSHM and RSHM) of Swift’s hardening parameters. To judge whether the models represent correctly the data, a comparative study between the experimental response and the computed response, expressed in terms of tension-elongation, was carried out. It was found that the relative average deviation betweenHassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í1072 1071experimental model and numerical models is less than 9.5% in all cases.Moreover, correlation between welding and hardening parameters provided has many benefits. The correlation relationships can solve inverse problem relating to optimal choice of parameters linked up with the desired welded joints properties to produce welds having tailor-made mechanical properties. The correlation predictions offer the possibility to identify the behavior of friction stir welded joints necessary for finite element simulations of various forming processes while minimizing experimental cost and time. Ultimately, understanding correlations can be useful for studies on reliability of welded assemblies in service life expectancy.6 Conclusions1) Rotational speed and welding feed rate are the factors that have greater influence on hardening parameters (k, n, İ0), followed by diameter ratio that has no influence on the hardening coefficient (n).2) The numerical models RSHM were compared with those through LSHM and confronted to the experimental results. Indeed, within the limit of a relative average deviation of about 9.3%, between the experimental model and numerical models expressed in terms of tension-elongation, the validity of these models is acceptable.3) The predictive models of work-hardening coefficients, established taking into account the FSW parameters, have made possible the numerical simulation of tensile tests of FSW joints. These results can be used to perform multi-criteria optimization for producing welds with specific mechanical properties or conducting numerical simulation of plastic deformation of forming process of friction stir welded parts such as hydroforming, bending and forging.References[1]THOMAS W M, NICHOLAS E D, NEEDHAM J C, MURCH M G,TEMPLE-SMITH P, DAWES C J. Friction stir butt welding,PCT/GB92/ 02203 [P]. 1991.[2]XUE P, NI D R, WANG D, XIAO B L, MA Z Y. Effect of friction stirwelding parameters on the microstructure and mechanical propertiesof the dissimilar AlíCu joints[J]. Materials Science and EngineeringA, 2011, 528: 4683í4689.[3]LIU H J, ZHANG H J, YU L. Effect of welding speed onmicrostructures and mechanical properties of underwater friction stirwelded 2219 aluminum alloy [J]. Materials and Design, 2011, 32:1548í1553.[4]MISHRA R S, MA Z Y. Friction stir welding and processing [J].Materials Science and Engineering R, 2005, 50: 1í78.[5]ARB EGAST W J. A flow-partitioned deformation zone model fordefect formation during friction stir welding [J]. Scripta Materialia,2008, 58: 372í376.[6]LEWIS N P. Metal cutting theory and friction stir welding tooldesign [M]. NASA Faculty Fellowship Program Marshall SpaceFlight Center, University of ALABAMA, NASA/MSFC Directorate:Engineering (ED-33), 2002.[7]ARB EGAST W J. Modeling friction stir welding joining as ametalworking process, hot deformation of aluminum alloys III [C].San Diego: TMS Annual Meeting, 2003: 313í327.[8]ARTHUR C N Jr. Metal flow in friction stir welding [R]. NASAmarshall space flight center, EM30. Huntsville, AL 35812.[9]FONDA R W, B INGERT J F, COLLIGAN K J. Development ofgrain structure during friction stir welding [J]. Scripta Materialia,2004, 51: 243í248.[10]NANDAN R, DEBROY T, BHADESHIA H K D H. Recent advancesin friction stir weldingüProcess, weldment structure and properties[J]. Progress in Materials Science, 2008, 53: 980í1023.[11]LOCKWOOD W D, TOMAZ B, REYNOLDS A P. Mechanicalresponse of friction stir welded AA2024: Experiment and modeling[J]. Materials Science and Engineering A, 2002, 323: 348í353. [12]SALEM H G, REYNOLDS A P, LYONS J S. Microstructure andretention of superplasticity of friction stir welded superplastic 2095sheet [J]. Scripta Materialia, 2002, 46: 337í342.[13]LOCKWOOD W D, REYNOLDS A P. Simulation of the globalresponse of a friction stir weld using local constitutive behavior [J].Materials Science and Engineering A, 2003, 339: 35í42.[14]SUTTON M A, YANG B, REYNOLDS A P, YAN J. B andedmicrostructure in 2024–T351 and 2524-T351 aluminum friction stirwelds, Part II. Mechanical characterization [J]. Materials Science andEngineering A, 2004, 364: 66í74.[15]ZHANG H W, ZHANG Z, CHEN J T. The finite element simulationof the friction stir welding process [J]. Materials Science andEngineering A, 2005, 403: 340í348.[16]ZHANG Z, ZHANG H W. Numerical studies on controlling ofprocess parameters in friction stir welding [J]. Journal of MaterialsProcessing Technology, 2009, 209: 241í270.[17]B UFFA G, FRATINI L, SHIVPURI R. Finite element studies onfriction stir welding processes of tailored blanks [J]. Computers andStructures, 2008, 86: 181í189.[18]SWIFT H W. Plastic instability under plane stress [J]. Journal of theMechanics and Physics of Solids, 1952, 1: 1í18.[19]MONTGOMERY D C. Design and analysis of experiments [M].Fifth Edition. New York: John Wiley & Sons, 2001: 684.[20]MYERS R H, MONTGOMERY D C, ANDERSON-COOK C M.Response surface methodology: Process and product optimizationusing designed experiment [M]. 3rd Edition. New York: John Wiley& Sons, 2009: 680.[21]VIJAY S J, MURUGAN N. Influence of tool pin profile on themetallurgical and mechanical properties of friction stir welded Al–10% TiB2 metal matrix composite [J]. Materials and Design,2010, 31: 3585í3589.[22]ELANGOV AN K, BALASUBRAMANIAN V. Influences of tool pinprofile and tool shoulder diameter on the formation of friction stirprocessing zone in AA6061 aluminum alloy [J]. Materials andDesign, 2008, 29: 362í373.[23]PALANIVEL R, KOSHY MATHEWS P, MURUGAN N.Development of mathematical model to predict the mechanicalproperties of friction stir welded AA6351 aluminum alloy [J]. Journalof Engineering Science and Technology Review, 2011, 4(1): 25í31.Hassen BOUZAIENE, et al/Trans. Nonferrous Met. Soc. China 22(2012) 1064í107210722017䪱 䞥 ⛞ ⛞⹀ ⱘ ㋏Hassen BOUZAIENE, Mohamed-Ali REZGUI, Mahfoudh AYADI, Ali ZGHALBesearch Unit in Solid Mechanics, Structures and Technological Development (99-UR11-46),Higher School of Sciences and Techniques of Tunis, Tunisia㽕˖ 2017䪱 䞥䖯㸠 ⛞ ˈ㸼䗄Swift⹀ 㾘 DŽ䞛⫼䴶 䆒䅵 ⊩䖯㸠⛞ ⱘ Ԍ 偠䆒䅵DŽ䞛⫼ Ѣ ѠЬ⊩ 䴶⊩ⱘ2⾡ 䆘Ԅ ⛞ ⛞ ㋴ ⹀ ⱘ DŽ䞛⫼ 䰤 Abaqus ⛞ Ԍ⌟䆩㒧 DŽⳌ 㒧 㸼 ˈ 偠㒧 㒧 䕗 DŽ䖭ѯ㒧 㛑⫼Ѣ 偠 Ⳃ Ӭ ˈ 㸠 ԧ⛞ ⛞ 䳊ӊ 䖛Ё ⱘ ˈ ⎆ ǃ 䬏䗴DŽ䬂䆡˖ ⛞ ˗ 䴶 ⊩˗䴶 Ё 䆒䅵˗⹀ ˗ ˗Ⳍ(Edited b y LI Xiang-qun)。
金属-有机骨架MIL-88A (Fe)及其复合物的合成与高级氧化降解水体有机污染物的研究进展
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成条件( 如加热温度和溶剂种类) 对颗粒尺寸有明显
影响ꎬ通常以 Ｈ ２ Ｏ 为溶剂且提高反应温度可得到粒
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关注度较高. ＭＩＬ 系列的铁基 ＭＯＦｓ 有 ＭＩＬ￣５３( Ｆｅ)、
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OptiStruct_Optimization
• Shape: is an automated way to modify the structure shape based on a predefined
shape variables to find the optimal shape.
