隨機方向法減速器優(yōu)化設(shè)計【單級圓柱齒輪減速器】【P=10KW n=960r-min i=5】【說明書+CAD+SOLIDWORKS】
隨機方向法減速器優(yōu)化設(shè)計【單級圓柱齒輪減速器】【P=10KW n=960r-min i=5】【說明書+CAD+SOLIDWORKS】,單級圓柱齒輪減速器,P=10KW n=960r-min i=5,說明書+CAD+SOLIDWORKS,隨機方向法減速器優(yōu)化設(shè)計【單級圓柱齒輪減速器】【P=10KW,n=960r-min,i=5】【說明書+CAD+SOLIDWORKS】,隨機
隨機方向法齒輪減速器優(yōu)化設(shè)計
學(xué)生姓名： 周馳 班級：0781051
指導(dǎo)老師：朱保利
摘要：齒輪減速器優(yōu)化設(shè)計。設(shè)計理念及方法包括很多，有傳統(tǒng)方法一般需要經(jīng)過調(diào)查分析、方案擬定、技術(shù)設(shè)計、零件工作圖繪制等環(huán)節(jié)，初步訂出一個設(shè)計方案，對齒輪的模數(shù)、齒數(shù)、尺寬、螺旋角以及傳動比等取作設(shè)計變量進行優(yōu)化設(shè)計，然后進行驗算。但用這種方法設(shè)計出的減速器往往尺寸偏大或者只是某一條件的最優(yōu)化，這可能并不是最優(yōu)的設(shè)計方案，使許多工程問題懸而未決。
本文對單機圓柱齒輪減速器優(yōu)化設(shè)計是對單機圓柱齒輪減速器的體積最小優(yōu)化設(shè)計。主要問題包括齒輪傳動的優(yōu)化設(shè)計既可以成為多目標函數(shù)問題，故對多方面的的條件都考慮了，比如強度、剛度、穩(wěn)定性等性能分析計算。這主要是利用邊界約束和性能約束使得單機圓柱齒輪減速器的體積最小。
根據(jù)論文要求，本文采用采用隨機方向法，以體積最小為目標進行減速器優(yōu)化設(shè)計。單機圓柱齒輪減速器優(yōu)化設(shè)計包括建立優(yōu)化設(shè)計問題的數(shù)學(xué)模型和隨機方向法優(yōu)化方法與程序兩方面的內(nèi)容。數(shù)學(xué)模型一旦建立，減速器最小體積問題就變成一個數(shù)學(xué)求解問題。隨機方向法隨機方向法是一種原理簡單的直接解法，它的優(yōu)點是對目標函數(shù)的性態(tài)無特殊要求，程序計算，使用方便。通過計算機軟件（frotran語言）編程，調(diào)試，運行，最后得出6個參考數(shù)據(jù)得到的減速器最小體積，理論上應(yīng)該比常規(guī)計算的最小體積要小，而此時最小體積也是最優(yōu)化結(jié)果，并且用三維軟件SolidWorks設(shè)計畫圖。
關(guān)鍵詞：優(yōu)化設(shè)計 隨機方向方法 齒輪減速器 3維設(shè)計
指導(dǎo)老師簽名：
Optimal Design of gear reducer random method
Student name：zhou Chi Class：0781051
Supervisor: Zhu Baoli
Abstract: For optimum design of gear decelerator The major methods of the study traditionally include investigation, program planning, technical design and working drawing, etc. Generally speaking, designers combine personal experience and materials collected in order to get a preliminary design by the traditional methods, optimizing variables like modulus, number, square wide, helical angle and transmission ratio of the gear and checking in the end. However, decelerators designed via the traditional methods are often of bigger size and conditionally work, leaving many practical engineering problems unsettled.
