Sage Journals: Discover world-class research

Abstract

Based on Hertz contact theory, an elastic-plastic contact mechanics model of outer cylinder under different contact angles of axis is proposed. The relationship among contact angle, load and contact deformation, contact stiffness and contact area is established. The finite element method is used to simulate the elastic-plastic contact process of the cylinder. The influence of the load and radius of the cylinder model on the contact deformation and the contact stiffness is compared and analyzed under different contact angles. The error of the analysis results of the finite element and the mechanical model is within 9%. On this basis, the influence of contact deformation, contact area and contact angle on the contact stiffness of the outer cylinder in elastic and plastic stage is explored. The results show that in the stage of elastic and plastic deformation, the amount of contact deformation and contact area increase with the increase of load. The contact stiffness decreases with the increase of contact angle and increases with the increase of cylinder radius. The amount of contact deformation decreases with the increase of cylinder radius, and tends to constant gradually. In the elastic stage, the contact stiffness increases with the increase of load. The contact area decreases with the increase of contact angle and increases with the increase of cylinder radius. In the plastic stage, the contact stiffness is constant with the increase of load, and the contact area is independent of contact angle and cylinder radius.

Keywords

Cylinder contact model contact finite element elastic–plastic contact angles contact stiffness

Introduction

Hertz contact theory¹ and fractal theory are the main methods to analyze cylinder contact model. In recent years, several typical cylinder contact models have been proposed based on Hertz contact theory.² Johnson³ proposed a model of long cylinder in non-conformal contact, which considered the internal and external contact between two cylinders. Radzimovsky⁴ proposed an outer cylinder contact model, which was derived from the stress–strain formula. Goldsmith⁵ also proposed an inner cylinder contact model based on Hertz theory, which gave the expression between the load and the contact deformation. However, the above studies are all elastic contact models, so it is impossible to analyze the mechanical properties of the model under the condition of plastic deformation under heavy load. Moreover, the above model formulas include logarithmic function; so when the load is applied to a certain value, the model will fail.² Through the research of rolling bearing, Lui and Shao^6,7 put forward a cylinder contact model with lubricating oil film, which analyzed the influence of support stiffness on contact deformation. Sharma and Jackson⁸ carried out the finite element analysis of the elastoplastic cylinder contact problem, and compared the finite element results under the elastic and full plastic conditions with the existing Hertz contact and spherical elastoplastic contact models. Vijaywargiya and Green⁹ simulated two-dimensional sliding between two interacting elastoplastic cylinders by finite element analysis. Dumas and Baronet¹⁰ used the finite element method to study the elastic–plastic indentation of an infinite rigid cylinder with its axis parallel to the surface of half-space in detail, and gave the calculation results of different strain hardening slopes. Jackson¹¹ presented a simple solution to a cylindrical rigid frictionless punch indenting a half-space considering only perfectly plastic deformation, which was verified by the finite element calculation. Based on the finite element method, Komvopoulos¹² solved the elastic contact problem of a layered semi-infinite solid with rigid surface compression. Cinar and Sinclair¹³ studied the problem of infinite rigid cylinder under the condition of frictionless and complete adhesion release under incremental elastic–plastic condition. Bower and Johnson¹⁴ evaluated the effect of strain hardening on the cumulative plastic deformation of cylinder under repeated rolling and sliding contact by using the non-linear kinematic hardening law. By comparing different contact models, Beheshti and Khonsari¹⁵ found that the use of elastic–plastic micro-contact model can predict lower maximum normal pressure and larger contact width and actual contact area. Based on the fractal theory and Hertz contact theory, Huang et al.¹⁶ established the contact model of two cylinders. Zhao et al.¹⁷ established the fractal model of normal contact stiffness of the joint surface of two cylinders. Based on the theory of classification, Li et al.¹⁸ established a fractal prediction model of the normal stiffness of the joint surface of two cylinders considering friction factors. Based on the Hertz contact theory and the fractal theory, the deformation properties of the model in elastic, elastic–plastic, and plastic stages are analyzed, but the deformation properties of the cylinder contact model in different contact angles are not considered.

