Shock and Vibration
Volume 2019 (2019), Article ID 3956169, 10 pages
https://doi.org/10.1155/2019/3956169

Research Article

Effect of Surface Morphology on Dynamic Characteristics of Cam-Follower Oblique Impact System

Wangqun Deng,¹ Haibo Feng,2,3 Jianjun Wang,² and Yongfeng Yang2,4

¹AECC Hunan Aviation Powerplant Research Institute, Zhuzhou 412002, China
²Institute of Vibration Engineering, Northwestern Polytechnical University, Xi’an 710072, China
³AECC Sichuan Gas Turbine Establishment, Mianyang 621000, China
⁴Key Laboratory of Vibration and Control of Aero-Propulsion System Ministry of Education, Northeastern University, Shenyang 110819, China

Correspondence should be addressed to Yongfeng Yang; yyf@nwpu.edu.cn

Received 4 December 2018; Accepted 27 December 2018; Published 22 January 2019

Academic Editor: Francesco Franco

Copyright © 2019 Wangqun Deng et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

Abstract.

The effects of the fractal characteristics on the dynamic characteristics of the oblique impact system are studied via considering the normal contact stiffness with fractal dimension parameter of the microstructure of the interface in this paper. The normal distribution is used to describe the trend of contact line length. The effects of the position parameters and the scale parameters are analyzed. The simulation results show that the increasing of the interface roughness can make the system response more stable. The system response eventually evolves into chaos as the fractal dimension increases. The system response changes between quasiperiod and chaos affected by the contact line length with a normal random distribution.

1. Introduction

Mechanical systems are usually modeled as multibody systems with nonsmoothness. Typical examples are the vibration and noise produced in engines, impact print hammers, railway brakes, or chattering of machine tools. These effects are due to the nonsmooth characteristics such as impacts, clearances, intermittent contacts, dry friction, unbalances, crack, or a combination of these effects [1–5]. In nonsmooth systems, the time evolution of displacements and velocities is not requested to be smooth. Especially for the impact, the velocities are even allowed to undergo jump at certain time instances in order to fulfill the kinematical restrictions.

Cam-follower devices are very important in impacting systems and widely applied in actual engineering systems. The rotation of the cam at special constant speed provides the force to operate the follower. The most common example is the valve train of the internal combustion engine. The cam rotation imparts force through the follower to the engine valve, while a spring provides the restoring force necessary to maintain contact between the two components [6, 7].

The impact on the cam-follower is a typical oblique impact. By using nonsmooth dynamics, oblique impact on rough bodies with an unsymmetrical configuration can result in self-locking or “jam” at the sliding contact if the coefficient of friction is large enough [8]. It has been observed that, under the variation of the cam-follower system parameters, the responses may exhibit complex behaviors including bifurcations and chaos [9, 10]. For example, Zhang [11] designed a new experimental device to verify the vibration suppression of a cantilever beam bond with a piezoelectric actuator by an adaptive controller. Ding et al. [12, 13] investigated the convergence of the Galerkin method of an elastic beam resting on a nonlinear foundation with viscous damping subject to a moving concentrated load. Alzate [14, 15] shows that a sudden transition to chaos is observed in an experimental cam-follower by ignoring the tangential friction effect. Considering the effect of tangential friction, Sundar et al. [16] studied the linear response of a cam-follower. In addition, the normal contact stiffness is an important parameter affecting the dynamic characteristics of the contact between the cam and follower when considering the surface topography [17]. In traditional research, the stiffness of the impact system is mostly studied as a deterministic linear or nonlinear stiffness. However, the mechanical roughness of the surface topography may affect the wear, friction, and contact deformation, which make the stiffness no longer determined [18]. Majumdar and Bhushan [19] found that the mechanical processing surface has self-similar fractal characteristics and proposed the contact fractal theory and the contact fractal model (MB model), which uses the fractal dimension D and the fractal dimension parameter G to characterize the mechanical roughness of the surface topography.

The contact of the cam-follower system consists of a round bar and a cam, which subject to the two intersecting cylindrical contact model. When the two parts contact, the contact surface is equivalent to an ellipse and the length of the contact line is equal to the length of the ellipse’s long axis. During the operation of the cam-follower system, the length of contact line is constantly changing due to the continuous change of the contact force between the follower and cam. Therefore, the length of the contact line should be dynamically changed in the actual analysis.