The main aim of the article is to study the method to minimize the size of the single column-shaped gear decelerator. The article centers on boundary constraints and performance constraints，and considers assorted conditions of the decelerators like intensity, rigidity and stability, etc, to settle the problems of Multi-objective functions。
According to the requirement of paper, this paper using random direction method, with the target of smallest Volume to optimization design of gear reducer. The optimize design of single cylindrical gear reducer include the mathematical model of optimal design problem and random direction optimization method and procedure. Once established mathematical model, Minimum volume reducer become a mathematical solving problem. Random direction method is a simple direct solution principle whose advantage is no special requirements on the characteristic of objective function, program calculation, and easy to use. Through the computer software (frotran Software) Programming, debugging and running and finally reached six reference data of minimum volume gear reducer, theoretically, the volume should be smaller than the conventional calculation, and the minimum volume is the optimal result.
Keyword: Optimal Design random direction method gear reducer 3D design
Signature of Supervisor:
畢業(yè)設(shè)計（論文）任務(wù)書
I、畢業(yè)設(shè)計(論文)題目：隨機方向法減速器優(yōu)化設(shè)計
II、畢 業(yè)設(shè)計(論文)使用的原始資料(數(shù)據(jù))及設(shè)計技術(shù)要求：
1、原始數(shù)據(jù)：
單級圓柱齒輪減速器，已知輸入功率P=10kW，輸入轉(zhuǎn)速n1=960r/min，傳動比i=5，
工作壽命15年，每年工作300天。
2、設(shè)計技術(shù)要求：
1）采用隨機方向法，以體積最小為目標進行減速器優(yōu)化設(shè)計；
2）與常規(guī)設(shè)計結(jié)果進行比較分析；
3）繪制減速器裝配圖及主要零件圖。
III、畢 業(yè)設(shè)計(論文)工作內(nèi)容及完成時間：
1. 收集資料、開題報告、外文翻譯 2.16-3.08
2. 建立優(yōu)化設(shè)計的數(shù)學(xué)模型 3.09-3.22
3．編寫優(yōu)化設(shè)計程序、計算 3.23-4.18
4. 減速器常規(guī)設(shè)計計算、結(jié)果分析 4.18-4.28
5. 繪制減速器裝配圖及主要零件圖 4.28-5.24
6. 撰寫畢業(yè)設(shè)計論文 5.25-6.01
Ⅳ 、主 要參考資料：
1 璞良貴，紀名剛主編.機械設(shè)計.第八版.北京：高等教育出版社，2007
2 孫靖民主編.機械優(yōu)化設(shè)計.第三版.北京：機械工業(yè)出版社，2005
3 方世杰，綦耀光主編.機械優(yōu)化設(shè)計.北京：機械工業(yè)出版社，1997.2
4 王昆等主編. 機械設(shè)計課程設(shè)計手冊.北京：機械工業(yè)出版社，2004
5 Carrol, R., and Johnson, G.,“Optimal design of compact spur gear sets”, ASME Journal of mechanisms, transmissions and automation in design. Vol.106, No.1, March 1984, pp.95-101
航空工程 系 機械設(shè)計制造及自動化 專業(yè)類 0781051 班
學(xué)生（簽名）
日期： 自 2011 年 2 月 16 日 至2010年 6 月 1 日
指導(dǎo)教師（簽名）：
助理指導(dǎo)教師(并指出所負責(zé)的部分)：
航空工程 系主任（簽名）：
附注:任務(wù)書應(yīng)該附在已完成的畢業(yè)設(shè)計說明書首頁。
南昌航空大學(xué)科技學(xué)院學(xué)士學(xué)位論文
前 言
優(yōu)化設(shè)計是60年代初發(fā)展起來的一門新學(xué)科，它是將最優(yōu)化原理和計算機技術(shù)應(yīng)用于設(shè)計領(lǐng)域，為工程設(shè)計提供一種重要的科學(xué)設(shè)計方法。利用這種新的設(shè)計方法，人們就可以從眾多的設(shè)計方案中尋找最佳設(shè)計方案，從而大大提高設(shè)計效率和質(zhì)量。因此優(yōu)化設(shè)計是現(xiàn)代設(shè)計理論和方法的一個重要領(lǐng)域，它已廣泛應(yīng)用于各個工業(yè)部門。在緒論中僅對機械優(yōu)化設(shè)計的特點、發(fā)展概況、本門課程的主要內(nèi)容作一簡要介紹。