• Size: is an automated way to modify the structure parameters (Thickness, 1D
Copyright © 2008 Altair Engineering, Inc. All rights reserved.
Day 1 Agenda
• • • Introduction Structural Optimization Concepts OptiStruct Features: FEA Solver and Optimizer
•
• • • •
Exercise 5.4: Creating Shapes
Exercise 5.5: Pre-processing the Shape Optimization of a Channel Exercise 5.6: Shape Optimization of a Rail Joint Exercise 5.7: Shape optimization of a 3-D bracket model using Free-Shape method
•
Shape Optimization Concepts (Morphing based and Free Shape)
• •
• • •
Exercise 5.1: Basics of Domains and Handles Exercise 5.2: Morph Volume Exercise 5.3: Mapping a mesh to a new geometry
Journal of Environmental Chemical Engineering
Characterization of nano zero-valent iron (nZVI) and its application in sono-Fenton process to remove COD in palm oil mill effluent
M.R. Taha a, A.H. Ibrahim b,*
This present study highlights the characterization of the nZVI particle and examines the effects of pH, ultrasound intensity (%), and ultrasound duration on the nZVI particle to produce Fe2+. Tests have also been conducted to analyze the application of the nZVI particle as a replacement for FeSO4 in the sono-Fenton process to remove chemical oxygen demand (COD) particularly in palm oil mill effluent (POME).
Journal of Environmental Chemical Engineering 2 (2014) 1–8
Contents lists available at ScienceDirect
Journal of Environmental Chemical Engineering
journal homepage: /locate/jece
The combination of ultrasound with the Fenton process (sono-
翻译英文文献
Optim Eng(2011)12:175–198DOI10.1007/s11081-009-9094-2Optimal structure of gas transmission trunklinesJean André·J.Frédéric BonnansReceived:5January2009/Accepted:15October2009/Published online:14November2009©Springer Science+Business Media,LLC2009Abstract In this paper,we consider the optimal design of a straight pipeline system. Suppose a gas pipeline is to be designed to transport a specifiedflowrate from the entry point to the gas demand point.Physical and contractual requirements at supply and delivery nodes are known as well as the costs to buy and lay a pipeline or build a compressor station.In order to minimize the overall cost of creation of this main-line,the following design variables need to be determined:the number of compressor stations,the lengths of pipeline segments between compressor stations,the diameters of the pipeline segments,the suction and discharge pressures at each compressor sta-tion.To facilitate the calculation of the design of a pipeline,gas engineers proposed, in several handbooks,to base their cost-assessments on some optimal properties from previous experiences and usual engineering practices:the distance between compres-sors is constant,all diameters are equal,and all inlet(resp.outlet)pressures are equal. The goals of this paper are(1)to state on which assumptions we can consider that the optimal properties are valid and(2)to propose a rigorous proof of the optimal prop-erties(based on nonlinear programming optimality conditions)within a more general framework than before.Afirst version of this paper was presented at the International Conference on Engineering Optimization(EngOpt2008),Rio de Janeiro,Brazil,01–05June2008.J.AndréR&I Division,Simulation Optimisation Section,GDF SUEZ,93211La Plaine Saint Denis,FranceJ.AndréInstitut des Mers du Nord,Universitédu Littoral Côte d’Opale,59140Dunkerque,Francee-mail:Jean.Andre@univ-littoral.frJ.F.Bonnans( )INRIA-Saclay and Centre de Mathématiques Appliquées,Ecole Polytechnique,91128Palaiseau, Francee-mail:Frederic.Bonnans@inria.fr176J.André,J.F.Bonnans Keywords Gas network·Pipeline system·Network design·Optimality conditions·Generalized multipliers1IntroductionThe gas trunkline system is a long-distance,wide-diameter pipeline system that gen-erally links a major supply source(production area,natural gas processing plants...) with a market area.Between the source and the delivery points,a number of com-pressor stations are located along the transmission system.These stations contain several compressor units whose purpose is to increase the pressure(which has de-creased since the previous compressor station),and thus,facilitate theflow of natural gas along the pipeline.Most compressor units are driven with natural gas(taken from the pipeline)turbines but,more recently,the use of electric motors has been growing for environmental reasons.In the classical sense,the pipeline design problem can be addressed as follows. Suppose a gas pipeline is to be designed to transport a specified quantity of gas per time from the entry point to the gas demand point.Physical and contractual require-ments at supply and delivery nodes(mainly minimal and maximal bounds on pres-sures)are known as well as the costs to buy and lay a pipeline or build a compressor station.In order to minimize the overall cost of creation of this mainline,the fol-lowing design variables need to be determined:the number of compressor stations, the lengths of pipeline segments between compressor stations,the diameters of the pipeline segments,the suction and discharge pressures at each compressor station.Therefore,the design of natural gas transmission involves a high number of alter-natives.Edgar et al.(1978)were thefirst to apply mathematical programming techniques to such an open-ended problem.They considered the minimization of the total cost of operation per year including the capital cost in their objective function against which the above parameters are to be optimized.The capital cost of the compres-sor stations was either a linear function of the horsepower or a linear function of the horsepower with afixed capital outlay for zero horsepower to account for installation, foundation,and other costs.Thefirst cost relationship allowed direct application of non linear programming,but it did require the initial postulation of compressor lo-cation.The technique,when converged,indicated which compressor stations should be deleted.They solved the second scenario using the branch and bound technique to handle the integer variables which are the number of compressors.They applied their techniques not only to gunbarrel pipelines but also to branched systems(withfixed branch lengths).Soliman and Murtagh(1982)showed that a commercial nonlinear solver(MINOS, Murtagh and Saunders1998)could be used to solve large instance of the continuous pipeline design problem(withoutfixed installation outlay)within moderate comput-ing times.More recently,Babu et al.(2003)applied Differential Evolution,an evolutionary computation technique,to the same problem and example as Edgar et al.