Dynamic analysis of reciprocating compressor with clearance and subsidence

Xiao, Shungen; Liu, Shulin; Cheng, Shouguo; Xue, Xiaogang; Song, Mengmeng; Sun, Xin

doi:10.21595/jve.2017.18771

Journal of Vibroengineering

Browse Journal

Submit article

Published: 15 November 2017

Check for updates

Dynamic analysis of reciprocating compressor with clearance and subsidence

Shungen Xiao¹

Shulin Liu²

Shouguo Cheng³

Xiaogang Xue⁴

Mengmeng Song⁵

Xin Sun⁶

^{1, 2, 3, 4, 6}School of Mechatronical Engineering and Automation, Shanghai University, Shanghai, People’s Republic of China

³Department of Mechanical and Electrical Engineering, Jiangyin Polytechnic College, Jiangsu, People’s Republic of China

^{5, 1}College of Information, Mechanical and Electrical Engineering, Ningde Normal University, Ningde, People’s Republic of China

Corresponding Author:

Shulin Liu

Cite the article Download PDF

Downloads 1827

WoS Core Citations 6

CrossRef Citations 12

Abstract

In this paper, the reciprocating compressor with clearance and subsidence of the crosshead is studied, considering the varying cylinder pressure. To investigate the nonlinear dynamical behaviors of the reciprocating compressor precisely, a novel dynamic model of the reciprocating compressor of single cylinder with clearance and subsidence for the varying cylinder pressure is established based on the Lagrangian approach. It is demonstrated that different clearance sizes, subsidence sizes and crankshaft angular velocities can affect the dynamic response of the crosshead in the horizontal direction, respectively. The analysis results of dynamic response illustrate that with the increase of clearance sizes and subsidence sizes, the influence of crosshead displacement, velocity and acceleration increase, but the effect of clearance is much stronger than subsidence. Fast Fourier transformation is also applied to analyze the frequency spectrum of the system response. Moreover, the stability of the motion is studied using phase trajectories, maximum Lyapunov exponents and Poincaré sections. Numerical solution results show that clearance sizes, subsidence sizes and crankshaft angular velocities change the dynamical behavior of the system. Through calculation of the maximum Lyapunov exponents and Poincaré portraits, the results reveal that the reciprocating compressor system is characterized by chaotic behavior with the faults of clearance and subsidence. Furthermore, with the increase of the clearance sizes and the crankshaft angular velocities, the shapes of chaotic phase trajectories have changed greatly, and varied inconspicuously with the increase of subsidence sizes in reciprocating compressor system.

1. Introduction

Reciprocating compressors are one of the most popular machines used in petroleum and chemical production processes, such as gas compression, petroleum transportation and natural gas transportation [1, 2]. In practice, with reciprocating compressor working on a period of time, as the result of manufacture tolerance, material deformation, and wear, some clearances in its joints and subsidence of crosshead commonly exist, which are inevitable. In the case of oversized joint clearances and subsidence, contact forces generate impulsive effect, which causes increased vibration and noise, and reduces system reliability, stability, life and precision. So, clearance and subsidence play a significant role in the prediction of kinematic and dynamic behavior of reciprocating compressor [3].

In the past few decades, most studies have focused on the fault diagnosis method of reciprocating compressor with signal processing. For example, aiming at the bearing clearance fault of reciprocating compressor, a series of fault detection approaches have been used extensively in the literatures [4-6]. In addition, there are also many other studies on the fault diagnosis of reciprocating compressor valves [7-10]. However, few researchers studied the failure mechanism of reciprocating compressor with joint clearances fault and subsidence fault of crosshead, and so on. Zhao et al. [11] studied the dynamic behavior of a reciprocating compressor transmission mechanism with joint clearance. In their study, taking cylinder pressure, amplitude of clearance, crank speed and flexibility of connecting rod as influence factors, the results showed that these factors play a significant role in dynamic behavior of mechanisms. Zhao et al. [12] also presented a parameter optimization approach for planar joint clearance model and its application for dynamics simulation of reciprocating compressor. The dynamics response experimental test verified the effectiveness of this application.

