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南昌航空大學科技學院學士學位論文 輪輻的柔性變形結(jié)構的效果和在滾動接觸的輪/ 軌道的潛變力的追蹤 金學松 吳平博 文澤峰 中國 成都 600031 西南交通大學 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)構變形的效果和軌條詳細地被分析研究。輪副的一般結(jié)構柔性變形和軌道首先分別用有限元的機械要素方法和關系一起分析,從而獲得表達滾動方向和輪副的橫方向的結(jié)構柔性變形和對應的負載。按照它們之間的關系,我們計算輪和軌條的在一點相接接觸的影響力系數(shù)。影響力系數(shù)代表發(fā)生在輪/軌道接觸的一個小的矩形面積上的單位面積的牽引力引起的結(jié)構柔性變形。他們習慣校訂一些與Kalker的無赫茲的形狀滾動接觸的三維空間的有柔性體的理論 Bossinesq 和 Cerruti 的公式一起獲得的影響力系數(shù)。在潛變力的分析中, 利用了修正的 Kalker 的理論。從輪副和軌道的結(jié)構柔性變形中獲得的數(shù)字結(jié)果表明潛變力發(fā)揮的很大影響力。 2002 Elsevier 科學出版社版權所有。 關鍵字: 輪/軌條; 滾動接觸;潛變力;柔性變形結(jié)構 1.介紹 由于火車輪副和軌道之間的很大相對運動作用力引起輪副和軌道的結(jié)構較大的柔性變形。大的結(jié)構變形極大影輪和軌條響滾動接觸的性能,如潛變力，波形 [1 – 3] ，黏著，滾動接觸疲勞, 噪音 [4,5] 和脫軌[6]等等. 到現(xiàn)在為止在輪/ 軌道的潛變力的分析中廣泛應用的滾動接觸理論是以柔性一半的空間假定為基礎的 [7 – 12]. 換句話說，輪/ 軌道的一個接觸的柔性變形和牽引之間的關系可以用Bossinesq 和 Cerruti 的理論公式表達。實際, 當輪副在軌道上持續(xù)運動,接觸的柔性變形是比那些以滾動接觸的現(xiàn)在理論公式計算的更大。因為輪副/ 軌道的撓性是比柔性一半的空間更加大 。由對應的負荷所引起的輪副/ 軌道柔性變形結(jié)構在圖中被顯示。如 1 和 2. 在圖中輪副彎曲變形被顯示出來。在圖 1a 中被顯示的輪副彎曲變形主要由車輛和輪副/軌條的垂直動載荷所引起。在圖 1 b 中描述的輪副扭轉(zhuǎn)的變形是由于輪和軌道之間的縱潛變力的作用生產(chǎn)的。在圖 1 c 中顯示的輪副斜角彎曲變形和在圖 2 中顯示的軌道翻折變形主要地由交通工具和輪副/軌道的橫動態(tài)負荷所引起。在輪副 (圖 1 d) 的軸周圍的和旋轉(zhuǎn)裝置相同方向的扭轉(zhuǎn)變形,火車可以使用的,主要在電動機的輪/ 軌條和驅(qū)動扭矩的接觸補綴上的牽引所引起。到目前為止很少的出版物討論滾動接觸的輪副和軌道之間的爬動和潛變力的效果。 事實上，上面提到輪副/ 軌道的柔性變形結(jié)構是在輪/軌道的常態(tài)和切線的接觸剛性以下運動。輪/ 軌道的正常的接觸點的剛性通常低于軌道的下沉位置。 低于正常接觸點的剛性很少的影響接觸面積上的正常壓力。那低于切線的接觸剛性很大影響接觸面積的黏結(jié)/ 滑移面積狀態(tài)和牽引力。如果滾動接觸的柔性變形結(jié)構的影響被對于輪/軌道的分析考慮進去，一對接觸面積的全體微粒滑移與用現(xiàn)在滾動接觸理論計算的結(jié)果不同。