(1978). Both scenarios above mentioned have been solved by these population based-searchOptimal structure of gas transmission trunklines177 algorithms.They found an optimal value closed to the one in Edgar et al.(1978), although the solution found is not so close to the bounds as the one in Edgar et al. (1978).To facilitate the calculation of the design of a pipeline,gas engineers proposed to reduce the high number of alternatives by applying criteria based on previous ex-periences and/or usual engineering practices.Afirst class of procedures is a trial and error process among several candidate designs proposed beforehand(Mohitpour et al.2003).For that purpose,Lang(1988)highlights the usefulness of simulation softwares to assess what is the best trade-off between compressor costs and pipeline costs.A second approach is to establish some optimal properties to reduce the num-ber of variables.Hence,Cheeseman(1971)states that the compression ratios giving the minimum energy consumption should be equal for each station.Kabirian and Hemmati(2007)assume that the new compressor stations are located in the middle of pipes.In the French handbook of Chapon“Design and Construction of gas transportation networks”(Chapon1990),the following assumptions are taken:–the layout is horizontal,–theflowrate Q is constant along the pipeline,–the number of compressor stations is known.Besides,the power is approximated by a specific logarithmic formulation.In this case,Chapon asserts,without proof,that the resolution of the pipeline design prob-lem with differential calculation leads to the following optimal characteristics of the network:–diameters are equal on each pipeline segments(including the terminal segments),–discharge pressures for all compressor stations are equal to the maximum admissi-ble operational pressure of the pipelines,–compressor stations are equidistant,and hence,compressor ratios are equal. Thanks to these properties,the computation is strongly simplified with only two re-maining variables to determine:one optimal diameter and one optimal compression ratio for the whole pipeline.Then,it is only necessary to select the right number of compressor station which minimizes the associated costs.Boucly(1992)presents a partial proof of the above properties but the arguments were not very clear and al-ways limited to the Chapon’s framework.In his PhD Thesis,Hafner(1994)does not discuss the validity of these assertions and only details the calculation steps of the two last remaining variables.More recently,Ainouche(2004)based his cost analysis on the same properties.As the best of our knowledge,no paper has been published to give a theoretical proof of these optimal properties.The goals of this paper are to state on which assumptions we can consider that the optimal properties are valid and to propose a solid proof of the optimal proper-ties(based on nonlinear programming optimality conditions)within a more general framework than before.178J.André,J.F.Bonnans 2Physical backgroundA gas network is made of pipelines and compressor stations.In this section,physical rules are recalled as well as simplifications made for design purposes.2.1PipesLet us consider the physical parameters related to a single pipe:–Q,theflowrate in a pipe,–πi,the inlet square pressure(or inlet head)of the pipe,–πo,the outlet square pressure(or outlet head)of the pipe,–L,the length,–D the internal diameter of the pipe.Let us write the Weymouth equation(Katz et al.1959;Mohitpour et al.2003) modeling the pressure loss on a pipe element:πi−πo=K1.d.T.Z av(πi,πo).λ(Q,D).Q2.LD(1)with–K1(constant)function of P0,standard pressure,T0,standard temperature andρA, the mass density of dry air,–d,the gas specific gravity compared with air,T,the gas temperature,–Z av(πi,πo),the average gas compressibility factor,function of the suction and discharge pressures.Its expression is as follows,where C<0is a constant and theaverage pressure P av,defined as P av=23P i P oP i+P o ,with P i=√πi and P o=√πo(Mohitpour et al.2003):Z av=1+C.P av(πi,πo),(2)–λ(Q,D),the friction factor depending on the diameter and theflow regime(lami-narflow,mixed or transitionflow,or fully turbulentflow).In this paper,β=K1.d.T.Z av(πi,πo).λ(Q,D)will be considered as a constant regarding the inlet and outlet pressures and the diameter.This reasonable assumption for design purpose has been made in previous papers,e.g.(Edgar et al.1978).The drop pressure equation will be written as follows:πi−πo=β.Q2.LD.(3)2.2Compression powerLet us defineπs,the suction square pressure andπd,the discharge square pressure. The power of an adiabatic compressor is given by this formula(Katz et al.1959; Mohitpour et al.2003):ˆW=1ηad .K2.T s.Z av(πs,πd).γγ−1.Q.πdπsγ−12γ−1,(4)Optimal structure of gas transmission trunklines 179with Z av defined above (see (2)),and:–K 2(constant)function of P 0,standard pressure and T 0,standard temperature,–γ,the specific heat ratio,ηad ,the efficiency constant and T s ,the inlet temperature.This power is adjusted to recover ISO conditions at 15°C:W =ˆWpf 1.pf 2.pf 3(5)with pf 1=0.95,pf 2=0.97,pf 3=0.98.By setting average values for these factors,a well-accepted law is that the com-pression horsepower can be written as follows,for some positive constants γ1and γ2:W =γ1.Q. πd π γ22−1 .(6)Mandatory pressure drops at the entry and the exit of a compressor station are assumed to be negligible.If several compressors are available in a same compressor station,the total horsepower is the sum of the power of each compressor.3Mathematical programming backgroundSince our method consists in solving the first-order necessary optimality conditions,we will in this section give a brief account of them.Consider the following nonlinear programming problem with equality,inequality and bound constraints:⎧⎪⎪⎪⎨⎪⎪⎪⎩min x ∈R n f (x)g i (x)=0,i =1,...,p h i (x)≤0,i =1,...,q x j ≤x j ≤¯x j ,j =1,...,n,(7)where f :R n →R ,g :R n →R p and h :R n →R q are C 1mappings,and x j <¯x j ,j =1,...,n .The Lagrangian function in non-qualified form associated with this problem isL (x,η,θ,u,v):=η0f (x)+pi =1θi g i (x)+q i =1ηi h i (x)+n j =1 u i (x i −x i )+v j (x i −¯x i ) .(8)Its derivative w.r.t.the primal variable is∇x L (x,η,θ,u,v)=η0∇f (x)+pi =1θi ∇g i (x)+q i =1ηi ∇h i (x)−u +v.(9)180J.André,J.F.Bonnans We say that(θ,η,u,v)is a generalized Lagrange multiplier associated with x ∈R n if the following holds:⎧⎪⎪⎪⎨⎪⎪⎪⎩η≥0;u≥0;v≥0;|η|+|θ|+|u|+|v|>0;∇x L(x ,η,θ,u,v)=0;g(x )=0;h i(x )≤0;ηi h i(x )=0;i=1,...,q;x j≤x j≤¯x j;u j(x j−x j)=v j(¯x j−x j)=0,j=1,...,n.(10)The setΛG(x )of generalized Lagrange multipliers associated with x is a poly-hedral convex cone;ifη0=0(resp.