Reciprocating compressor of single cylinder is a slider-crank mechanism, which is shown in Fig. 1. The crankshaft rotates one revolution, driving the connecting rod, the crosshead and the piston to reciprocate. The cylinder can realize the four processes of expansion, suction, compression and exhaust. Although working environment of reciprocating compressor has its particularity, kinematics and dynamics analysis of slider-crank mechanism with joint clearance can be used for reference. There are several publications on the dynamical analysis of slider-crank mechanisms with clearance: with regard to continuous contact force model with clearance, Earles [13], Zhang [14] and Erkaya [15] introduced a model based on permanent contact condition to study clearances in the joints, respectively. In the model, clearance is replaced by a massless virtual link that connects the journal center to the bearing center. Moreover, Feng [16] et al. performed an optimization method to control the inertia forces by redistribution of masses of the moving links in planar mechanisms, in the presence of clearances at joints. In their study, clearance is also modeled with a virtual massless link that connects the journal center to the bearing center.

For contact-separation model with clearance, Dubowsky and Freudenstein [17, 18] formulated an impact pair model to predict the dynamic response of an elastic mechanical joint with clearance. In fact, in the recent decades, there are a lot of researches [19-25] using the impact model with clearance. The contact or separation between the bushing and pin is determined by the relative eccentricity between joint elements. If the eccentricity distance is greater than the radial clearance of a joint, the bushing and pin will contact each other in the direction of the eccentricity. Conversely, if the eccentricity is less than the radial clearance of the joint, the bushing and pin will remain separated from each other [26].

For chaotic behavior with joint clearance case, Farahan [27] analyzed the nonlinear dynamic behavior of a four-bar mechanism with joint clearance at the connection between the coupler and rocker. In their study, Numerical simulations display both periodic and chaotic motions in the system behavior. Wang [28] et al. carried out a study on chaotic control of a flexible multibody system with uncertain joint clearance. In their research, with the purpose to keep the continuous contact of the clearance joint, a modified extended delayed feedback control is used to stabilize the chaotic motion of the flexible multibody system.

Fig. 1Schematic diagrams of reciprocating compressor of single cylinder

Based on the research results of the previous description, the main purpose of this study is to conduct a study based on dynamic response of single cylinder reciprocating compressor with clearance joints and subsidence of the crosshead. The paper is organized as follows: The dynamic model of single cylinder reciprocating compressor with clearance and subsidence is established in Section 2. The effects of joint clearance size, subsidence size and angular velocity are discussed in Section 3, respectively. Phase trajectories of the reciprocating compressor crosshead are analyzed, and the chaotic behavior of the motion is studied using Lyapunov exponents and Poincaré sections with the change of clearance size, subsidence size and crankshaft angular velocity under varying cylinder pressure in Section 4. Dynamic response and chaotic behavior of the reciprocating compressor are summarized in Section 5. In addition, the conclusions of this paper are also given in Section 5.

2. System model of reciprocating compressor with clearance and subsidence

After the reciprocating compressor works for a period of time, the revolute joints clearance gradually increases and the crosshead may generate subsidence due to wear. In order to study the combined effects of clearance and subsidence on the motion of the crosshead, we build the dynamical mathematical model of the reciprocating compressor system.

2.1. Model of cylinder pressure

With the crankshaft of reciprocating compressor rotating a circle, the cylinder is accordingly carried out a working cycle, including expansion, suction, compression and exhaust processes, as shown in Fig. 2. In a circle, when the crankshaft is located at zero angle, the piston is located at right end with the inlet and exhaust vales closing at the same time. As the crankshaft turns clockwise, the crosshead and piston move from right to left, working volume that is located at the right side of the piston gradually increases, cavity gas gradually expands and cylinder pressure gradually decreases, which is expansion process. When the cylinder internal pressure decreases to slightly less than the external pressure of the cavity, the inlet valve is opened, until the crosshead and piston move to the far left, which is suction process. In the suction process, cylinder pressure is almost constant. The suction process is accomplished at the far left. The compression and exhaust processes are mostly the opposite of expansion and suction. Combining with the indicator diagram of reciprocating compressor, cylinder pressure can be expressed using the following equation:

1

P = 200000 μ,

where $P$ is the cylinder pressure, $μ$ is a cylinder pressure coefficient given by:

2

μ = \{\begin{array}{l} s i n (\frac{π}{2} - θ_{1}), 0 ° + 2 n π \leq θ_{1} \leq \frac{7 π}{16} + 2 n π (n is integer) Expansion, \\ s i n \frac{π}{16}, \frac{7 π}{16} + 2 n π \leq θ_{1} \leq π + 2 n π (n is integer) Suction, \\ - s i n (θ_{1} + \frac{π}{16}), π + 2 n π \leq θ_{1} \leq \frac{23 π}{16} + 2 n π (n is integer) Compression, \\ 1, \frac{23 π}{16} + 2 n π \leq θ_{1} \leq 2 π + 2 n π (n is integer) Exhaust . \end{array}

2.2. Equations of motion

In this subsection, motion equations are obtained using Lagrangian approach for the reciprocating compressor mechanism with subsidence of the crosshead and revolute clearance joint between the crankshaft and the connecting rod. In normal working condition, the schematic of kinematic diagram of reciprocating compressor is showed in Fig. 3(a). It is assumed that there are both a clearance in B position between the crankshaft and the connecting rod, and a subsidence of the crosshead produces because of wear.

Fig. 2Expansion, suction, compression and exhaust processes

Fig. 3Schematic of kinematic diagram of reciprocating compressor

a) Schematic of reciprocating compressor in normal working condition

b) Hypothetical rod in revolute pair with clearance

c) Schematic of reciprocating compressor with clearance in B position and subsidence of the crosshead

According to the positional relationship shown in Fig. 3, the displacement equations of crankshaft, connecting rod and crosshead in centroid position can be written as:

3

[\begin{array}{l} x_{1} y_{1} \\ x_{2} y_{2} \\ x_{3} y_{3} \end{array}] = [\begin{array}{l} r_{s} 0 0 \\ r l_{s} r_{c} \\ r l r_{c} \end{array}] [\begin{array}{l} c o s θ_{1} s i n θ_{1} \\ c o s θ_{2} s i n θ_{2} \\ c o s θ_{c} s i n θ_{c} \end{array}] .

In which $x_{i}$ and $y_{i} (i = 1,2, 3)$ are the centroid position of crankshaft, connecting rod and crosshead, respectively. $θ_{1}$ , $θ_{c}$ and $θ_{2}$ are the angle of the crankshaft, the clearance and connecting rod with the $x$ -axis, respectively. $r$ is the length of crankshaft, $l$ is the length of connecting rod and $r_{c}$ is clearance radius in B position. $r_{s}$ is the length of A joint to the centroid position of crankshaft and $l_{s}$ is the length of B joint to the centroid position of connecting rod.

According to the geometric relationship of the crank-slider mechanism, $θ_{2}$ can be calculated using:

4

θ_{2} = - s i n^{- 1} (\frac{d + r s i n θ_{1} + r_{c} s i n θ_{c}}{l}) .

In this expression, $d$ is the depth of crosshead subsidence, namely, $d = - y_{3}$ . It is clear that $θ_{2}$ is a function of $θ_{1}$ and $θ_{c}$ . Therefore, ${\dot{θ}}_{2}$ is given by:

5

{\dot{θ}}_{2} = \frac{\partial θ_{2}}{\partial θ_{1}} {\dot{θ}}_{1} + \frac{\partial θ_{2}}{\partial θ_{c}} {\dot{θ}}_{c} .

Obviously, the Eq. (4) can become:

6

r s i n θ_{1} + r_{c} s i n θ_{c} + l s i n θ_{2} + d = 0 .

In Eq. (5), $\partial θ_{2} / \partial θ_{1}$ and $\partial θ_{2} / \partial θ_{c}$ are calculated by taking $θ_{1}$ and $θ_{c}$ partial derivatives of Eq. (6), respectively, as follows:

7

r c o s θ_{1} + l c o s θ_{2} \frac{\partial θ_{2}}{\partial θ_{1}} = 0,

8

r_{c} c o s θ_{c} + l c o s θ_{2} \frac{\partial θ_{2}}{\partial θ_{c}} = 0 .

$\partial θ_{2} / \partial θ_{1}$ and $\partial θ_{2} / \partial θ_{c}$ are obtained in matrix form as:

9

[\begin{array}{l} \frac{\partial θ_{2}}{\partial θ_{1}} \\ \frac{\partial θ_{2}}{\partial θ_{c}} \end{array}] = - \frac{1}{l c o s θ_{2}} [\begin{array}{l} r c o s θ_{1} \\ r_{c} c o s θ_{c} \end{array}] .