Therefore, based on Hertz contact theory, this article proposes an elastic–plastic contact model of cylinder under different contact angles; establishes the relationship between load and contact deformation, contact stiffness, and contact area; and uses the finite element method to simulate the elastic–plastic contact process for comparison. The first section of the article establishes the contact mechanical model of the cylinder, which mainly derives the deformation formula of the cylinder model in the elastic and plastic phases. The second section conducts simulation analysis and comparison of the cylinder model, which mainly analyzes the effect of the load on the contact deformation and the effect of load on contact stiffness. In the third section, the contact mechanical characteristics of cylinder are studied, which mainly analyzes the effect of the load on the contact area and the influence of the cylinder radius on the model mechanical properties.

Cylinder contact mechanics model

The contact state of cylinder model can be divided into three stages: elastic stage, elastic–plastic stage, and plastic stage. In this model, the deformation formulas of cylinder in elastic and plastic stage are derived.

Full elastic contact

Let the radius of both cylinders be $R$ . When there is no load, the two cylinders only contact at one point. As shown in Figure 1, the original gap between the two contact points $M_{1}$ and $M_{2}$ is $h = z_{1} - z_{2}$ . Under the pressure, the deformation displacement of the upper cylinder at $M_{1}$ is $ω_{1}$ , and that of the lower cylinder at $M_{2}$ is $ω_{2}$ . From the geometric relationship, the distance $α$ of the two contact points $M_{1}$ and $M_{2}$ approaching each other can be expressed as

\begin{matrix} α = h + ω_{1} + ω_{2} \\ = \frac{si n^{2} θ}{2 R} x^{2} + \frac{1 + co s^{2} θ}{2 R} y^{2} + ω_{1} + ω_{2} \end{matrix}

(1)

From equation (1) and the displacement formula of the midpoint of the object under the distributed pressure on the semi-infinite boundary plane¹⁹

(k_{1} + k_{2}) \int \int \frac{F'}{R_{1}} dx' dy' = α - \frac{si n^{2} θ}{2 R} x^{2} - \frac{1 + co s^{2} θ}{2 R} y^{2}

(2)

where $k_{1} = (1 - v_{1}^{2}) / (π E_{1})$ and $k_{2} = (1 - v_{2}^{2}) / (π E_{2})$ ; $F' dx' dy'$ is the pressure acting on element $dx' dy'$ of the contact part; $R_{1}$ is the distance from any point on the contact surface to the specified point on the contact surface; $θ$ is the contact angle; $υ_{1, 2}$ is Poisson’s ratio; and $E_{1, 2}$ is Young’s moduli.

Figure 1.

Cylinder contact model: (a) before loading and (b) after loading.

From equation (2), the area of the contact ellipse and the relationship between the load and the deformation can be obtained as

S = π {(1 - e^{2})}^{- \frac{1}{6}} {[\frac{3}{2} (k_{1} + k_{2}) PR E_{(e)}]}^{\frac{2}{3}}

(3)

P_{1} = [{(\frac{2}{3})}^{\frac{2}{3}} {(\frac{E_{(e)} R}{1 - e^{2}})}^{\frac{1}{3}} \frac{1}{K_{(e)} {(k_{1} + k_{2})}^{\frac{2}{3}}}] α^{\frac{3}{2}}

(4)

where $K_{(e)} = \int_{0}^{\frac{π}{2}} d φ / \sqrt{1 - e^{2} \sin^{2} φ}$ , $E_{(e)} = \int_{0}^{\frac{π}{2}} \sqrt{1 - e^{2} \sin^{2} φ} d φ$ ; $S$ is the contact area; $P_{1}$ is the load; and $e$ is the radius of curvature of the contact ellipse.