η0=1)we say that(η,θ,u,v)is a singular (grange)multiplier.The set of Lagrange multipliers is denotedΛL(x ).The Mangasarian-Fromovitz qualification hypothesis(Mangasarian and Fromovitz1967) is⎧⎪⎨⎪⎩Dg(x )is onto,and there exists d∈Ker Dg(x );∇h i(x )·d<0,if h i(x )=0,j=1,...,q,d j>0if x j=x j;d j<0if x j=¯x j,j=1,...,n.(11)This is desirable property,as shows the following well-known result,see John(1948), Mangasarian and Fromovitz(1967)and Bonnans and Shapiro(2000,Sect.5.2).Lemma1If x is a local solution of(7),then(i)ΛG(x )=∅,and(ii)Condition (11)holds iff one of the following conditions holds:(a)the setΛL(x )of Lagrange multiplier is nonempty and bounded,(b)the set of singular multipliers is empty.It may be more effective to express the optimality conditions in term of the re-stricted Lagrangian function(in which the bound constraints are not dualized):L R(x,η,θ):=η0f(x)+pi=1θi g i(x)+qi=1ηi h i(x).(12)Denote byΛRG(x )the set of reduced generalized multipliers,i.e.,couples(η,θ)∈R p×R q such that(η,θ,u,v)∈ΛL(x ),for some(u,v)∈R n×R n.Whenη0=1, we also call Lagrange multipliers the elements ofΛRG(x ).It is easily checked that (η,θ)∈ΛRG(x )iff⎧⎪⎪⎪⎨⎪⎪⎪⎩g(x )=0;h i(x )≤0;ηi h i(x )=0;i=1,...,q;For all1≤j≤n:∂∂x jL R(x ,η,θ)⎧⎪⎨⎪⎩≥0if x j=x j;≤0if x j=¯x j;=0otherwise.(13)We will say that x is a critical point of problem(7)ifΛG(x )=∅,and that x is a nondegenerate critical point of problem(7)ifΛL(x )=∅.Optimal structure of gas transmission trunklines181 4Problem formulationOur goal is to determine the least-cost configuration of a pipeline(with compressors) linking one supply node to one delivery point without any withdrawals and assump-tions on the compressor stations locations.Let us define a“section”k,as the association of a pipe,oriented in the direction of theflow,followed by a downstream compressor station that compensates for the pres-sure drop of the upstream pipe.The compression occurs at the outlet of the section. There is no loss of generality in assuming such a structure,since either the compres-sion ratio can be taken equal to1,or the length of a section can be zero(not both of them of course).4.1Objective functionThe cost model will be equivalent to the model used by Edgar et al.(1978),Boucly (1992)or Soliman and Murtagh(1982).The objective function comprises the sum of terms for each section consisting of the annualized capital cost of the pipe and compressor,and the operation cost of the compressor.The annualized capital costs for each pipeline section depend linearly on the pipe diameter and length with a factorαp,the amortization factor reducing the capital cost to an annual cost.C pipe=αp LD.(14)Operating and maintenance charges for a compressor station are directly related to the horsepower O c.The total capital cost of a compressor station is divided into two parts:–an initialfixed installation outlay B,–a cost proportional to the power:C c W,where C c is the compressor capital cost per unit horsepower.The functionϕof compression costs yielded by the installation of a compressor sta-tion is then given by:ϕπdπ=αc Wπdπ+B,(15)whereαc:=O c+C c represent the annualized capital cost and operating cost per unit horsepower,resp.The problem is tofind the number n of compressor stations,diameters D k,section lengths L k,and suction and discharge pressures(πs k,πd k)that minimize the costs to lay pipes and/or build compressor stations:φ(D,L,πs,πd):=nk=1αp L k D k+ϕπs kπk.(16)Note that,forfixed n,the constant B plays no role in the minimization problem.182J.André,J.F.Bonnans We will assume the following properties on the functionϕ:(i)ϕis of class C1:(0,∞)→R+;(ii)ϕ (t)>0,t∈(0,∞),(17) where byϕ we denote the derivative ofϕ.In particular,the cost of compression is increasing with the square compression ratioρ:=πd/πs,and the latter is greater or equal to1.4.2ConstraintsWe adopt the following notations:–πd k−1:inlet head of section k,equal to the discharge head of the previous upstream section k−1,–πs k:outlet head of section k,is the suction head of the compressor station of that section,–β :=βQ2,afixed coefficient.With these notations,the pressure drop equation on section k is as follows:πd k−1−πs k=β L kDσk,k=1,...,n,(18)where the input headπd0and output headπd n are given,andσ≈5for gas networks. Since other values may be used for differentfluids,and our results hold with an arbitrary value,we adopt this more general law.On every compressor station,the discharge pressure cannot be less than the suction pressure:πs k≤πd k,k=1,...,n.(19) In this model we do not give bounds on the square compression ratioρk:=πd k/πs k on section k(other than those that are consequences of the lower and upper bounds on pressures).The sum of length of section must equal the distance between the supply node and the delivery point:nk=1L k= .(20) In addition,upper and lower bounds are set on diameters and pressures:0<D min≤D k≤D max,πmin≤πs k≤πmax,(21)πmin≤πd k≤πmax,k=1,...,nwith D max,the maximal commercial diameter proposed by the contractors of a gas transportation company,P0,standard pressure,and MOP,the maximum operational pressure of the pipes equal for every section.We denoteπmin:=P20,πmax:=MOP2.Note that the engineering practice is that diameters can take afinite number of values corresponding to market standards.Our model can therefore be interpreted as a continuous relaxation of a mixed-integer optimization problem.Optimal structure of gas transmission trunklines183 As boundary conditions of the network,we consider in this paper that thefirst inlet pressure and the last outlet pressure are given.4.3ProgramThe program to solve is then the following(writingfirst equality constraints,then bound constraints and ending by general inequality constraints):⎧⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎨⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎪⎩min D,L,πs,πdφ:=nk=1(αp L k D k+ϕk(πd kπsk))β L kDσk−πd k−1+πs k=0,k=1,...,n(a)−nk=1L k=0(b)πd=¯πd0,πd n=¯πd n;(c)πs k−πd k≤0,k=1,...,n(d)D min≤D k≤D max,k=1,...,n(e)πmin≤πs k≤πmax,k=1,...,n(f)πmin≤πd k≤πmax,k=1,...,n−1(g)(22)We assume that,for each section k,the functionϕk satisfies the generic proper-ties(17).In some statements we will assume thatϕk satisfies(6)and(15).These hypotheses are applicable to a wide class of pipeline design problem.5Necessary optimality conditionsIn the formulation of the problem we will actually considerπd0andπd n as data(and not optimization variables as in formulation(22).We denote by(λ,μ,η)the La-grange multipliers associated resp.to pressure drop(22)(a),total length(22)(b),and compression constraints(22)(d).The restricted Lagrangian function of program(22)isL(D,L,πs,πd,λ,μ,η)=η0nk=1αp L k D k+ϕkπd kπs k+nk=1λkβ L kDσk−πd k−1+πs k+μ−nk=1L k+nk=1ηkπs k−πd k.