減速器的設(shè)計，一般需要經(jīng)過調(diào)查分析、方案擬定、技術(shù)設(shè)計、零件工作圖繪制等環(huán)節(jié)。傳統(tǒng)設(shè)計方法通常在調(diào)查分析的基礎(chǔ)上，參照同類產(chǎn)品通過估算、經(jīng)驗類比或試驗來確定初始設(shè)計方案。然后，根據(jù)初始設(shè)計方案的設(shè)計參數(shù)進行強度、剛度、穩(wěn)定性等性能分析計算，檢查各性能是否滿足設(shè)計指標要求。如果不完全滿足性能指標的要求，設(shè)計人員將憑借經(jīng)驗或直觀判斷對參數(shù)進行修改。這樣反復(fù)進行分析計算-性能檢驗-參數(shù)修改，直到性能完全滿足設(shè)計指標的要求為止。整個傳統(tǒng)設(shè)計過程就是人工試湊合定性分析比較的過程，主要的工作是性能的重復(fù)分析，至于每次參數(shù)的修改，僅僅憑借經(jīng)驗或直觀判斷，并不是根據(jù)某種理論精確計算出來的。實踐證明，按照傳統(tǒng)設(shè)計方法作出的設(shè)計方案，大部分都有改進提高的余地，而不是最佳設(shè)計方案。
現(xiàn)代化的設(shè)計工作已不再是過去那種憑借經(jīng)驗或直觀判斷來確定結(jié)構(gòu)方案，也不是像過去“安全壽命可行設(shè)計”方法那樣：在滿足所提出的要求的前提下，先確定結(jié)構(gòu)方案，再根據(jù)安全壽命等準則，對該方案進行強度、剛度等的分析、校核，然后進行修改，以確定結(jié)構(gòu)尺寸。而是借助電子計算機，應(yīng)用一些精確度較高的力學(xué)的數(shù)值分析方法（如有限元法等）進行分析計算，并從大量的可行設(shè)計方案中尋找出一種最優(yōu)的設(shè)計方案，從而實現(xiàn)用理論設(shè)計代替經(jīng)驗設(shè)計，用精確計算代替近似計算，用優(yōu)化設(shè)計代替一般的安全壽命的可行性設(shè)計。
優(yōu)化方法不僅用于產(chǎn)品結(jié)構(gòu)的設(shè)計、工藝方案的選擇，也用于運輸路線的確定、商品流通量的調(diào)配、產(chǎn)品配方的配比等等。目前，優(yōu)化方法在機械、冶金、石油、化工、電機、建筑、宇航、造船、輕工等部門都已得到廣泛的應(yīng)用。
本設(shè)計采用優(yōu)化設(shè)計的方法（隨機方向法）對單級圓柱齒輪減速器體積進行優(yōu)化，通過優(yōu)選小齒輪齒數(shù)，充分提高各級齒輪的承載能力，并使高速級和低速級達到等強度來對單級圓柱齒輪減速器進行優(yōu)化設(shè)計。
由于時間比較緊張，準備不充分，使得設(shè)計可能存在一些問題，希望能得到各位老師和同學(xué)的批評與指正！
學(xué)士學(xué)位論文原創(chuàng)性聲明
本人聲明，所呈交的論文是本人在導(dǎo)師的指導(dǎo)下獨立完成的研究成果。除了文中特別加以標注引用的內(nèi)容外，本論文不包含法律意義上已屬于他人的任何形式的研究成果,也不包含本人已用于其他學(xué)位申請的論文或成果。對本文的研究作出重要貢獻的個人和集體，均已在文中以明確方式表明。本人完全意識到本聲明的法律后果由本人承擔(dān)。
作者簽名： 日期：
學(xué)位論文版權(quán)使用授權(quán)書
本學(xué)位論文作者完全了解學(xué)校有關(guān)保留、使用學(xué)位論文的規(guī)定，同意學(xué)校保留并向國家有關(guān)部門或機構(gòu)送交論文的復(fù)印件和電子版，允許論文被查閱和借閱。本人授權(quán)南昌航空大學(xué)可以將本論文的全部或部分內(nèi)容編入有關(guān)數(shù)據(jù)庫進行檢索，可以采用影印、縮印或掃描等復(fù)制手段保存和匯編本學(xué)位論文。
作者簽名： 日期：
導(dǎo)師簽名： 日期：
南昌航空大學(xué)科技學(xué)院學(xué)士學(xué)位論文
畢業(yè)設(shè)計（外文翻譯）
題 目： 隨機方法減速器優(yōu)化設(shè)計
專業(yè)名稱： 機械設(shè)計制造及其自動化
班級學(xué)號：
學(xué)生姓名：
指導(dǎo)教師：
二〇一一 年 三 月
Effects of structure elastic deformations of wheelset and track on creep forces of wheel/rail in rolling contact
Xuesong Jin, Pingbo Wu, Zefeng Wen
National Traction Power Laboratory, Southwest Jiaotong University, Chengdu 610031, PR China
Abstract: In this paper the mechanism of effects of structure elastic deformations of bodies in rolling contact on rolling contact performance is briefly analyzed. Effects of structure deformations of wheelset and track on the creep forces of wheel and rail are investigated in detail. General structure elastic deformations of wheelset and track are previously analyzed with finite element method, and the relations, which express the structure elastic deformations and the corresponding loads in the rolling direction and the lateral direction of wheelset, respectively, are obtained. Using