The motivation of this paper is to establish the normal contact stiffness model based on the contact fractal theory via considering the fractal dimension D and the fractal dimension parameter G. Normal distribution will be used to describe the variation of the contact line length. The effects of the normal contact stiffness on the dynamic characteristics of the oblique impact system are studied.

2. Mechanical Model and Dynamic Equation

2.1. System Description

Figure 1 shows the schematic diagram of the cam-follower system. The follower makes a fixed axis rotation around . The cam rotates around a fixed point , R is the radius, and is the rotating angular velocity of the cam. The eccentric is the distance between the geometric center and the rotation point . The angular displacement of the cam is , and the angle between the follower and the horizontal axis is At the initial time, A is the cam and follower contact point. When the system is rotating, and are the impact points on the follower and cam, respectively. is a local coordinate system, and note as the distance , which indicates the deformation of contact springs between the follower and cam. Obviously, the size of the can be used to determine whether the impact occurs or not, that is, indicates the separate state, and indicates the contact state.

Figure 1: Schematic diagram of the cam-follower system.

2.2. The Equation of Motion

During the operation of the cam, the follower will show two kinds of motion states, namely, the contact state and the separate state, and the topology of the system will change with time.

Using the Lagrangian approach, the follower motion equation can be obtained:

where is the follower’s moment of inertia, is the friction factor between follower and cam, and is the normal contact force, and the expression is

where and represent the equivalent stiffness and damping coefficient of the normal contact, respectively.

Using the pure damping model which was proposed by Padmanabhan [20], the given damping coefficient is

where is the impact damping factor.

2.3. Impact Law

In this model, the impact time is very short, the displacement of the various parts is constant, and the speed changes before and after the impact. By ignoring the plastic characteristic, the oblique impact problem studied here only involves the elastic impact. Considering the impact recovery coefficient, the impact process is divided into two stages: compression and recovery. The velocity relationship before and after the impact is

where is the coefficient of impact recovery and and are given by the following expressions:

2.4. Normal Contact Stiffness Fractal Model

The contact stiffness is related to the material properties of the two contacting objects and the geometry of the contact surface. For a specific mechanical system, the material properties of the components have been determined, and only the contact surface geometry may affect the contact stiffness coefficient.

The actual mechanical interface consists of two rough surfaces. According to the results of Reference [21], the contact area can be reduced to a rigid plane in contact with a rough surface. Figure 2 shows a schematic diagram of the contact between a microconvex body and a rigid plane. When the contact occurs, the real area of the rough surface accounts for only a small part of the nominal contact area. Therefore, the contact problem of the mechanical joint surface can be handled with the contact of the convex body. When the surface is stressed, the microconvex body will occur elastic or plastic deformation. We focus on the elastic deformation of the local components.

(a)

(b)

Figure 2: Schematic diagram of the contact between a microconvex body and a rigid plane. (a) Unloaded state. (b) Loaded state.

The single microconvex body on the rough surface is equivalent to the sphere, and R is recorded as its equivalent radius of curvature.

When the normal load p is applied to the contact point, is the normal contact deformation. The radius of the contact area is R. According to Reference [20], the relationship between p and is

where is the modulus of elasticity of the two contact materials:

where and represent Poisson’s ratio and Young’s modulus of the material, respectively. Subscripts f and c represent the follower and cam.

According to equation (6), the normal contact stiffness of a single microconvex body contact with a rigid plane is

According to the geometric relationship between the microconvex deformation and the typical value of the fractal roughness parameter G in Reference [22], , and the expression of the cross-sectional area of the microconvex body is

Substituting equation (9) into (8), we can obtain

According to the contact fractal theory [23], the distribution function of the contact point of the microcontact area is

where is the actual contact area of the maximum contact point, is the real contact area of the rough surface, and is the fractal dimension of rough surface which reflects the irregularity and complexity of surface profile on all scales. Considering the two-dimensional fractal problem, the range . According to the Hertz contact theory, when contact occurs, the contact area of two objects is elliptical, and the real contact area is about .