(23)For later use,we note the expressions of the partial derivatives of the Lagrangian w.r.t.primal variables(reminding thatρk:=πd k/πs k):∂L ∂L k =η0αp D k+λkβDσk−μ,k=1...,n,(24)184J.André,J.F.Bonnans∂L ∂D k =η0αp L k−σβ L kλkDσ+1k=L kη0αp−σβλkDσ+1k,k=1...,n,(25)∂L ∂πs k =−η0πd k(πs k)2ϕ k(ρk)+λk+ηk,k=1...,n,(26)∂L ∂πk =η0πs kϕ k(ρk)−λk+1−ηk,k=1...,n−1.(27)Our analysis will be based on thefirst-order optimality system.In most cases,it allows to compute the optimal design of the network.There are some singular situa-tions,however,where the optimality system provides no much information.Example1(Special case1)Assume thatπd0=πmin.Then,in view of the drop equa-tion,L1=0andπs1=πmin.Takeμ=0and all components ofλandηequal to zero, except forλ1>0.Then the equations of a critical point are satisfied,and at the same time we get no useful information on the solution.In this case we have to change the formulation of the problem by considering L1=0andπs1=πmin as data,and taking the equality(22)(a)for k=2to n only into account.Therefore(24)–(26)hold for k=2to n only.We can assume that thefirst compressor is active,and hence,πs1<πd1andη1=0.(28)Example2(Special case2)Assume thatπd n=πmin.Then,in view of the drop equa-tion,πs n=πmin.Takeμ=0and all components ofλandηequal to zero,except forηn>0.Again the equations of a critical point are satisfied,but we get no useful information on the solution.We have to change the formulation of the problem by consideringπs n=πmin as data,removingϕn from the cost function,and taking constraint(22)(d)for k=1to n−1only into account.Therefore(26)holds for k=1to n−1only.Example3(Special case3)Assume that bothπd0=πmin andπd n=πmin.Then inthe new formulation we have to combine the modifications of cases1and2.We are going to prove the following properties of an optimal pipeline system. Denote the set of sections with positive lengths byI L:={1≤i≤n;L i>0}.(29) Theorem1For the optimal number n of compressor stations,the only degenerate (withη0=0)solution of the necessary optimality conditions,is when all diameters have their maximal value,all suction(resp.discharge)pressures have their minimal (resp.maximal)value(except of course for the givenfinal discharge pressure),and if compressors are identical,all section lengths(except possibly for thefirst and last ones)are equal.Theorem2For the optimal number n of compressor stations,the nondegenerate (withη0=1)solutions of the necessary optimality conditions have the following structure:(i)Sections1to say k0have zero length(possibly with k0=0,i.e.,no section haszero length).If the model of compressors satisfies(6)and(15),then the com-pression ratiosρk,for k=1to k0,have the same valueˆρ.(ii)All sections have the same diameter,and sections k0+1to n−1have the same maximal discharge pressure.(iii)If the model of compressors satisfies(6)and(15),then sections k0+1to n−1 have the same suction pressureπs∗,and sections k0+2to n−1have the same positive length L∗.6Proof of the main resultsThe proof is based on a sequence of lemmas.We will not discuss the three special cases,for which the proof is a simple variant of the standard case.Wefirst discuss a degenerate case.Lemma2A degenerate critical point is such thatμ=0.Proof Assume on the contrary thatη0=μ=0.For1≤k≤n,by(24),λk=0if L k>0,andλk≥0if L k=0.Let us prove by contradiction thatηk=0,k=1,...,n. Assume on the contrary thatηk>0,for some1≤k≤n.Sinceλ≥0,(26)–(27)imply thatπs k=πmin,πd k=πmax.(30) We deduce thatπs k<πd k,contradictingηk>0.So we have proved thatη=0.We next prove thatλ=0.Assume on the contrary thatλk=0,for some1≤k≤n. Sinceη=0,by(24),L k=0,and hence by the drop equationπs k=πd k−1.We see that –when k=1,sinceπd0>πmin,we have thatπs1>πmin,in contradiction with(26) for k=1,–when k>1,sinceπs k=πd k−1,these two variables cannot both reach their bounds, in contradiction with(26)–(27)(the latter at index k−1).We have proved that(η,λ,μ)=0,therefore we must also have(u,v)=0,i.e.,all multipliers associated with bound constraints also must be zero.But this contradicts the definition of a generalized multiplier.Lemma3For any critical point,over sections with positive length,all diameters D k (resp.multipliersλk)have a constant value D∗(resp.λ∗),that satisfy−λ∗β(D∗)=η0αp−μD∗.(31)Proof Let k∈I L.Since L k has no upper bound,∂L∂L k=0,and hence,−λkβD k =η0αp−μD k.(32)Substituting this expression in(25),and settingδ(D k):=(L k)−1∂L∂D k,obtainδ(D k)=η0αp(1+σ)−σμD k.(33)This function does not depend on k,and cannot be identically zero since eitherη0>0 orμ=0by the previous lemma.Ifδ(D)is positive(negative)over(D min,D max),then all diameters are equal to some value Dη0,μ,equal to eitherπmin orπmax.Ifon the contraryδ(D)changes of sign over[D min,D max],thenη0>0,and then we may takeη0=1,μ>0,andδ(D)has a unique zero Dη0,μ:=σμ/(αp(1+σ)).In addition,δ(D)is an increasing function.In view of(13),it follows that whatever the value ofη0is,we have that D k=D η0,μ,whereD η0,μ=max(D min,min(Dη0,μ,D max)),(34)proving that all diameters are equal.That the same holds for theλk follows from(32). Remark1For all sections of positive length,since(24)equals zero,the multipliers λk have the same valueλ∗=(D η0,μ)σβ(μ−η0αp D η0,μ).(35)In particular,if the diameters are out of bound,thenλ∗=λk=αpσβσμ(σ+1)αp(σ+1),k∈I L.(36)The previous result has an important consequence.We may,and will do in the sequel of the paper,set the diameters of zero length sections to the same value as the one of positive sections.If two sections are separated by one or several non active compressors,since these sections have equal diameters,they can be viewed as a single section.We have proved the following:⎧⎨⎩For the optimal n,we may assume without loss of generalitythat all diameters are equal and that all compressors,exceptperhaps for the last one,are active.(37)So in the sequel we will assume that:πs k<πd k andηk=0,k=1,...,n−1.(38)Proof of Theorem1Assume thatη0=0.Thenμ=0by Lemma2.For k∈I L,in view of(24),we have thatλk=0,and by Lemma3its value is a positive constantλ∗over I L.Ifλ∗<0,then for k∈I L,k<n,(26)combined with(38)would imply that πs k attains its upper bound,which cannot happen since compressors are running.So λ∗>0,and alsoμ>0by(31).Consequently,for a section k of length zero,since∂L ∂L k ≥0,we also haveλk>ing(25)–(27),we obtain that for k∈I L,∂L∂D k<0,so that we may assume that diameters reach their maximal value in all sections,andfor any k,∂L∂πs k >0,and(if k≤n−1)∂L∂πd k−1<0,so that all suction(resp.discharge)pressures have their minimal(resp.maximal)value.The latter proves that all sections have a positive length.If compressors are identical,then by the drop equation,for 1<k<n,lengths are equal.The result follows. Soη0=0corresponds to the limiting case when,forfixed n,the maximum ofresources must be used in order to comply with the constraints.In the sequel we will assume thatη0=1in order to compute the nondegenerate solutions.Lemma4For any nondegenerate critical point,discharge pressures reach their maximal values for all sections of positive length(except perhaps for the last one):πd k=πmax,for all k∈I L,k<n.