the relations, we calculate the influence coefficients of tangent contact of wheel and rail. The influence coefficients stand for the occurring of the structure elastic deformations due to the traction of unit density on a small rectangular area in thecontact area of wheel/rail. They are used to revise some of the influence coefficients obtained with the formula of Bossinesq and Cerruti in Kalker’s theory of three-dimensional elastic bodies in rolling contact with non-Hertzian form. In the analysis of the creep forces, the modified theory of Kalker is employed. The numerical results obtained show a great influence exerted by structure elastic deformations of wheelset and track upon the creep forces.
? 2002 Elsevier Science B.V. All rights reserved.
Keywords: Wheel/rail; Rolling contact; Creep force; Structure elastic deformation
1. Introduction
During running of a train on track the fierce action between wheelset and rails causes large elastic deformations of structure of wheelset and track. The large structure deformations greatly affect performances of wheels and rails in rolling contact, such as creep forces, corrugation [1–3], adhesion, rolling contact fatigue, noise [4,5] and derailment [6]. So far rolling contact theories widely used in the analysis of creep forces of wheel/rail are based on an assumption of elastic half space [7–12]. In other words, the relations between the elastic deformations and the traction in a contact patch of wheel/rail can be expressed with the formula of Bossinesq and Cerruti in the theories. In practice, when a wheelset is moving on track, the elastic deformations in the contact patch are larger than those calculated with the present theories of rolling contact. It is because the flexibility of wheelset/rail is much larger than that of elastic half space. Structure elastic deformations (SED) of wheelset/rail caused by the corresponding loads are shown in Figs. 1 and 2. The bending deformation of wheelset shown in Fig. 1a is mainly caused by vertical dynamic loads of vehicle and wheelset/rail. The torsional deformation of wheelset described in Fig. 1b is produced due to the action of longitudinal creep forces between wheels and rails. The oblique bending deformation of wheelset shown in Fig. 1c and the turnover deformation of rail shown in Fig. 2 are mainly caused by lateral dynamic loads of vehicle and wheelset/rail. The torsional deformations with the same direction of rotation around the axle of wheelset (see Fig. 1d), available for locomotive, are mainly caused by traction on the contact patch of wheel/rail and driving torque of motor. Up to now very few published papers have discussions on the effects of the SED on creepages and creep forces between wheelset and track in rolling contact.