Assume that the rough surface is isotropic in the microtopography. According to the contact fractal theory, the microconvex body contact deformation belongs to the plastic deformation when , and the contact deformation belongs to the elastic deformation when . is determined by Reference [24] as

where is the fractal roughness parameter of the rough surface. Larger G means rougher contact surface. is a factor related to the softer material hardness and the yield strength , and is generally taken as 2.8. is a factor related to and the equivalent elastic modulus .

Thus the normal contact stiffness of the joint surface is

Substituting Equations (10) and (11) into (14), we can obtain

According to the relationship , we have

Substituting Equation (16) into (15), the normal contact stiffness can be obtained

For a definite rough surface, is constant, and the normal stiffness depends on the real contact area of the maximum contact point.

2.5. Contact Line Length with Random Normal Distribution

Using the Hertz contact theory in Reference [24], the equivalent stiffness coefficient is given by

where represents the length of the contact line.

Assume that the length of the contact line obeys the law of normal distribution, that is, the contact line length is controlled by the position parameter and the scale parameter . and , respectively, determine the position and amplitude of the normal distribution. Figure 3 shows the numerical simulation of the normal contact line length with random distribution. It is found that the amplitude range of the contact line length increases as the scale parameter increases. Obviously, the position parameter and the scale parameter affect the dynamic response of the system. indicates that the normal contact line length is constant, and indicates that the length is a random parameter.

(a)

(b)

(c)

Figure 3: Normally distributed random contact line length. (a) . (b) . (c) .

3. Numerical Simulation

Considering the system dynamic equations contain strong nonlinear time-varying parameters, the analytic solutions are difficult to obtain. The numerical iterative method, fourth-order Runge–Kutta, is employed to solve the dynamic equations and calculates the system’s response over 20 seconds. From the numerical simulation results, it is found that the first several periods’ responses are generally affected by the initial integral parameters and we give up these responses to eliminate the transient effect.

At the initial time, the follower and cam keep in touch, and the parameter values of the cam-follower oblique impact system are shown in Table 1. In the simulation process, the system response is calculated by equation (1), and the follower angular velocity value is calculated by the impact law of equation (4).

Table 1: Values of the system parameters.

Parameters
Values

Follower length,

Follower radius,

Follower mass,

Cam radius,

Cam eccentricity,

Poisson’s ratio,

Acceleration of gravity,

Friction coefficient,
0.3

Impact damping factor,

Impact recovery coefficient,

Modulus of elasticity,

Cam speed,

3.1. Effect of Contact Line Length

The length of the contact line affects the nonlinear stiffness coefficient of the contact surface. Taking the contact line length as the control parameter, varies from 0.001 m to 0.018 m in steps of 0.00025 m, and the global bifurcation diagram of the follower angle position is shown in Figure 4. It can be found from the bifurcation diagram that the cam-follower system exhibits complex dynamic behaviors, including periodic motion, quasiperiodic motion, and chaotic motion. The system response changes from the initial chaotic motion first to periodic 2, then to quasiperiod 2, and then finally to chaos.

Figure 4: Global bifurcation diagram of .

3.2. Effect of Joint Surface Fractal

Take  = 2.8,  = 0.01,  = , , and takes , , and , respectively. Figure 5 shows the variation of contact stiffness with fractal parameters G and D. It can be found that increases with the increase of the fractal dimension D and decreases with the increase of the scale parameter G, which indicates that increasing the roughness of the joint surface is benefit to the reduction of the normal contact stiffness.

Figure 5: Variation of contact stiffness with G and D.

Taking the fractal dimension as the control parameter, the global bifurcation diagram of the follower angle position for the different scale parameters G is shown in Figure 6. It can be found from Figure 6 that the system response is more sensitive to the fractal parameters D and G. Smaller parameter variety will affect the response state. When , the system first enters the period 2, soon moves into the quasiperiod 2, and finally moves into large amplitude chaos. In addition, corresponds to the larger bandwidth of the relatively stable response interval of the system. Smaller G means smaller joint normal contact stiffness, and it is benefit to the stability of the system response.

(a)

(b)

Figure 6: Global bifurcation diagram of with D for different G. (a) . (b) .