(39) In addition,any section of positive length is followed by a section of positive length (except perhaps for the last one).Proof Let k∈I L.Adding(26)and(27),we obtain for k<n∂L ∂πs k +∂L∂πk=1πs kϕ k(ρk)1−πd kπs k+λk−λk+1.(40)Since by(24),∂L∂L kin increasing w.r.t.λk,we have thatλk=λ∗≤λk+1,and hence, sinceϕ k(ρk)>0andπs k<πd k by(37),the r.h.s.of the above display is negative. Hence,at least one of the two partial derivatives is negative,which implies that one variable is at its upper bound.Sinceπs k<πd k≤πmax,we have that∂L∂πsk≥0.There-fore∂L∂πd k<0.This proves(39).If,for1<k<n,section k−1is of positive length and section k is of zero length,the latter has an active compressor with a maximal suction pressure,which is impossible.The result follows.So it is possible that sections say1to k0have zero length.We now study this situation.Lemma5Assume that sections1to k0have zero length(and not section k0+1).If the model of compressors satisfies(6)and(15),then the compression ratio is con-stant,for sections1to k0.Proof It suffices to check that,if k0≥2,thenρ1=ρ2.Set a i=(ρi)γ2/2and b= a1a2.Given b corresponding to the compression ratio over the twofirst sections,。
化工设备英文名称大全
化工设备英文名称大全目? ? 录? ?Contents1. 工艺设备Process Equipment 1. 塔Column 11.1.1. 板式塔和填料塔Plate Column and Packed Column 1. 液流型式Liquid – Flow Patterns 2. 泡罩（帽）塔盘Bubble Cap Trays 3. 浮阀塔盘Valve Trays 4. 筛板塔盘Sieve Trays 6. 穿流式塔盘和喷射型塔盘Dual – Flow Trays and Jet Trays 7. 塔盘的支承Supports of Tray 8. 塔底结构及重（再）沸器Bottom Structures and Reboilers 9 . 进料和抽出Feed and Draw – Off 10. 填料Packing 12. 液体分配（布）器，再分配（布）器及填料支持版Liquid Distributors, Redistributors and Support Plates 13. 塔附件??T ower Attachments 14. 楼梯（梯子）和平台Stair and Platform 15CO2吸收塔CO2 Absorber 16再生塔/CO2汽提塔Regenerator / CO2 Stripper 17造粒塔Prill Tower 18. （造粒塔）总图及造粒喷头组装图General Assembly and Prill-Spray Assembly 18. 造粒塔扒料机Prill tower Reclaimer 20. 反应器Reactor 22氨合成塔Ammonia Converter 22聚合釜Polymerizer 24电解槽Cell 26. 隔膜电解槽Diaphragm Cells 26. 水银电解槽Mercury Cells 27. 贮罐Storage Tanks 28浮顶罐Floating Roof Tanks 30. 浮顶型式??Floating Roof Types 32. 浮顶罐的密封形式??Seal Types of Floating Roof Tank 34内浮顶罐??Covered Floating Roof Tanks 35低温贮罐Refrigerated Storage Tanks 36. 蒸发器Evaporators 37. 换热器Heat Exchangers 38换热器的名称Nomenclature of Heat Exchanger 40. 换热器部件Components of Heat Exchanger 40. 固定端头盖（或管箱），壳体及后端头盖型式Types of Stationary Head, Shell and Rear End Head 42. 管板Tube sheets 43. 管子－管板连接，膨胀节及其他零件Tube-Tube Sheet Joints, Expansion Joints and Other Parts 44. 横向折流板和纵向折流板Transverse Baffles and Longitudinal Baffles 46套管式换热器和刮面式换热器Double-Pipe Heat Exchanger and Scraped-Surface Exchanger 47套管式纵向翅片换热器Double Pipe Longitudinal Finned Exchanger 48 板式换热器Plate-Type Exchangers 49蒸汽表面冷凝器，凝汽器Steam Surface Condensers 50空冷器，空气冷却器Air-Cooled Heat Exchangers 51. 空冷器的组合形式Bay Arrangements of Air-Cooled Heat Exchanger 52 . 管束和头盖（管箱）的典型结构Typical Construction of Tube Bundles and Headers 53. 空冷器的驱动装置Drive Arrangements for Air Cooler 54. 翅片Fins 55. 空冷器的温度控制Temperature Control of Air Cooler 56冷却塔，凉水塔（1）Cooling Towers(Ⅰ) 57冷却塔，凉水塔（2）Cooling Towers(Ⅱ) 58. 工业炉Furnace 60管式加热炉Pipe Heater 60. 管式加热炉型式Types of pipe Heaters (pipe Still Heater) 60 . 加热炉Heaters 62. 燃烧器，烧嘴Burners 63. 炉管，联管箱和回弯头Tube, Headers and Return Bends 64 . 管架Tube Supports 65转化炉Reformers (Reforming Furnaces) 66二段转化炉Secondary Reformer 67变换炉Shift Converter 68热回收和废热锅炉Heat Recovery and Waste Heat Boiler 69. 热回收Heat Recovery 69. CO燃烧废热锅炉CO Firing Waste Heat Boiler 70. 第一废热锅炉Primary Waste Heat Boiler 71. 第二废热锅炉Secondary Waste Heat Boiler 72火炬Flare Stacks 73. 混合设备Mixing Equipment 74搅拌器型式（1）Types of Agit ator(Ⅰ) 74搅拌器型式（2）Types of Agitator(Ⅱ) 76混合（搅拌）槽Mixing Tanks 77管道混合器Line Mixers (Flow Mixers) 78静止混合器Static Mixers 79膏状物料及粘性物料混（拌）合设备Paste and Viscous-Material Mixing Equipments 80固体混合机械Solids Mixing Machines 82双螺杆连续混合机Double Screw Continuous Mixer 83. 萃取器Extractors 84连续萃取设备，连续抽提设备Continuous Contact (DifferentialContact) Equipments 84浸提设备Leaching Equipments 86. 旋风分离器、沉清器、过滤器和离心机Cyclone, Decanter, Filter and Centrifuge 87旋风分离器（1）Cyclone Separators (Ⅰ) 87旋风分离器（2）Cyclone Separators (Ⅱ) 88气体洗涤器Gas Scrubbers 90沉降罐，澄清器Gravity Settlers (Decanters) 92过滤机Filter 93压滤机Pressure Filters 93叶滤机Pressure Leaf Filters 94袋式过滤器Bag Filters 95转鼓真空过滤机Rotary-Drum Vacuum Filter 96离心式分离机Centrifugal Separator 97. 双鼓真空离心过滤机Double-Bowl Vacuum Centrifuge 97. 离心机Centrifuges 98. 静止叶片型离心式分离器Stationary Vane Type Centrifugal Separators 100. 干燥器Dryers 101间接干燥器Indirect Dryers 101直接干燥器Direct Dryers 102喷雾干燥器Spray Dryers 104. 雾化喷头，喷雾嘴，雾化器Spray Nozzles (Atomizers) 105气流(气动)输送干燥器? ? Pneumatic Conveyor Dryers 106. 其他? ? Miscellaneous 107石油炼制中的流化过程? ? Fluidization Processes in Petroleum Refinery107. 流态化? ? Fluidization 108. 流化床分布器? ? Distributors for Fluidized Bed 109破沫器及其应用? ? Demister and Its Applications 110. 破沫网的安装和纤维除雾器? ? Installation of Mesh and Fiber Mist Eliminator 111设备的支座和封头? ? Supports and Heads of Equipments 112 立式容器的外部保温? ? External Thermal Insulation for Vertical Vessel 1132. 泵? ? Pump 114. 各种型式的泵(1) Various Types of P ump (Ⅰ) 114各种型式的泵(2) Various Types of Pump (Ⅱ) 116各种型式的泵(3) Various Types of Pump (Ⅲ) 117各种型式的泵(4) Various Type s of Pump (Ⅳ) 118. 离心泵(1)? ? Centrifugal Pump(Ⅰ) 119离心泵(2)? ? Centrifugal Pump(Ⅱ) 120离心泵(3)? ? Centrifugal Pump(Ⅲ) 121. 管道泵? ? Inline Pump 122. 双作用蒸汽往复泵? ? Duplex Acting Steam-Driven Reciprocating Pump 123 . 双作用活塞式往复泵? ? Double Action Reciprocating Pump, Bucket Type 124 . 混流泵??Mixed-Flow Pump 126. 计量泵? ? Metering Pumps 127. 喷射泵? ? Jet Pumps 128. 喷射装置? ? Ejector Units 129喷射器的结构? ? Ejector Structures 1303. 压缩机、鼓风机和风机? ? Compressors Blowers and Fans 131. 螺杆压缩机? ? Screw Compressors 131. 旋转式螺杆压缩机? ? Rotary Helical Screw Compressors 132 . 活塞式压缩机? ? Piston Compressors 133. 往复式压缩机? ? Reciprocating Compressors 134. 低密度聚乙烯(超)高压压缩机? ? High Pressure Compressor forLow Density Polyethylene Process 136高压气缸和中心型组合阀? ? High-Pressure Cylinder and Central Valve 138 卸荷阀并及其他阀? ? Unloading Valve and Other Valves 140. 水平剖分式离心压缩机? ? Horizontally Split Centrifugal Compressor 142 . 鼓风机，压气机? ? Blowers 144. 风机? ? Fans 146. 典型的空气压缩机装置? ? Typical Compressor Installation 1484. 输送机和提升机? ?Conveyor and Elevator 149. 垂直提升(输送)机? ? Vertical Elevator (Conveyor) 149斗式提升机? ? Bucket Elevator 149垂直提升输送机和箱类提升机? ? Vertical Rising Conveyor and Case Elevator 150双带提升机? ? Twin Riser 151. 带式输送机? ? Band (Belt) Conveyor 152带式输送机示意图? ? Band Conveyor Sketch 152输送机系统? ? Conveyor Systems 153带式输送机? ? Band Conveyor 154中心距超过600英尺的单轮传动带式输送机用的张紧装置? ? Take-up Unit for Single Drum Drive Belt Conveyor Exceeding 600 Feet Centers 155双轮传动带式输送机的张紧装置? ? Take-up Unit for Dual Drum Drive Belt Conveyor 156拼装式皮带运输机和移动式皮带运输机? ? Pre-built Sectional Belt Conveyor and Mobile Belt Conveyor 157. 