所有的連絡顆粒和摩擦功的總的滑移比那在分析輪/軌道淺動力的時候，被忽略的柔性變形結(jié)構更小。同樣一個接觸面積的根/ 轉(zhuǎn)差面積的比率比沒有考慮的柔性變形結(jié)構的效果更大。在這一篇論文中，在滾動接觸性能上的滾動接觸的車體柔性變形機構的裝置被簡短地分析，而且和Kalker''''s 無赫茲的形狀滾動接觸的三度空間的有柔性車體的理論模型用來分析在輪副和軌道之間的潛變力。在數(shù)值分析中挑選的輪副和軌條分別地,是貨車輪副的錐形輪廓，中國 "兆位元組" 和鋼軌條的質(zhì)量是60 公斤/m 。有限元分析方法用來決定他們的柔性變形結(jié)構。依照柔性變形結(jié)構的關系和對應的由于 FEM 獲得負荷, 表示輪副的柔性變位的影響系數(shù)是由輪/ 軌條的接觸單位面積密度有所反應的牽引生產(chǎn)的軌條所決定。這些影響系數(shù)用來代替一些與 Kalker''''s 的理論 Bossinesq 和 Cerruti 的公式一起計算的影響系數(shù)。在圖 1a 中被顯示的輪副彎曲變形的效果和在輪副軌道的柔性變形結(jié)構之中的橫斷的影響力在研究中被疏忽。獲得的數(shù)字結(jié)果表明在輪副/軌道柔性變形結(jié)構的潛變力效果考慮和疏忽的條件之間的顯著差別。 2. 減少連絡剛性機構增加接觸面積的根粘滯/滑動比 為了要使輪副/ 軌道關于滾動接觸的輪/ 軌的的柔性變形結(jié)構的效果較好的理解, 我們必需簡短地解釋減少的接觸剛性的機構增加在沒有飽和的潛變力的狀態(tài)下面的接觸面積的粘滯/ 滑移面積的比。通常在一個接觸面積的一對接觸顆粒之間的總的滑移含有剛性的滑移,局部一個接觸面積和柔性變形結(jié)構的柔性變形。圖 3 a一描述一對滾動接觸車體①和沒有柔性變形②接觸顆粒， A1 和 A2 的狀態(tài) 。在圖 3 a中的線A1A 1 和 A2A 2, 為了要作描述的讓大家接受而被作記號。在車體的形變發(fā)生之后,線的位和形變,A1A 1 和 A2A2,在圖 3 b 中被顯示。位移差別 , w1, 在圖 3 b 的二個劃線之間由車體的剛性運動①和②所引起(滾動或變化). 局部點 A1 和 A2 的柔性變形,被 u11 和 u21 指示,與基于有柔性- 半份空間的假設滾動接觸的一些現(xiàn)代的理論一起決定,他們有差別在于點 A1 和點A2之間的有柔性位移 u1= u11- u21。如果車體的結(jié)構柔性變形的效果和被忽視的A1 和 A2點之間的總轉(zhuǎn)差 , 能用公式: S1 = w1 ? u1 = w1 ? (u11 ? u21) 表示。柔性變形結(jié)構車體 1 和 2 主要地由牽引力所引起,p 和 p 代表接觸插線和車體的其他邊界條件1和 2,他們做線,A1A 1 和 A2A 2 產(chǎn)生與接觸面積的局部的坐標 (ox1x3,圖 3 a) 無關的剛性運動。u10 和 u20 用來表達點 A1 和點A2的位移,各自歸于結(jié)構柔性變形。在任何的荷載階段他們?yōu)橐?guī)定的邊界條件和車體 1 和 2 的幾何學可能被當做有不防礙局部的坐標常數(shù)。在點 A1 和點 A2 之間的位移差別取決于 u10 和 u20, 應該是 u0= u10-u20。如此在考慮車體 1 和 2的柔性變形結(jié)構的條件之下,在點之間的總滑移 , A1 和 A2,同樣地用公式:S*1 = w1 - u1 - u0表示。