By taking time derivatives of $x_{i}$ and $y_{i} (i = 1,2, 3)$ , the velocity equations of crankshaft, connecting rod and crosshead in centroid position can be expressed as:

10

[\begin{array}{l} {\dot{x}}_{i} \\ {\dot{y}}_{i} \end{array}] = {\dot{θ}}_{1} [\begin{array}{l} \frac{\partial x_{i}}{\partial θ_{1}} \\ \frac{\partial y_{i}}{\partial θ_{1}} \end{array}] + {\dot{θ}}_{c} [\begin{array}{l} \frac{\partial x_{i}}{\partial θ_{c}} \\ \frac{\partial y_{i}}{\partial θ_{c}} \end{array}] .

In Eq. (10), $\partial x_{i} / \partial θ_{1}$ , $\partial y_{i} / \partial θ_{1}$ , $\partial x_{i} / \partial θ_{c}$ and $\partial y_{i} / \partial θ_{c}$ are calculated by taking $θ_{1}$ and $θ_{c}$ partial derivatives of Eq. (3) as follows, respectively:

11

[\begin{array}{l} \frac{\partial x_{1}}{\partial θ_{1}} \\ \frac{\partial y_{1}}{\partial θ_{1}} \end{array}] = r_{s} [\begin{matrix} - s i n θ_{1} \\ c o s θ_{1} \end{matrix}],

12

[\begin{array}{l} \frac{\partial x_{2}}{\partial θ_{1}} \\ \frac{\partial y_{2}}{\partial θ_{1}} \end{array}] = [\begin{matrix} r & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} \\ r & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} \end{matrix}] [\begin{matrix} - s i n θ_{1} & c o s θ_{1} \\ - s i n θ_{2} & c o s θ_{2} \end{matrix}],

13

[\begin{array}{l} \frac{\partial x_{3}}{\partial θ_{1}} \\ \frac{\partial y_{3}}{\partial θ_{1}} \end{array}] = [\begin{matrix} r & l \frac{\partial θ_{2}}{\partial θ_{1}} \\ r & l \frac{\partial θ_{2}}{\partial θ_{1}} \end{matrix}] [\begin{matrix} - s i n θ_{1} & c o s θ_{1} \\ - s i n θ_{2} & c o s θ_{2} \end{matrix}],

14

[\begin{array}{l} \frac{\partial x_{1}}{\partial θ_{c}} \\ \frac{\partial y_{1}}{\partial θ_{c}} \end{array}] = [\begin{array}{l} 0 \\ 0 \end{array}],

15

[\begin{array}{l} \frac{\partial x_{2}}{\partial θ_{c}} \\ \frac{\partial y_{2}}{\partial θ_{c}} \end{array}] = [\begin{matrix} r_{c} & l_{s} \frac{\partial θ_{2}}{\partial θ_{c}} \\ r_{c} & l_{s} \frac{\partial θ_{2}}{\partial θ_{c}} \end{matrix}] [\begin{matrix} - s i n θ_{c} & c o s θ_{c} \\ - s i n θ_{2} & c o s θ_{2} \end{matrix}],

16

[\begin{array}{l} \frac{\partial x_{3}}{\partial θ_{c}} \\ \frac{\partial y_{3}}{\partial θ_{c}} \end{array}] = [\begin{matrix} r_{c} & l \frac{\partial θ_{2}}{\partial θ_{c}} \\ r_{c} & l \frac{\partial θ_{2}}{\partial θ_{c}} \end{matrix}] [\begin{matrix} - s i n θ_{c} & c o s θ_{c} \\ - s i n θ_{2} & c o s θ_{2} \end{matrix}] .