In fact, the SED of wheelset/rail mentioned above runs low the normal and tangential contact stiffness of wheel/rail. The normal contact stiffness of wheel/rail is mainly lowed by the subsidence of track. The normal contact stiffness lowed doesn’t affect the normal pressure on the contact area much. The lowed tangential contact stiffness affects the status of stick/slip areas and the traction in the contact area greatly. If the effects of the SED on the rolling contact are taken into account in analysis of rolling contact of wheel/rail, the total slip of a pair of contacting particles in a contact area is different from that calculated with the present rolling contact theories. The total slip of all the contacting particles and the friction work are smaller than those obtained under condition that the SED is ignored in the analysis of creep forces of wheel/rail. Also the ratio of stick/slip areas in a contact area is larger than that without consideration of the effects of the SED.
In this paper the mechanism of effects of structure elastic deformations of bodies in rolling contact on rolling contact performance is briefly analyzed, and Kalker’s theoretical model of three-dimensional elastic bodies in rolling contact with non-Hertzian form is employed to analyze the creep forces between wheelset and track. In the numerical analysis the selected wheelset and rail are, respectively, a freight-car wheelset of conical profile, China “TB”, and steel rail of 60 kg/m. Finite element method is used to determine the SED of them. According to the relations of the SED and the corresponding loads obtained with FEM, the influence coefficients expressing elastic displacements of the wheelset and rail produced by unit density traction acting on the contact area of wheel/rail are determined. The influence coefficients are used to replace some of the influence coeffi- cients calculated with the formula of Bossinesq and Cerruti in Kalker’s theory. The effect of the bending deformation of wheelset shown in Fig. 1a and the crossed influences among the structure elastic deformations of wheelset and rail are neglected in the study. The numerical results obtained show marked differences between the creep forces of wheelset/rail under two kinds of the conditions that effects of the SED are taken into consideration and neglected.
2. Mechanism of reduced contact stiffness increasing the stick/slip ratio of contact area
In order to make better understanding of effects of the SED of wheelset/track on rolling contact of wheel/rail it is necessary that we briefly explain the mechanism of reduced contact stiffness increasing the ratio of stick/slip area in a contact area under the condition of unsaturated creep-force. Generally the total slip between a pair of contact particles in a contact area contains the rigid slip, the local elastic deformation in a contact area and the SED. Fig. 3a describes the status of a pair of the contact particles, A1 and A2, of rolling contact bodies and without elastic deformation. The lines, A1A_1 and A2A_2 in Fig. 3a, are marked in order to make a good understanding of the description. After the deformations of the bodies take place, the positions and deformations of lines, A1A_1 and A2A_2, are shown in Fig. 3b. The displacement difference, w1, between the two dash lines in Fig. 3b is caused by the rigid motions of the bodies and (rolling or shift). The local elastic deformations of points, A1 and A2, are indicated by u11 and u21, which are determined with some of the present theories of rolling contact based on the assumption of elastic-half space, they make the difference of elastic displacement between point A1 and point A2, u1 = u11 ? u21. If the effects of structure elastic