3.3. Effect of Random Contact Line Length

From the bifurcation diagram of Figure 4, it can be found that the system performs quasiperiod 2 motion when . Figure 7 shows the system response with different contact line length distributions for and . is the angle between the rod and the horizontal direction in the persistent contact. It can be found that as the random deviation σ increases, the system response evolves from quasiperiodic to chaos, which indicates that the contact line length with a normal random distribution can lead the system unsteady.

(a)

(b)

(c)

Figure 7: System response with different contact line length distributions (). (a) Quasiperiod 2 (; left frame: red represents , blue represents ). (b) Quasiperiod 2 (; left frame: red represents , blue represents ). (c) Chaos (; left frame: red represents , blue represents ).

In Figure 4, when , the system response is chaos. Figure 8 shows the system response for different σ when and . It can be seen that all systems exhibit quasiperiod 2 motions, which indicates that the random deviations can effectively suppress the chaos in the system.

(a)

(b)

(c)

Figure 8: System response for the different σ (). (a) Quasiperiod 2 (; left frame: red represents , blue represents ). (b) Quasiperiod 2 (; left frame: red represents , blue represents ). (c) Quasiperiod 2 (; left frame: red represents , blue represents ).

The determinate response is shown in Figure 9 when , and it is chaos. Figure 10 shows the system response after applying a random deviation when . It can be found that the system also exhibits quasiperiod 2, which means applying random deviation can effectively suppress the chaos in the system.

Figure 9: Chaotic response when ().

(a)

(b)

(c)

Figure 10: System response after applying a random deviation (). (a) Quasiperiod 2 (; left frame: red represents , blue represents ). (b) Quasiperiod 2 (; left frame: red represents , blue represents ). (c) Quasiperiod 2 (; left frame: red represents , blue represents ).

4. Conclusions

In this paper, the fractal model of the normal contact stiffness has been established by considering the microtopography of the joint surface. The effects of the fractal dimension D and the scale parameter G on the dynamic characteristics of the cam-follower oblique impact system have been studied. The effects of the location and scale parameters of the system dynamic characteristics have been analyzed. The main conclusions can be listed as follows:

(1)Increasing the roughness of the joint surface is a benefit to the reduction of the normal contact stiffness.(2)The system response is more sensitive to the fractal parameters, D and G. The response state changes as a minor parameter varies, and the system response eventually turns into chaos with the increase of D.(3)The system response changes between quasiperiod and chaos affected by the contact line length with a normal random distribution.

Data Availability

The data used to support the findings of this study are available from the corresponding author upon request.

Conflicts of Interest

The authors declare that they have no financial or nonfinancial competing interest, and all of the authors agree to the publication of this paper.

Acknowledgments

This study was funded by the National Natural Science Foundation of China (grant number 11272257), NPU Aoxiang New Star and the Fundamental Research Funds for the Central Universities (grant number 3102018ZY016), and the Key Laboratory of Vibration and Control of Aero-Propulsion System Ministry of Education, Northeastern University (grant number VCAME201803).

References

P. Flores, R. Leine, and C. Glocker, “Modeling and analysis of planar rigid multibody systems with translational clearance joints based on the non-smooth dynamics approach,” Multibody System Dynamics, vol. 23, no. 2, pp. 165–190, 2009.

Y. Yang, Q. Wu, Y. Wang, W. Qin, and K. Lu, “Dynamic characteristics of cracked uncertain hollow-shaft,” Mechanical Systems and Signal Processing, 2019, In press.

R. Lima and R. Sampaio, “Stick-mode duration of a dry-friction oscillator with an uncertain model,” Journal of Sound and Vibration, vol. 353, pp. 259–271, 2015.

H. Dai, X. Jing, Y. Wang, X. Yue, and J. Yuan, “Post-capture vibration suppression of spacecraft via a bio-inspired isolation system,” Mechanical Systems and Signal Processing, vol. 105, pp. 214–240, 2018.

Y. Yang, H. Chen, and T. Jiang, “Nonlinear response prediction of cracked rotor based on EMD,” Journal of the Franklin Institute, vol. 352, no. 8, pp. 3378–3393, 2015.

M. D. Nora, T. D. M. Lanzanova, and H. Zhao, “Investigation of performance and combustion characteristics of a four-valve supercharged two-stroke DI engine fuelled with gasoline and ethanol,” Fuel, vol. 227, pp. 401–411, 2018.