These Eqs. (11) to (16) can be expressed into a matrix as follow:

17

[\begin{matrix} \frac{\partial x_{1}}{\partial θ_{1}} & \frac{\partial y_{1}}{\partial θ_{1}} \\ \frac{\partial x_{2}}{\partial θ_{1}} & \frac{\partial y_{2}}{\partial θ_{1}} \\ \frac{\partial x_{3}}{\partial θ_{1}} & \frac{\partial y_{3}}{\partial θ_{1}} \\ \frac{\partial x_{2}}{\partial θ_{c}} & \frac{\partial y_{2}}{\partial θ_{c}} \\ \frac{\partial x_{3}}{\partial θ_{c}} & \frac{\partial y_{3}}{\partial θ_{c}} \end{matrix}] = [\begin{matrix} r_{s} & 0 & 0 \\ r & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} & 0 \\ r & l \frac{\partial θ_{2}}{\partial θ_{1}} & 0 \\ 0 & l_{s} \frac{\partial θ_{2}}{\partial θ_{c}} & r_{c} \\ 0 & l \frac{\partial θ_{2}}{\partial θ_{c}} & r_{c} \end{matrix}] [\begin{matrix} - s i n θ_{1} & c o s θ_{1} \\ - s i n θ_{2} & c o s θ_{2} \\ - s i n θ_{c} & c o s θ_{c} \end{matrix}] .

By taking time derivative of Eq. (5), the angular velocity equations of connecting rod can be given by:

18

{\ddot{θ}}_{2} = \frac{\partial^{2} θ_{2}}{\partial θ_{1}^{2}} {\dot{θ}}_{1}^{2} + 2 \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} {\dot{θ}}_{1} {\dot{θ}}_{c} + \frac{\partial^{2} θ_{2}}{\partial θ_{c}^{2}} {\dot{θ}}_{1}^{2} + {\ddot{θ}}_{c} \frac{\partial θ_{2}}{\partial θ_{c}} + {\ddot{θ}}_{1} \frac{\partial θ_{2}}{\partial θ_{1}} .

In Eq. (18), $\partial^{2} θ_{2} / \partial θ_{1}^{2}$ , $\partial^{2} θ_{2} / \partial θ_{C}^{2}$ and $\partial^{2} θ_{2} / \partial θ_{c} \partial θ_{1}$ are calculated by taking $θ_{1}$ and $θ_{c}$ partial derivatives of Eq. (9), respectively, as follows:

19

\frac{\partial^{2} θ_{2}}{\partial θ_{1}^{2}} = \frac{r s i n θ_{1} + l s i n θ_{2} {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2}}{l c o s θ_{2}},

20

\frac{\partial^{2} θ_{2}}{\partial θ_{1}^{2}} = \frac{r {}_{c} l s i n θ_{c} (c o s θ_{2})^{2} + (r_{c} c o s θ_{c})^{2} s i n θ_{2}}{l^{2} (c o s θ_{c})^{3}},

21

\frac{\partial^{2} θ_{2}}{\partial θ_{c} \partial θ_{1}} = \frac{r . r_{c} . s i n θ_{2} . c o s θ_{1} . c o s θ_{c}}{l^{2} (c o s θ_{2})^{2}} .

The acceleration equations of crankshaft, connecting rod and crosshead in centroid position can be solved by taking time derivative of Eq. (10) as follow:

22

[\begin{array}{l} {\ddot{x}}_{i} \\ {\ddot{y}}_{i} \end{array}] = {\dot{θ}}_{1}^{2} [\begin{array}{l} \frac{\partial^{2} x_{i}}{\partial {θ_{1}}^{2}} \\ \frac{\partial^{2} y_{i}}{\partial {θ_{1}}^{2}} \end{array}] + 2 {\dot{θ}}_{1} {\dot{θ}}_{c} [\begin{array}{l} \frac{\partial^{2} x_{i}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} y_{i}}{\partial θ_{1} \partial θ_{c}} \end{array}] + {\ddot{θ}}_{c} [\begin{array}{l} \frac{\partial x_{i}}{\partial θ_{c}} \\ \frac{\partial y_{i}}{\partial θ_{c}} \end{array}] + {\dot{θ}}_{c}^{2} [\begin{array}{l} \frac{\partial^{2} x_{i}}{\partial θ_{c}^{2}} \\ \frac{\partial^{2} y_{i}}{\partial θ_{c}^{2}} \end{array}], (i = 1,2, 3),

where $\partial^{2} x_{i} / \partial θ_{1}^{2}$ , $\partial^{2} y_{i} / \partial θ_{1}^{2}$ , $\partial^{2} x_{i} / \partial θ_{1} \partial θ_{c}$ , $\partial^{2} y_{i} / \partial θ_{1} \partial θ_{c}$ , $\partial^{2} x_{i} / \partial θ_{c}^{2}$ and $\partial^{2} y_{i} / \partial θ_{c}^{2}$ can be determined using the following equations from Eqs. (23) to (31).

