Stress and Displacement Distributions on Cylindrical Roller Bearing Rings Using FEM^#

Optimization of operating conditions for a double-row tapered roller bearing

“…Despite the obvious advantages of using the FEM, there are some disadvantages when this method is applied to design mechanical components, such as convergence problems, due to the adjustment of the mesh size, especially if the FE model includes mechanical contacts. It is well known that if the contact surface between the bodies is limited and the mesh size is large, the number of nodes in that contact surface will be reduced and the calculation of contact stresses will not be accurate (Zhang et al 2003;Demirhan and Kanber 2008). Thus, it is concluded that the FEM is not an appropriate method to use in design and optimization processes if a considerable number of FE simulations are required and the FE models includes nonlinearities.…”

“…The FE models are assembled from a combination of elements with 8 and 6 nodes formulated in linear shape functions. The coefficient of friction between the hub and the inner raceway is considered to be 0.2, whereas the coefficient between the rollers and the inner raceway and between the rollers and the outer raceway is considered to be 0.001 (Demirhan and Kanber 2008). Raceways and rollers are modeled using linear elastic and isotropic steel with a Young's modulus (E) equal to 208 GPa and a Poisson's ratio (m) of 0.29.…”

An extensive review of vibration modelling of rolling element bearings with localised and extended defects

“…[43,44] to predict the vibration 156 frequencies produced by a single point defect and multiple (two) point defects within a rolling element f bpi in the absence of a radial load; however, in its presence, a response is also generated at equi-spaced on the waviness of raceways and rolling elements [87,. However, from the review of the literature 289 conducted during the course of this paper, it appears that the first nonlinear multi-body dynamic model 290 for predicting the vibration response of a rolling element bearing (in a bearing-pedestal system), due to 291 a localised (point) defect, was reported in 2002 by Feng et al [53]. Their model was an extension to the 292 model developed by Fukata et al [40] that describes the vibration response of an ideal (non-defective) ball 293 bearing.…”

“…As for the case of implicit models [281][282][283][284][285][286][287][288][289][290][291][292][293][294][295][296][297], explicit FE models for non-defective rolling element bearings 596 have also been developed [300][301][302][303]. These models simulate deep-groove ball bearings, and compare the 597 numerically estimated stress distribution results, obtained using LS-DYNA [298], at the rolling element-to-598 raceway contact interfaces, with the analytical results obtained using the classical Hertz theory of elasticity 599 [134][135][136].…”

“…For the case of non-defective rolling element bearings, a number of researchers [281][282][283][284][285][286][287][288][289][290][291][292][293][294][295][296][297] have conducted 570 FE modelling studies using the aforementioned software packages to investigate the following static pa-571 rameters -stresses at the rolling element-to-raceway contact interfaces, rolling element-to-raceway contact 572 forces, load-deflection relationships, load carrying capacity of rolling elements, stiffness matrix calculation, 573 and fatigue life. As the models in references [281][282][283][284][285][286][287][288][289][290][291][292][293][294][295][296][297] do not include a defect within the bearing models, 574 they are not directly relevant to the current paper, and therefore, are not reviewed here.…”