deformations of bodies and are neglected the total slip between points, A1 and A2, can read as: S1 = w1 ? u1 = w1 ? (u11 ? u21) (1) The structure elastic deformations of bodies and are mainly caused by traction, p and p_ acting on the contact patch and the other boundary conditions of bodies and , they make lines, A1A_1 and A2A_2 generate rigid motions independent of the local coordinates (ox1x3, see Fig. 3a) in the contact area. The u10 and u20 are used to express the displacements of point A1 and point A2, respectively, due to the structure elastic deformations. At any loading step they can be treated as constants with respect to the local coordinates for prescribed boundary conditions and geometry of bodies and . The displacement difference between point A1 and point A2, due to u10 and u20, should be u0 = u10 ? u20. So under the condition of considering the structural elastic deformations of bodies and , the total slip between points, A1 and A2, can be written as: S?1 = w1 ? u1 ? u0 (2) It is obvious that S1 and S?1 are different. The traction (or creep-force) between a pair of contact particles depends on S1 (or S?1 ) greatly. When |S1| > 0 (or |S?1 | > 0) the pair of contact particles is in slip and the traction gets into saturation. In the situation, according to Coulomb’s friction law the tractions of the above two conditions are same if the same frictional coefficients and the normal pressures are assumed. So the contribution of the traction to u1 is also same under the two conditions. If |S1| = |S?1 | > 0, |w1| in (2) has to be larger than that in (1). Namely the pairs of contact particles without the effect of u0 get into the slip situation faster than that with the effect of u0. Correspondingly the whole contact area without the effect of u0 gets into the slip situation fast than that with the effect of u0. Therefore, the ratios of stick/slip areas and the total traction on contact areas for two kinds of the conditions discussed above are different, they are simply described with Fig. 4a and b. Fig. 4a shows the situation of stick/slip areas. Sign in Fig. 4a indicates the case without considering the effect of u0 and indicates that with the effect of u0. Fig. 4b expresses a relationship law between the total tangent traction F1 of a contact area and the creepage w1 of the bodies. Signs and in Fig. 4b have the same meaning as those in Fig. 4a. From Fig. 4b it is known that the tangent traction F1 reaches its maximum F1max at w1 = w_1 without considering the effect of u0 and F1 reaches its maximum F1max at w1 = w_1 with considering the effect of u0, and w_1 < w__ 1 . u0 depends mainly on the SED of the bodies and the traction on the contact area. The large SED causes large u0 and the small contact stiffness between the two bodies in rolling contact. That is why the reduced contact stiffness increases the ratio of stick/slip area of a contact area and decreases the total tangent traction under the condition of the contact area without full-slip.
3. Calculation of structure deformation of wheelset/rail
In order to calculate the SED described in Fig. 1b–d, and Fig. 2, discretization of the wheelset and the rail is made. Their schemes of FEM mesh are shown in Figs. 5, 7 and 9. It is assumed that the materials of the wheelset and rail have the same physical properties. Shear modulus: G = 82,000 N/mm2, Poisson ratio: μ = 0.28. Fig. 5 is used to determine the torsional deformation of the wheelset. Since, it is symmetrical about the center of wheelset (see Fig. 1b), a half of the wheelset is selected for analysis. The cutting cross section of the wheelset is fixed, as shown in Fig. 5a. Loads are applied to the tread of the wheelset in the circumferential direction, on different rolling circles of the wheel. The positions of loading are, respectively, 31.6, 40.8 and 60.0 mm, measured from the inner side of the wheel. Fig. 6 indicates the torsional deformations versus loads in the longitudinal direction. They are all linear with loads, and very close for the different points of loading. The effect of the loads on the deformation of direction of y-axis, shown
in Fig. 5a, is neglected.
Parameters of contact geometry of wheelset/rail to be used in the latter analysis read as:
ri =ri(y,ψ)
δi = δi(y,ψ)
?i = ?i(y,ψ)
ai = ai(y,ψ)
hi = hi(y,ψ)
z = z(y,ψ)
φ = φ(y, ψ) (3)
where i = 1, 2 stand for the left and right side w
heels/rails, respectively. The parameters in (3) are defined in detail in the Nomenclature of the present paper.We define thaty > 0
when the wheelset shifts towards the left side of track and ψ > 0 if it is inclined, in the clockwise direction, between the axis of wheelset and the lateral direction of track pointing to the left side. The parameters depend on the profiles of wheel and rail, y and ψ. But if profiles of wheel and rail are prescribed they mainly depend on y [7]. Detailed discussion on the numerical method is given in [7,8] and results of contact geometry of wheel/rail.