Elastic–plastic contact

When the two cylinders in contact appear initial yield, the average contact pressure between the contact surfaces can be expressed as²⁰

P_{e} = σ_{e} C^{- 1}

(5)

where $P_{e}$ is the average contact pressure, $σ_{e}$ is the maximum von Mises stress, and $C^{- 1}$ is a constant.

Green²⁰ gave the calculation formula of constant C

C = {\begin{matrix} \frac{1}{\sqrt{1 + 4 (v - 1) v}} & v \leq 0.1938 \\ 1.164 + 2.975 v - 2.906 v^{2} & v > 0.1938 \end{matrix}

(6)

where $v$ is Poisson’s ratio.

From equation (4)

P_{e} = [{(\frac{2}{3})}^{\frac{2}{3}} {(\frac{E_{(e)} R}{1 - e^{2}})}^{\frac{1}{3}} \frac{1}{K_{(e)} {(k_{1} + k_{2})}^{\frac{2}{3}}}] α_{1}^{\frac{3}{2}}

(7)

According to equations (5) and (7), the displacement distance of two cylinders at initial yield is

α_{1} = {(σ_{e} C^{- 1})}^{\frac{2}{3}} {(\frac{9 (1 - e^{2}) K_{(e)}^{3} {(k_{1} + k_{2})}^{2}}{4 E_{(e)} R})}^{\frac{2}{9}}

(8)

where $α_{1}$ is the displacement distance at initial yield.

Plastic contact

When the material enters the complete plastic deformation stage, the average contact pressure is close to the yield strength²¹

P_{e} = σ_{s}

(9)

where $σ_{s}$ is the yield strength.

According to the theory of ABBOTT, E.J.²², the contact area can be expressed as

A_{p} = 2 S

(10)

where $A_{p}$ represents the contact area in plastic stage.

From equations (3) and (4)

S = π {[\frac{3 (k_{1} + k_{2}) {(E_{(e)} R)}^{4}}{2 {(1 - e^{2})}^{\frac{7}{4}} K_{(e)}^{3}}]}^{\frac{2}{9}} α

(11)

According to equation (10), the contact area can be obtained as

A_{p} = 2 π {[\frac{3 (k_{1} + k_{2}) {(E_{(e)} R)}^{4}}{2 {(1 - e^{2})}^{\frac{7}{4}} K_{(e)}^{3}}]}^{\frac{2}{9}} α

(12)

Then the total load can be expressed as

P = P_{e} A_{p}

(13)

where P is the total load.

Namely

P = 2 π σ_{s} {[\frac{3 (k_{1} + k_{2}) {(E_{(e)} R)}^{4}}{2 {(1 - e^{2})}^{\frac{7}{4}} K_{(e)}^{3}}]}^{\frac{2}{9}} α

(14)

According to equation (14), the contact stiffness is

K = \frac{dP}{d α}

(15)

where $K$ represents the contact stiffness.

Namely

K = 2 π σ_{s} {[\frac{3 (k_{1} + k_{2}) {(E_{(e)} R)}^{4}}{2 {(1 - e^{2})}^{\frac{7}{4}} K_{(e)}^{3}}]}^{\frac{2}{9}}

(16)

Fiinite element method analysis and comparison

Modeling and analysis

In this article, the upper and lower cylinder models are made of carbon structural steel of the same material. The following material properties are selected: Young’s moduli $E = 2.1 \times 10^{5} MPa$ , $υ = 0.3$ , yield strength $H = 380 MPa$ , and $R = 2.5 mm$ . This article mainly analyzes the mechanical characteristics of the cylinder model when it is in contact with 45°, 60°, and 90°. As shown in Figure 2, the cylinder mesh model adopts the face-to-face contact mode and refines the mesh around the contact surface. The minimum mesh size is $4 \times 10^{- 4} mm$ . The boundary condition is that the bottom degree of freedom of the lower cylinder model is fully fixed. And the top of the upper cylinder model is fixed except for the free end in the vertical direction. The vertical load is applied to the upper surface of the upper cylinder model, and the simulation calculation is carried out.