明顯的 S1 和 S?1 是不同的。在一對接觸顆粒之間的牽引 ( 或潛變力)非常仰賴 S1( 或 S?1) 。當 |S1|>0(或 |S?1|>0)那對接觸顆粒是在滑移中和牽引力進入飽和。在進入飽和的情形中, 依照庫倫摩擦定律的如果一樣的磨擦力系數(shù)而且正常的壓力被假定的二個條件，牽引是相同的。如此對 u1 的牽引影響在二個條件之下也是相同的。如果 |S1|=|S?1|>0,|w1| 在 (2) 必須是比在(1)更大。即沒有 u0 的影響的那對接觸顆粒比有 u0 的影響的滑移更快。相應地沒有 u0 的影響整個的接觸面積進入滑移情況快于有 u0 的影響。因此，在接觸面積上的粘滯/ 滑移面積的比率和在上面被討論的二個類型的總牽引是不同的,他們只是被圖 4a 和 b一起被簡單描述。圖 4a表明粘滯/ 滑移面積的情況。圖 4a 的號訊 1 表明不考慮 u0 和 2的效果而指示外殼 即用 u0 的效果指示。圖 4 b表示在接觸面積上總的接觸牽引力F1和車體的滑動關系的一種規(guī)律。在圖 4 b 中的號訊 1 和 2 和圖 4 中的意義相同。從圖 4 b 中已知 , 在一點相接牽引力 F1 在 w1=w 時到達它的最大值 F1max 不考慮 u0 和 F1 接觸的效果在 w1=w 它的最大 F1max 僅由于 u0 的效果來看w1< w 1. u0 主要仰賴于車體的柔性變形結(jié)構和在接觸面積上的牽引力。大的柔性變形結(jié)構引起滾動接觸的在二個車體之間的大 u0 和小的接觸剛性。那是為什么增加一個接觸面積的根/ 滑移面積的比率和減少沒有全滑移的在接觸面積的條件下面的全體的牽引力而減少的接觸剛性。 3. 輪副/軌條的結(jié)構形變的計算 為了要計算在圖 1 b – d, 和圖 2 中被描述的柔性變形結(jié)構，輪副的離散化而且軌條被虛構。他們的 FEM 網(wǎng)目的方案 在圖 5,7 和 9中被顯示。假定輪副和軌條有相同的物理性質(zhì)。剪[切]模量:G=82,000個牛頓/mm2,泊松比: μ =0.28. 圖 5 用來決定輪副的扭轉(zhuǎn)形變。因為,它是關于輪副 (圖 1 b) 的中心對稱,一個一半的輪副被選擇來分析。輪副的切斷橫斷面被安裝,如圖 5 所示一。負荷被應用到圓周方向輪副的胎面,在輪的不同的母圓上。荷載的分布分別位于從輪的內(nèi)部邊測量31.6,40.8 和 60.0毫米, 圖 6 表示縱方向扭轉(zhuǎn)的形變相對于負荷位置。他們都是線性載荷，載荷的不同點都非常接近。在圖 5 中被顯示Y軸方向形變的的負荷被忽略。 i=1,2 分別代表左邊和右邊的邊輪/軌條。叁數(shù) (3) 在現(xiàn)在的論文命名中被詳細地義。如果它被傾斜，當輪副向軌道和ψ >0 的左邊變檔的時候 ,在順時針方向,在輪副的軸線和左邊的軌道的橫向方向之間，我們定義那 y>0。叁數(shù)仰賴y 和ψ，輪和軌條的輪廓。但是如果輪和軌條的輪廓被指定他們主要地仰賴 y[16]. 詳細的討論用數(shù)字的方法被屈服[16,17] 和輪/軌條的接觸幾何學的結(jié)果。 當一個輪副移動到一個正切追蹤剛性蠕動輪副和軌條的時候當做 [17]: i=1,2時它有如同寫在底下在(3)的 i 一樣的意義。在 (4)的不明確的叁數(shù)能在命名法中看到。很明顯蠕動不僅與接觸幾何學的叁數(shù)有關, 而且也與輪副運動的狀態(tài)有關。