When a wheelset is moving on a tangent track the rigid creepages of wheelset and rails read as [8]:
[7]
[8]
where i = 1, 2, it has the same meaning as subscript i in (3). The undefined parameters in (4) can be seen in the Nomenclature. It is obvious that the creepages depend on not only the parameters of contact geometry, but also the status of wheelset motion. Since the variation of the parameters of contact geometry depend mainly on y with prescribed profiles of wheel/rail some of their derivatives with respect to time can be written as
Putting (5) into (4), we obtain:
In the calculation of contact geometry and creepage of wheel/rail, the large ranges of the yaw angle and lateral displacement of wheelset are selected in order to make the creepage and contact angle of wheel/rail obtained include the situations producing in the field as completely as possible. So we select y = 0, 1, 2, 3, . . . , 10 mm, ψ = 0.0, 0.1, 0.2, 0.3, . . . , 1.0?, ˙ y/v = 0, 0.005 and r0 ˙ ψ/v = 0, 0.001. ?ri?y, ?φ/?y and ??i/?y are calculated with center difference method and the numerical results of ri , φ and ?i versus y. l0 = 746.5mm, r0 = 420mm.Using the ranges of y, ψ, ˙ y/v and r0 ˙ ψ/v selected above we obtain that ξ i 1 ranges from ?0.0034 to 0.0034, ξ i 2 ranges from ?0.03 to 0.03, ξ i 3 ranges from ?0.00013 to 0.00013 (mm?1), and contact angle δi is from to 2.88 to 55.83?. Due to length limitation of paper the detailed numerical results of creepage and contact geometry are not shown in this paper.
4. Conclusion
(1) The mechanism of effects of structure elastic deformation of the bodies in rolling contact on rolling contact performance is briefly analyzed. It is understood that the reduced contact stiffness of contacting bodies increases the stick/slip area of a contact area under the condition that the contact area is not in full-slip situation.
(2) Kalker’s theoretical model of three-dimensional elastic bodies in rolling contact with non-Hertzian form is employed to analyze the creep forces between wheelset and track. In the analysis, finite element method is used to determine the influence coefficients expressing elastic displacements of wheelset/rail produced by unit traction acting on each rectangular element, which
are used to replace some of the influence coefficients calculated with the formula of Bossinesq and Cerruti in Kalker’s theory. The numerical results obtained show the differences of the creep forces of wheelset/rail under two kinds of conditions that effects of structure elastic deformations of wheelset/rail are taken into consideration and neglected.
(3) The structure elastic deformations of wheelset and track run low the contact stiffness of wheelset and track, and reduce the creep forces between wheelset and track remarkably under the conditions of unsaturated creep force. Therefore, the situation is advantageous to the reduction of the wear, rolling contact fatigue of wheel and rail.
(4) In the study the effect of the bending deformation of wheelset shown in Fig. 1a is neglected, and the crossed influence coefficients AIiJj(i _= j ; i, j = 1, 2) are
not revised. So, the accuracy of the numerical results obtained is lowed. In addition, when the lateral displacement of center of the wheelset, y > 10mm, the flange action takes place. In such situation the contact angle is very large and the component of the normal load in the lateral direction is very large. The large lateral force causes track and wheelset to produce large structure deformations, which affect the parameters of contact geometry of wheel/rail and the rigid creepages. Therefore, the rigid creepages, the creep forces, the parameters of contact geometry, the SED and the motion of wheelset have a great influence upon each other. It is necessary that they are synthetically put into consideration in the analysis. Numerical results of them can be obtained with an alternative iterative method. Probably conformal contact or two-point contact between wheel and rail take place during the action of flange. Such phenomenon of wheelset and rails in rolling contact is very complicated, and can be analyzed with a new theory of rolling contact, which may be a FEM model including effects of structure deformations and all boundary conditions of wheelset and track in the near future.