Figure 2.

Cylinder mesh model: (a) 45°, (b) 60°, and (c) 90°.

The simulation results of strain pattern can be obtained after solution. Figure 3(a) is the integral deformation cloud of the cylinder model, the contact angle is 90°, and the load is $20 KN$ , and Figure 3(b) is the vertical partial deformation cloud diagram of the lower cylinder, which clearly reflects the distribution and size of deformation. It can be seen that the maximum deformation of the contact surface is symmetrically distributed around the middle point, rather than appearing at the middle point. This is because the overall deformation of the cylinder model is characterized by point-to-surface contact. At the beginning of the contact, there is no contact but a certain distance around the middle point of the contact surface between the upper and lower cylinders, so the amount of deformation around the contact will be greater than the middle position during the contact process. And finally the contact surface will be formed.

Figure 3.

Cloud chart of cylinder contact deformation: (a) global deformation cloud and (b) cloud picture of local deformation of lower cylinder.

Contact deformation comparison

The amount of deformation obtained by the theoretical derivation formula of the elastic–plastic deformation of the cylinder model is compared with the result obtained by the finite element simulation, and the data are fitted by the image.

It can be seen from Figure 4 that there are some errors between the simulation value and the theoretical value of contact deformation, but the trend is consistent. When the load is about $6 KN$ , the model begins to plastic deformation, in which the elastic stage is exponential and the plastic stage is linear, and the contact deformation increases with the increase of load. Figure 4 also shows clearly that the cylindrical model has a higher data consistency in the elastic stage than in the plastic stage. Therefore, the errors between the simulated and theoretical values of plastic contact deformation at $14$ and $20 KN$ are further compared in Table 1. The maximum deformation error is 8.95% and the minimum deformation error is 0.81%. Under the same load, the contact deformation increases with the increase of contact angle.

Figure 4.

Comparison between simulation value and theoretical value of contact deformation: (a) 45° contact, (b) 60° contact, and (c) 90° contact.

Table 1.

Comparison between simulation value and theoretical value of contact deformation.

Contact angle/°	P/KN	$α$ (simulation value)/µm	$α$ (theoretical value)/µm	Deformation error/%
45	14	1.86543	1.71227	8.95
45	20	2.61457	2.44610	6.89
60	14	1.97147	1.98737	0.81
60	20	2.65624	2.81639	5.96
90	14	2.15773	1.98988	8.43
90	20	3.08247	3.30868	7.34

From the angle of error generation, it is mainly divided into two aspects. On one hand, it is analyzed from the material itself that the material has not reached the stage of complete plastic deformation during loading, and there is certain elastic deformation which results in deviation of the deformation quantity; on the other hand, it is analyzed from the model itself. The main sources of errors include partition density of grid unit, calculation method of model, setting of boundary conditions, and geometric dimensions. For the first error, the contact deformation can be removed from the elastic region by increasing the applied load; for the second error, it can be solved by further improving the accuracy of the grid element, selecting a more appropriate unit type and contact type, and a more accurate geometric model.

Contact stiffness comparison

It can be seen from the comparison of theoretical value and simulation value of contact stiffness of cylindrical model that the change trend of theoretical value and simulation value of the model is basically the same as that shown in Figure 5. In the elastic stage, the contact stiffness increases exponentially with increasing load, and in the plastic stage, the contact stiffness remains unchanged regardless of the load.

Figure 5.

Comparison between simulation value and theoretical value of contact stiffness: (a) 45° contact, (b) 60° contact, and (c) 90° contact.

The simulation value and theoretical value rigidity of $P = 14$ and $20 KN$ under different contact angles are also compared here. As shown in Table 2, the maximum rigidity error is $8.44 %$ , and the minimum rigidity error is only $0.80 %$ . The reason for the error is basically the same as the above statement, and under the same load, the contact rigidity decreases with the increase of contact angle.