螺旋输送机? ? Screw Conveyor 158. 吊挂式链输送机和振动输送机? ? Chain Trolley Conveyor and Vibrating Conveyor 159吊挂式链输送机部件? ? Units of Chain Trolley Conveyor 160. 辊子输送机? ? Roller Conveyors 162. 惰轮(托辊)型式? ? Types of Idlers 163托辊(惰轮)结构? ? Construction of Iders 1645. 破碎和筛分设备? ? Crushing and Screening Equipment 166. 颚式破碎机? ? Jaw crusher 166. 颚式冲击破碎机? ? Impact Jaw Crusher 168. 回转球形破碎机? ? Gyrasphere Crusher 169. 盘式回转破碎机? ? Tray Type Gyratory Crusher 170. 液压锥形破碎机和冲击式破碎机(叶片破碎机)? ? Hydraulic Cone Crusher and Impact Crusher (Impeller Breaker) 172 . 辊子粉碎机? ? Roller Mill 173. 双轴锤击破碎机? ? Double Shaft Hammer Mill 174. 球磨机? ? Ball Mill 176. 干燥粉磨机? ? Dryer-Pulveriser 177. 返混设备布置? ? Layout of Back mixing Equipment 178. 振动筛? ? Vibrating Screen 179. 分级机? ? Classifiers 1806. 塑料和橡胶加工成型机械? ???Forming Machine For Plastics and Rubber181. 挤压机? ? Extruder 181. 螺杆注塑机? ? Screw Injection Molding Machine 182. 聚氯乙烯辊压机生产线? ? Calender Line for PVC Production 183. 四辊辊压机? ? Four-Roll Calender 1847. 给料机，称量器和包装机? ? Feeder, Weighing and Bagging Machine 186 . 振动给料机? ? Vibrating Feeder 186. 电振动给料机? ? Electric Vibrating Feeder 188. 板式给料机? ? Apron Feeder 189. (粉末)均匀自动给料机? ? Smooth Auto-Feeder 190. 带式计量秤? ? Dosing Belt Weigher 191. 定量给料秤? ? Constant Feed Weigher 192. 自动装袋系统??Automatic Bagging System 1938. 汽轮机? ? Steam Turbine 194. 汽轮机的分类(1)? ? Classification of Steam Turb ines (Ⅰ) 194汽轮机的分类(2)? ? Classification of Steam Turbines (Ⅱ) 196. 汽轮机的循环? ? Steam Turbine Cycles 197. 汽轮机供汽方式? ???Methods of Steam Supply to a Turbine 198. 单级汽轮机? ? Single Stage Steam Turbine 199. 冲动式汽轮机? ? Impulse Turbines 200. 汽轮机轴封? ? Turbine Glands and Gland Sealings 202. 汽轮机的润滑? ? Lubrication of Steam Turbine 204. 汽轮机调速器及调速? ? Governors and Governing of Steam Turbine 206 . 汽轮机调速器??Turbine Governor 208. 超速脱扣装置(保安器)??Overspeed Tripping Device 210. 汽轮机的安装??Installation of Steam Turbine 2119. 锅炉??Boiler 212. 火管锅炉及水管锅炉的基本型式??Basic Patterns for Fire and Water Tube Boiler 212. 椭圆管板换热器??Ellipsoidal Shell and Tube Heat Exchanger 213. 水冷管夹套换热器??Cooling Tubes and Jacket Heat Exchanger 214. 蒸汽净化及锅筒内件(1)??Steam Purification and Drum Internals (Ⅰ) 215蒸汽净化及锅筒内件(2)??Steam Purification and Drum Internals (Ⅱ) 216蒸汽净化及锅筒内件(3)??Steam Purification and Drum Internals (Ⅲ) 218蒸汽净化及锅筒内件(4)??Steam Purification and Drum Internals (Ⅳ) 219 . 过热器??Superheater 220. 减温器??Attemperators 221. 空气预热器??Air Preheater 222. 炉排??Grates 224. 下饲炉排??Underfeed Stoker 225. 喷燃器，燃烧器??Burners 226. 省煤器??Economizer 228. 抛煤机??Spreader Feeders 229. 磨煤机??Pulverizers 23010. 机械零件??Machine Element 231. 万向节??FUniversal Joints 231. 联轴器??Couplings 232. 液力联轴器(1)??Fluid Couplings (Ⅰ) 234液力联轴器(2)??Fluid Couplings (Ⅱ) 235. 轴颈密封，圆周密封??Circumferential Seals 236. 端面密封，轴封，轴端连接件??Face Seals, Shaft Sealings and End Fittings 237. 滚子轴承，滚柱轴承??Roller Bearings 238. 球轴承，滚珠轴承 Ball Bearings 239. 加油机构??Oiling Devices 240. 紧固件??Fastener 241螺栓和双头螺柱??Bolts and Studs (stud bolts) 241螺钉的头部和端部型式??Heads and Points of Screw 242螺母??Nuts 243非螺纹紧固件??Non-threaded Fasteners 24411. 配管(管路)和管件??Piping and Fitting 245. 阀杆与阀盖结构??Valve Stem and Bonnet Designs 245. 阀门(1)??Valves(Ⅰ) 246阀门(2)??Valves(Ⅱ) 248阀门(3)??Valves(Ⅲ) 249阀门(4)??Valves(Ⅳ) 250. 闸阀??Gate Valve 251. 截止阀??Globe Valve 252. 球阀??Ball Valve 253. 止回阀??Check Valve 254. 弹簧安全泄压阀??Spring Safety-Relief Valve 255. 液面控制浮球阀??Pilot Operated Ball Float Valve 256. 波纹管密封闸门阀??Bellows Sealed Gate Valve 257. 热膨胀阀??Thermo Expansion Valve 258. 阀门操纵机构??Valve Operating Mechanisms 259. 蒸汽疏水阀(器)和空气疏水阀(器)??Steam Traps and Air Traps 260. 管道附件??Pipe Line Fitments 262. 法兰、法兰密封面及垫片??Flanges, Flange Facings and Gaskets 264. 填料??Packings 266. 管件??Pipe Fitting 267法兰管件??Flanged Fittings 267螺纹管件??Threaded Fittings 268钢焊接管件??Steel-Welding Fittings 269. 塑料压接管接头??Plastics Compression Joints 270. 预制弯管与膨胀节??Fabricated Pipe Bends and Expansion Joints 271. 管子连接??Joints in Tubing and Pipe 272. 管道绝热??Piping Insulation 273. 管吊与管支架??Pipe Hangers and Pipe Supports 274. 急救冲洗和洗眼站??Safety Shower and Eyewash Station? ?? ?? ?Hose??Station??软管站 27612. 量测仪表??Instrumentation 277. 液位(面)计??Level Gage 277就地安装直读液面计??Locally Mounted Direct Reading Level Gages 277 浮筒式液面计??Displacement Type Level Gages 278液面调节器及液位开关??Level Controllers and Switches 279. 压力测量仪表??Pressure Instruments 280液体压力计??Manometers 282压力测量的新成果??New Developments in Pressure Measurements 283压力表的安装??Installation of Pressure Guage 284. 流量测量元件??Flow Measuring Element 285速率式流量计??Inferential Meters① (Fluid Velocity Meter) 285 . 涡轮流量计??Turbine Meter 285. 漩涡流量计??Vortex flow meter 286. 漩涡流量计测量系统??Vortex Flow meter Measurement System 287一次流量元件??Primary Flow Elements 288容积式流量计??Positive Displacement Type Flow Meters 290 可变面积(定压降)式流量计??Variable Area Type Flow Meters 292差压流量计的安装? ?Installation of Head Meters 294面积式流量计及计量泵??Area Meters and metering pumps 296其他流量计(1)??Other Flow Meters(Ⅰ) 297其他流量计(2)??Other Flow Meters(Ⅱ) 298. 温度计??Thermometer 299热电偶??Thermocouple 299液体膨胀温度计及双金属温度计??Liquid Expansion and BimetallicThermometer 300电阻式温度计及热敏电阻??Resistance Thermometer and Thermistor 302 压力式温度计??Filled System Thermometer 303 辐射高温计??Radiation Pyrometer 304光学高温计??Optical Pyrometer 305电动指示调节器??Electritic Indicating Controller 306气动指示调节器??Pneumatic Indicating Controller 307多点长图温度记录仪??Multi-Point Long Chart Temperature Recorder 308 控制操作箱??Control Station 309记录纸??Charts 310. 变送器??Transmitter 311压力变送器??Pressure Transmitter 311差压变送器??Differential Pressure Transmitters 312气动温度变送器??Pneumatic Temperature Transmitter 314物位变送器??Level Transmitters 315. 调节(控制)器??Controller 316液位调节器??Liquid Level Controller 316气动调节器??Pneumatic Controller 317弹簧管调节器??Bourdon Tube Controller 318. 调节阀??Control Valve 319薄膜及活塞执行机构??Diaphragm and Piston Actuators 320调节阀阀盖??Bonnets of Control Valve 321调节阀阀体(1)??Control Valve Bodies (Ⅰ) 322调节阀阀体(2)??Control Valve Bodies (Ⅱ) 323阀芯及笼式阀芯??Valve plugs and Cages 324阀内组件(组成)部分??Components Valve Trim① 325调节阀的作用及导向??Acting and Guiding of Control Valve 326调节阀定位器??Positioner of Control Valve 327调节阀手动机构??Handjack Assembly of Control Valve 328气动活塞定位器??Pneumatic Piston Positioner 329. 氧分析器??Oxygen Analysis Equipment 330. 二氧化碳分析器??Carbon Dioxide Analyzer 332. PH计??pH meters 333. 粘度测量仪表??Viscosity Measuring Instruments 334. 比重仪表??Specific Gravity Instrument 336. 速度测量与控制??Speed Measurement and Control 337. 仪表盘??Instrument Panels 338. 温度控制??Temperature Control 340. 信号系统 Annunciators Systems 341集中式信号器??Integral Annunciators 342分离式信号器及半模拟式信号器??Remote Annunciator and Semigraphic Annunciator 343. 继动器??Relays 344. 仪表管件及仪表箱??Instrumentation Tube Fittings and Housings 346. 仪表图例符号及名称??Instrumentation Symbols and Identifications 348 . 总体分散控制系统(1)??Total Di stributed Control System(Ⅰ) 350. 