This work was supported by the Natural Science Foundation Committee of China that grant the key research project: “Corrugation of Contact Surface of Wheel and Rail and Rolling Contact Fatigue” (59935100) to the National Traction Power Laboratory, Southwest Jiaotong University. It is also supported by the Foundation for University Key Teacher by the Ministry of Education of China.
References
[1] K. Knothe, S.L. Grassie, Modeling of railway track and vehicle/track interaction at high frequencies, Vehicle Syst. Dynam. 22 (3/4) (1993) 209–262.
[2] K. Hempelmann, K. Knothe, An extended linear model for the prediction of short pitch corrugation, Wear 191 (1996) 161–169.
[3] W.F. Hayes, H.G. Tucker, Wheelset–track resonance as a possible source of corrugation wear, Wear 144 (1991) 211–226.
[4] P.J. Remington, Wheel–rail noise. Part IV. Rolling noise, J. Sound Vibrat. 46 (1975) 419–436.
[5] D. Thompson, Wheel–rail noise generation, J. Sound Vibrat. 161 (Part 3) (1993) 387–482.
[6] V.G. Krivonogov, V.S. Lysyuk, S.N. Sharapov. Critical displacement of the rail head under action of wheels, in: Proceedings of the conference IHHA, June 14–17 1999, Moscow, Russia, pp. 537–540.
[7] F.W. Carter, On the action of a locomotive driving wheel, Proc. R. Soc. Lond. A 112 (1926) 151–157.
[8] J.K. Vermeulen, K.L. Johnson, Contact of non-spherical bodies transmitting tangential forces, J. Appl. Mech. 31 (1964) 338–340.
[9] J.J. Kalker. On the rolling contact of two elastic bodies in the presence of dry friction, Ph.D. thesis, Delft University, The Netherlands, 1967, pp. 64–100.
[10] J.J. Kalker. Simplified Theory of Rolling Contact, Delft Progress Report, Delft University Press, The Netherlands, 1973, pp. 1–10.
[11] J.J. Kalker. Three-Dimensional Elastic Bodies in Rolling Contact, Kluwer Academic Publishers, The Netherlands, 1990.
[12] Z.Y. Shen, J.K. Hedrick, J.A. Elkins. A comparison of alternative creep-force models for rail vehicles dynamic analysis, in: Proceedings of the Eighth IAVSD Symposium, Cambridge, MA, 1984, pp. 591–605.
[13] S. Guo, C. Cai, W. Zhai. A study of lateral coupling dynamics of vehicle/track system, J. China Railway Soc. Suppl. (1994) 91–98 (in Chinese).
[14] W. Wei, A model of rail track receptance analysis, J. Dalian Railway Inst. 19 (4) (1998) 33–38 (in Chinese).
[15] S.L. Grassie. Benchmark test for model of railway track and of vehicle/track interaction at relative high frequencies, Vehicle Syst. Dynam. 24, Suppl. (1995) 355–362.
[16] X. Jin, W. Zhang, Analysis of creepages and their sensitivities for a single wheelset moving on a tangent track, J. Southwest Jiaotong Univ. 20 (2) (1996) 128–136.
[17] X Jin. Study on creep theory of wheel and rail system and its experiment, Ph.D. thesis, Southwest Jiaotong University, Chengdu, China, 1999, pp. 39–53 (in Chinese).
輪輻的柔性變形結(jié)構(gòu)的效果和在滾動接觸的輪/ 軌道的潛變力的追蹤
金學(xué)松 吳平博 文澤峰
中國 成都 600031 西南交通大學(xué) 國家的牽引動力實驗室
摘錄:在這一篇論文中，對滾動接觸機械裝置上的滾動接觸體結(jié)構(gòu)柔性變形的效果簡短地分析。輪副和軌道對輪的潛變力的結(jié)構(gòu)變形的效果和軌條詳細地被分析研究。輪副的一般結(jié)構(gòu)柔性變形和軌道首先分別用
收藏