Table 2.

Comparison between simulation value and theoretical value of contact stiffness.

Contact angle/°	P/KN	K (simulation value)/(KN/mm)	K (theoretical value)/(KN/mm)	Stiffness error/%
45	14	7504.95	8176.27	8.21
45	20	7649.44	8176.27	6.44
60	14	7044.50	7101.29	0.80
60	20	7529.44	7101.29	6.03
90	14	7035.62	6488.31	8.44
90	20	6044.71	6488.31	6.84

Contact analysis

Load influence

Figure 6 shows the influence of load on the contact area. The following material properties were selected: $E = 2.1 \times 10^{5} MPa$ , $υ = 0.3$ , $H = 380 MPa$ , and $R = 2.5 m$ . It can be seen from Figure 6 that the contact area increases with the increase of load, in which the elastic stage is exponential and the plastic stage is linear. Under the same load, the contact area of the elastic stage decreases with the increase of contact angle, and the contact area of the plastic stage is independent of contact angle.

Figure 6.

Influence of load on contact area.

Cylinder radius influence

Figures 7 –9 show the influence of cylinder radius on contact deformation, contact stiffness, and contact area, respectively. The following material properties were selected: $E = 2.1 \times 10^{5} MPa$ , $υ = 0.3$ , $H = 380 MPa$ , and $θ = 9 0^{°}$ . It can be seen from Figure 7 that the contact deformation decreases with the increase of the cylinder radius. As the contact deformation tends to be constant, the contact can be considered as the contact between two planes. From Figure 8, it can be seen that the contact stiffness increases with the increase of the cylinder radius. Figure 9 shows that in the elastic stage, the contact area increases with the increase of the cylinder radius; in the plastic stage, the contact area is independent of the cylinder radius.

Figure 7.

Influence of radius on contact deformation.

Figure 8.

Influence of radius on contact stiffness.

Figure 9.

Influence of radius on contact area.

Conclusion

Based on Hertz contact theory, this article presents an elastic–plastic contact mechanics model of cylinder under different contact angles of axis, including the relationship between contact angle, load and contact deformation, contact stiffness, and contact area, which is verified by finite element method. Based on this, the contact mechanical properties of cylinder are explored.

The contact deformation increases with the increase of load and contact angle.

In the elastic stage, the contact stiffness increases with the increase of load, and in the plastic stage, the contact stiffness does not change with the increase of load. The contact stiffness decreases with the increase of contact angle.

The contact area increases with the increase of load. In the elastic stage, the contact area decreases with the increase of contact angle, and in the plastic stage, the contact area is independent of contact angle.

In the elastic stage, the contact area increases with the increase of the cylinder radius, and in the plastic stage, the contact area is independent of the cylinder radius.

Footnotes

Declaration of conflicting interests

The author(s) declared no potential conflicts of interest with respect to the research, authorship, and/or publication of this article.

Funding

The author(s) disclosed receipt of the following financial support for the research, authorship, and/or publication of this article: This project is supported by National Natural Science Foundation of China (Grant No. 51875009).

ORCID iD

TieNeng Guo

Author biographies

Tieneng Guo is an associate professor, working at Beijing University of Technology, Beijing, China. His main research areas are structural dynamics, vibration detection and analysis, structural vibration and control, nonlinear vibration, etc.

Xu Hua is a graduate student studying at Beijing University of Technology, Beijing, China. His main research field is the mechanical characteristics of the combined surface of the regular characteristics of the machined surface.

Zhijie Yan is a graduate student studying at Beijing University of Technology, Beijing, China. His main research field is the mechanical characteristics of the combined surface of the regular characteristics of the machined surface.

Chunsheng Bai works in Tianjin Institute of Aerospace Mechanical and Electrical Equipment, Tianjin, Beijing. His main research fields are vibration analysis of fan bridge and stiffness research of joint surface.

References

Shen

Bao

. Advances in studies on asperity peak contacts. Light Ind Mach 2010; 28(6): 1–4.