R. Alzate, M. di Bernardo, U. Montanaro, and S. Santini, “Experimental and numerical verification of bifurcations and chaos in cam-follower impacting systems,” Nonlinear Dynamics, vol. 50, no. 3, pp. 409–429, 2007.

Y. Shen and W. J. Stronge, “Painlevé paradox during oblique impact with friction,” European Journal of Mechanics-A/Solids, vol. 30, no. 4, pp. 457–467, 2011.

H. S. Yan, M. C. Tsai, and M. H. Hsu, “An experimental study of the effects of cam speeds on cam-follower systems,” Mechanism and Machine Theory, vol. 31, no. 4, pp. 397–412, 1996.

W. Zhang and M. Ye, “Local and global bifurcations of valve mechanism,” Nonlinear Dynamics, vol. 6, no. 3, pp. 301–316, 1996.

T. Zhang, H. G. Li, Z. Y. Zhong, and G. P. Cai, “Hysteresis model and adaptive vibration suppression for a smart beam with time delay,” Journal of Sound and Vibration, vol. 358, pp. 35–47, 2015.

H. Ding and L.-Q. Chen, “Galerkin methods for natural frequencies of high-speed axially moving beams,” Journal of Sound and Vibration, vol. 329, no. 17, pp. 3484–3494, 2010.

H. Ding, L.-Q. Chen, and S.-P. Yang, “Convergence of Galerkin truncation for dynamic response of finite beams on nonlinear foundations under a moving load,” Journal of Sound and Vibration, vol. 331, no. 10, pp. 2426–2442, 2012.

R. Alzate, M. di Bernardo, G. Giordano, G. Rea, and S. Santini, “Experimental and numerical investigation of coexistence, novel bifurcations, and chaos in a cam-follower system,” SIAM Journal on Applied Dynamical Systems, vol. 8, no. 2, pp. 592–623, 2009.

R. Alzate, P. T. Piiroinen, and M. di Bernardo, “From complete to incomplete chattering: a novel route to chaos in impacting cam-follower systems,” International Journal of Bifurcation and Chaos, vol. 22, no. 5, Article ID 1250102, 2012.

S. Sundar, J. T. Dreyer, and R. Singh, “Rotational sliding contact dynamics in a non-linear cam-follower system as excited by a periodic motion,” Journal of Sound and Vibration, vol. 332, no. 18, pp. 4280–4295, 2013.

N. A. H. Tsuha, F. Nonato, and K. L. Cavalca, “Formulation of a reduced order model for the stiffness on elastohydrodynamic line contacts applied to cam-follower mechanism,” Mechanism and Machine Theory, vol. 113, pp. 22–39, 2017.

W. Pan, X. Li, L. Wang, N. Guo, and Z. Yang, “Influence of contact stiffness of joint surfaces on oscillation system based on the fractal theory,” Archive of Applied Mechanics, vol. 88, no. 4, pp. 525–541, 2017.

A. Majumdar and B. Bhushan, “Fractal model of elastic-plastic contact between rough surfaces,” Journal of Tribology, vol. 113, no. 1, pp. 1–11, 1991.

C. Padmanabhan and R. Singh, “Dynamics of a piecewise non-linear system subject to dual harmonic excitation using parametric continuation,” Journal of Sound and Vibration, vol. 184, no. 5, pp. 767–799, 1995.

X. Zhang, N. Wang, G. Lan, S. Wen, and Y. Chen, “Tangential damping and its dissipation factor models of joint interfaces based on fractal theory with simulations,” Journal of Tribology-Transactions of the ASME, vol. 136, no. 1, Article ID 011704, 2014.

S. Wang and K. Komvopoulos, “A fractal theory of the interfacial temperature distribution in the slow sliding regime: Part II-multiple domains, elastoplastic contacts and applications,” Journal of Tribology, vol. 116, no. 4, pp. 824–832, 1994.

S. Wang and K. Komvopoulos, “A fractal theory of the interfacial temperature distribution in the slow sliding regime: Part I-elastic contact and heat transfer analysis,” Journal of Tribology, vol. 116, no. 4, pp. 812–822, 1994.

K. L. Johnson, Contact Mechanics, Cambridge University Press, Cambridge, UK, 1987.