总体分散系统(2)??Total Distributed Control System(Ⅱ) 351 . 总体分散系统(3)??Total Distribu ted Control System(Ⅲ) 352 . 总体分散系统(4)??Total Distributed Control System(Ⅳ) 353 . 总体分散系统(5)??Total Distributed Control System(Ⅴ) 354 . 总体分散系统(6)??Total Distributed Control System(Ⅵ) 35513. 电气工程??Electrical Engineering 356. 旋转电机??Electrical Rotating Machine 356直流电机??Direct-Current Machine 356直流发电机??Direct-Current Generator 357AC换向电机??AC Commutator Machine 358交流电动机??Alternating-Current Motor 359滑环式感应电动机??Slip-ring Type Induction Motor 360无刷同步电动机??Brushless Synchronous Motor 362同步电动机的无刷励磁??Brushless Excitation of Synchronous Motor 363 线槽和绕组??Slots and Windings 364. 变压器??Transformer 365油浸式变压器正视图??Oil Immersed Transformer Front View 365油浸式变压器侧视图??Oil Immersed Transformer Side View 366油浸式变压器外视图??Oil Immersed Transformer Exterior 367 . 整流器和电池??Rectifier and Battery 368整流器??Rectifier 368原电池(1)??Primary Batteries(Ⅰ) 369原电池(2)??Primary Batteries(Ⅱ) 370. 高压开关装置??High Voltage Switchgear 372金属封闭式开关装置??Metal-Enclosed Switchgear 372金属高压开关柜??Metal-Clad High-Voltage Cubicle 373六氟化硫断路器??SF6 Circuit-Breaker 374T型断路器??T-Breaker 376电动机操纵机构??Motor Drive 377. 低压开关??Low-Voltage Switches 378限流空气断器??Currentt-Limiting Air-Break Circuit-Breaker 378塑料外壳断路器??Moulded Case Circuit-Breaker 379控制开关??Control Switches 380. 按钮开关??Pushbutton Switches 382. 凸轮旋转开关??Cam Switches 384. 电磁设备??Electromagnetic Apparatus 386电磁机构和器件??Electromagnetic Mechanism and Devices 386电磁继电器??Electromagnetic Relays 388电压调整继电器??Voltage Regulating Relay 390. 电气防爆??Electrical Explosion-proof 391危险场所内的电力和照明安装??Power and Lighting Installation in Hazardous Location 391防爆设备??Explosion-proof Apparatus 392. 供电系统??Power Supply System 394热电厂??Thermal Power Plant 394. 节能发电厂??Energy Saving Power plant 396变电所屋内配电装置??Indoor Installations of Electric Substation 398 铁塔及电杆??T owers and Poles 399静电除尘器??Electrostatic Precipitator 400. 内线??Interior Wiring 401电缆??Cables 401熔断器??Fuses 404连接器和端子??Connectors and Terminals 406灯泡??Lamps 407电热器件??Electroheating Devices 40814. 施工设备和工具??Construction Equipment and Tool 409. 起重机械??Hoisting Machinery 409桅杆起重机，转臂起重机??Derricks 409安装起重机??Erecting Cranes 410起重设备??Hoisting Devices 412起重机(1)??Cranes(Ⅰ) 413起重机(2)??Cranes(Ⅱ) 414起重机(3)??Cranes(Ⅲ) 415手拉葫芦和千斤顶??Chain Hoists and Jacks 416麻绳，钢丝绳，绳结和吊索??Hemp Ropes, Cable Wires, Knots and Sling Chains 418起重机用的起吊附件??Lifting Attachments for Crane Use 420 叉式起重车的附属配件??Fork-Truck Attachments 421. 工具??Tools 422扳手??Wrenches 422活扳手及管钳??Adjustable Wrenches and Pipe Wrenches 423 钳和剪钳??Pliers and Nippers 424刀具的柄部、套节及套筒??Shanks, Sockets and Sleeves 425丝锥??Taps 426绞刀??Reamers 427麻花钻??Twist Drills 428木工工具??Wood Working T ools 429检测规??Inspection Gages 430量具??Measuring T ools 43115. 焊接??Welding 432. 金属焊接??Welding of Metals 432. 焊接符号??Welding Symbols 434. 保护式电弧焊原理??Principles of Shielded Arc Welding 435 . 焊接位置、接头形式及焊接形式??Welding Positions, Types of Joints and Welding 436. 坡口??Grooves 437. 坡口详图??Detail of Grooves 438. 焊接缺陷??Defects of Welding 439. 填角焊，角焊??Fillet Welding 440. 自动埋弧焊??Automatic Submerged Arc Welding 441. 气体保护电弧焊??Gas-Shielded Arc Welding 442. 金属极楕性气体保护焊??Gas Metal-Arc welding 444. 金属极气体保护焊焊枪? ?Electrode Guns of Gas Metal-Arc Welding 445 . 普通电渣焊??Conventional Electroslag Welding 446 . 熔嘴电渣焊??Electroslag Welding by Consumable Guide Tube 447. 电气焊??Electrogas Welding 448. 管状焊丝电弧焊??Flux-Cored Arc Welding 450. 气焊设备??Gas Welding Equipment 451. 移动式乙炔发生器??Portable Acetylene Generators 452. 乙炔发生器的基本型式??Basic Types of Acetylene Generators 453. 塑料焊接(1)??Welding of Plastics(Ⅰ) 454塑料焊接(2)??Welding of Plastics(Ⅱ) 45516. 无损检验??No-Destructive Testing 456. 无损检验方法??Non-Destructive Testing Method 456. 探孔镜及显微镜??Borescope and Microscope 458. X射线发生管及其线路??X-ray Tube and Its Circuit 459. 射线照相及电子照相??Photoradiography and Electroradiography 460. 轻便X射线机及透度计??Mobile X-ray Unit and Penetrometer 461. 超声波探伤方法及探头??Ultrasonic Test Methods and Search Units 462 . 超声波发射探头及接受探头??Ultrasonic Transducer and Refraction 463 . 配管焊缝的超声波探伤??Ultrasonic T esting of Weld in Tubing 464. 液体渗透试验??Liquid Penetrant Test 465. 磁化法??Methods of Magnetization 46617. 土建工程??Civil Engineering and Building 467. 地形图和土层剖面图??Topographical Map and Subsoil Profile 467. 土壤与基础??Soils and Foundations 468. 桩的形式??Types of Pile 469. 设备基础??Foundations for Equipment 470. 大型设备的锚固(1)??Anchorage of Heavy Machine(Ⅰ) 471大型设备的锚固(2)??Anchorage of Heavy Machi ne(Ⅱ) 472. 道路和路面??Road and Paving 473. 屋顶的形式??Types of Roof 474. 薄壳屋顶??Shell Roofs 475. 钢筋混凝土结构??Reinforced Concrete Construction 476. 钢结构??Steel Construction 478钢结构连接详图??Structural Steel Connection Details 480钢构件的连接??Connection of Steel Members 481钢栏杆??Steel Balustrade 482钢扶梯和梯子??Steel Stairs and Ladders 483. 多层工业厂房??Multistory Industrial Buildings 484. 门的形式??Types of Doors 485. 窗的形式??Types of Windows 486窗的组成??Components of a Window 487. 工业构筑物??Industrial Structures 488管支架??Pipe Supports 488烟囱的形式??Types of Chimneys 490排气筒??Vent Stacks 491水塔的形式??Types of Water Towers 492冷却塔??Cooling T owers 493通廊和栈桥??Galleries and Trestles 494筒仓和贮斗??Silos and Bunkers 49518. 实验室仪器??Laboratory Apparatus and Instruments 496. 实验室常用仪器(1)??General Apparatus a nd Instruments(Ⅰ) 496实验室常用仪器(2)??General Apparatus and Instruments(Ⅱ) 498. 石油产品的蒸馏??Distillation of Petroleum Products 499. 粘度计??Viscometer 500. 比重天平，韦氏天平??Specific Gravity Balance (Westphal Balance) 501 . 闪点和燃点测定器??Flash and Fire Points Apparatus 502. 残碳及含水量??Carbon Residue and Water Content 503. 冰点，凝点和融点??Freezing Point, Pour Point and Melting Point 504 . 脆裂点，针入度及软化点??Breaking Point, Cone penetration and Softening Point 505. 吸附柱??Absorption Column 50619. 流程图和管道布置图??Flow Diagram and piping Layout 507. 工厂平面布置总图??Master Plot Plan 507. 炼厂加工流程图(1)??Diagrammatic Flow Sheet of Petroleum Ref inery(Ⅰ) 508炼厂加工流程图(2)??Diagrammatic Flow Sheet of Petroleum Refinery(Ⅱ) 510 . 合成氨装置工艺流程图??Ammonia Plant Process Flow Diagram 512. 乙烯装置工艺流程图??Ethylene Plant Process Flow Diagram 514. 管道布置-装置配管??Piping Layout-Installation Piping 516. 配管图，管道(路)图??Piping Drawing 517平面视图??Plan View 517前视图??Front View 518. 管道组装图(等角图，轴侧图，管段图)??Pipe Line Isometric Diagram (Erection Diagram) 519. 蒸汽伴热管的布置??Piping Arrangement of Steam Tracing Lines 520. 工艺管道及仪表流程图??Process Piping and Instrument Flow Diagram 521 管道代号??Piping Code 521管道图例??Line Symbols 522在仪表符号中字母标志的意义Meanings of Identification Letters in Instrument Symbols 524绘图示例-氨库装置??Illustrative Drawing-Ammonia Storage Facility 525 . 工程图常用缩写词 (按字母顺序排列) Abbreviations for Use on Drawings (in Alphabetical Order) 52620. 其他??Miscellaneous 536. 型钢，管子??Steel Sections, Pipes and Tubes 536. 钢管的制造方法??Manufacturing Methods of Steel Pipe 538 参考文献??Reference 539。
压力容器与管道安定性分析与评估方法进展
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井间ERT电极阵列优化及监测实验系统设计与开发
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