Pereira

Ramalho

Ambrósio

. A critical overview of internal and external cylinder contact force models. Nonlinear Dynamic 2011; 63(4): 681–697.

Johnson

. Contact mechanics. Cambridge, MA: Cambridge University Press, 1987.

Radzimovsky

. Stress distribution and strength conditions of two rolling cylinders pressed together. Eng Exp Sta Univ Ill 1953; 408: 127–134.

Goldsmith

. Impact: the theory and physical behaviour of colliding solids. Mineola, NY: Dover Publications, 2001.

Liu

Shao

. An improved analytical model for a lubricated roller bearing including a localized defect with different edge shapes. J Vib Control 2018; 24(17): 3894–3907.

Liu

. A dynamic modelling method of a rotor-roller bearing-housing system with a localized fault including the additional excitation zone. J Sound Vib 2020; 469: 115144.

Sharma

Jackson

. A finite element study of an elasto-plastic disk or cylindrical contact against a rigid flat in plane stress with bilinear hardening. Tribol Lett 2017; 65(3): 112.

Vijaywargiya

Green

. A finite element study of the deformations, forces, stress formations, and energy losses in sliding cylindrical contacts. Int J Non Linear Mech 2007; 42(7): 914–927.

10.

Dumas

Baronet

. Elastoplastic indentation of a half-space by an infinitely long rigid circular cylinder. Int J Mech Sci 1971; 13(6): 519–530.

11.

Jackson

. A solution of rigid perfectly plastic cylindrical indentation in plane strain and comparison to elastic-plastic finite element predictions with hardening. J Appl Mech T ASME 2018; 85(2): 024501.

12.

Komvopoulos

. Finite element analysis of a layered elastic solid in normal contact with a rigid surface. J Tribol 1988; 110(3): 477–485.

13.

Cinar

Sinclair

. Quasi-static normal indentation of an elasto-plastic half-space by a rigid circular cylinder of infinite length. Int J Solids Struct 1986; 22(8): 919–934.

14.

Bower

Johnson

. The influence of strain hardening on cumulative plastic deformation in rolling and sliding line contact. J Mech Phys Solids 1989; 37(4): 471–493.

15.

Beheshti

Khonsari

. Asperity micro-contact models as applied to the deformation of rough line contact. Tribol Int 2012; 52: 61–74.

16.

Huang

Zhao

Chen

. Research of fractal contact model on contact carrying capacity of two cylinders’ surface. Tribology 2008; 28(6): 529–533.

17.

Zhao

Chen

Huang

. Fractal model of normal contact stiffness between two cylinders’ joint interfaces. J Mech Eng 2011; 47(7): 53–58.

18.

Zhao

Liang

, et al. Fractal model and simulation of normal contact stiffness between two cylinders’ joint surfaces. Trans Chin Soc Agricult Mach 2013; 44(10): 277–281; 293.

19.

Johnson

. Contact mechanics. Cambridge: Cambridge University Press, 1985, pp. 84–106.

20.

Green

. Poisson ratio effects and critical values in spherical and cylindrical Hertzian contacts. Int J Appl Mech Eng 2005; 10(3): 451–462.

21.

Ghaednia

Wang

Saha

, et al. A review of elastic–plastic contact mechanics. Appl Mech Rev 2017; 69(6): 060804.

22.

Song

Xie

, et al. Mechanical engineering and technology. Berlin: Springer, 2012, pp. 100–105.

Research on the elastic–plastic external contact mechanical properties of cylinder

Abstract

Keywords

Introduction

Cylinder contact mechanics model

Full elastic contact

Elastic–plastic contact

Plastic contact

Fiinite element method analysis and comparison

Modeling and analysis

Contact deformation comparison

Contact stiffness comparison

Contact analysis

Load influence

Cylinder radius influence

Conclusion

Footnotes

Declaration of conflicting interests

Funding

ORCID iD

Author biographies

References