因為接觸幾何學的叁數(shù)變化主要依靠一些他們的導出于計時輪/ 軌條的規(guī)定輪廓y的變化有關被記做： 把(5)放進(4)之內(nèi)我們獲得: 在輪/軌條的接觸幾何學和滑移的計算，大范圍的偏角和輪副的橫向位移被選用以便輪輻的滑移和接觸角含盡可能完全地在磁場中被產(chǎn)生的情況被獲得。因此我們選擇 毫米 和 與中央的用不同的方法和ri, φ和 ?i 和 y l0=746.5mm ， r0=420mm比較的數(shù)字結(jié)果一起計算。使用選擇的y ，ψ，˙ y/ v 和 r0 ˙ψ/ v 的范圍在我們獲得上面ξ i 1個范圍從 ?0.0034 到 0.0034,ξ i 2個范圍從 ?0.03 到 0.03, ξ i 3 排列從 ?0.00013 到 0.00013(毫米?1), 和接觸角δ i 是從到 2.88 到 55.83度。由于論文的長度限制滑動和接觸幾何學的詳細數(shù)字的結(jié)果不被在這篇論文中顯示。 4．結(jié)論 (1). 在滾動接觸性能上的滾動接觸車體的柔性變形結(jié)構的效果機構被簡短地分析。一般了解連絡車體的接觸剛性減少則接觸面積在不全滑移情形中的粘滯/ 滑移面積增加。 (2). Kalker''''s 的和無赫茲的形狀滾動接觸的三度空間的彈性體的理論模型被用來分析在輪副和軌道之間的潛動力。在分析中，有限元法被用決定作用于每個矩形元件單位牽引生產(chǎn)的輪副/軌道有柔性位移表達的影響系數(shù),用來代替一些與 Kalker''''s 的理論 Bossinesq 和 Cerruti 的公式一起計算的影響系數(shù)。被獲得的數(shù)字結(jié)果表明在輪副/ 軌條結(jié)構柔性變形的效果被考慮和忽略的兩種情況之下輪副/ 軌條類型的潛動力的差別。 (3). 輪副和軌道的柔性變形結(jié)構低于運行輪副和軌道的接觸剛性, 而且在沒有飽和的潛動力的條件之下顯著地減少在輪副和軌道之間的潛動力。因此，這種情況有利于減少磨損和輪與軌條的滾動接觸疲勞。 (4).在研究中，在圖 1 中顯示的輪副彎曲形變的因素被忽略,而橫斷的影響系數(shù) 不被修正。因此，獲得數(shù)字結(jié)果的精確度很低。除此之外, 當輪副中心的橫向位移, y>10 mm,凸圓作用發(fā)生。在如此的情形中，接觸角非常大，而且橫的方向正常負載的元件也非常大。大的橫力引起軌道和輪副產(chǎn)生大的結(jié)構形變,影響輪/ 軌條的接觸幾何學的叁數(shù)和剛性的滑動。因此,剛性滑動,潛動力, 接觸幾何學的叁數(shù)，柔性變形結(jié)構和輪副的運動彼此有很大的影響。他們必需綜合地分析考慮。他們的數(shù)字結(jié)果能與一個其它可能的迭代法一起獲得 。或許共形的接觸或輪和軌條之間的點接觸在凸圓的作用期間發(fā)生。滾動接觸的輪副和軌條的現(xiàn)象是非常復雜的, 而且可能與可能是包括結(jié)構形變和包括輪副和軌道的所有邊界條件在不久的將來內(nèi)的效果 FEM 模型的滾動接觸的一個新的理論被分析。 這一個工作被研究計劃的中國自然的科學基礎委員會支持了: 輪和軌條和滾動接觸疲勞的接觸表面的波形。(59935100)國家牽引動力實驗室,西南交通大學 它也被中國的教育部鍵老師大學也提供基金支持。 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 coeffici