$\partial^{2} x_{1} / \partial θ_{1}^{2}$ and $\partial^{2} y_{1} / \partial θ_{1}^{2}$ are calculated by taking $θ_{1}$ derivative of Eq. (11) as follow:

23

[\begin{array}{l} \frac{\partial^{2} x_{1}}{\partial θ_{1}^{2}} \\ \frac{\partial^{2} y_{1}}{\partial θ_{1}^{2}} \end{array}] = r_{s} [\begin{array}{l} - c o s θ_{1} \\ - s i n θ_{1} \end{array}] .

$\partial^{2} x_{2} / \partial θ_{1}^{2}$ and $\partial^{2} y_{2} / \partial θ_{1}^{2}$ are computed by taking $θ_{1}$ derivative of Eq. (12) as follow:

24

[\begin{array}{l} \frac{\partial^{2} x_{2}}{\partial θ_{1}^{2}} \\ \frac{\partial^{2} y_{2}}{\partial θ_{1}^{2}} \end{array}] = - [\begin{matrix} r & l_{s} \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{1}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} \\ r & - l_{s} \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{1}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} \end{matrix}] [\begin{matrix} c o s θ_{1} & s i n θ_{1} \\ s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \end{matrix}] .

$\partial^{2} x_{3} / \partial θ_{1}^{2}$ and $\partial^{2} y_{3} / \partial θ_{1}^{2}$ can be deduced by taking $θ_{1}$ derivative of Eq. (13) as follow:

25

[\begin{array}{l} \frac{\partial^{2} x_{3}}{\partial θ_{1}^{2}} \\ \frac{\partial^{2} y_{3}}{\partial θ_{1}^{2}} \end{array}] = - [\begin{matrix} r & l \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{1}} & l {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} \\ r & - l \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{1}} & l {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} \end{matrix}] [\begin{matrix} c o s θ_{1} & s i n θ_{1} \\ s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \end{matrix}] .

$\partial^{2} x_{1} / \partial θ_{1} \partial θ_{c}$ and $\partial^{2} y_{1} / \partial θ_{1} \partial θ_{c}$ are expressed by taking $θ_{c}$ derivative of Eq. (11) as follow:

26

[\begin{array}{l} \frac{\partial^{2} x_{1}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} y_{1}}{\partial θ_{1} \partial θ_{c}} \end{array}] = [\begin{array}{l} 0 \\ 0 \end{array}] .

$\partial^{2} x_{2} / \partial θ_{1} \partial θ_{c}$ and $\partial^{2} y_{2} / \partial θ_{1} \partial θ_{c}$ are defined by taking $θ_{c}$ derivative of Eq. (12) as follow:

27

[\begin{array}{l} \frac{\partial^{2} x_{2}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} y_{2}}{\partial θ_{1} \partial θ_{c}} \end{array}] = - [\begin{matrix} l_{s} \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} \\ - l_{s} \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} \end{matrix}] [\begin{matrix} s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \end{matrix}] .

$\partial^{2} x_{3} / \partial θ_{1} \partial θ_{c}$ and $\partial^{2} y_{3} / \partial θ_{1} \partial θ_{c}$ are computed by taking $θ_{c}$ derivative of Eq. (13) as follow

28

[\begin{array}{l} \frac{\partial^{2} x_{3}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} y_{3}}{\partial θ_{1} \partial θ_{c}} \end{array}] = - [\begin{matrix} l \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} \\ - l \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} \end{matrix}] [\begin{matrix} s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \end{matrix}] .

$\partial^{2} x_{1} / \partial θ_{c}^{2}$ and $\partial^{2} y_{1} / \partial θ_{c}^{2}$ are calculated by taking $θ_{c}$ derivative of Eq. (14) as follow:

29

[\begin{array}{l} \frac{\partial^{2} x_{1}}{\partial θ_{c}^{2}} \\ \frac{\partial^{2} y_{1}}{\partial θ_{c}^{2}} \end{array}] = [\begin{array}{l} 0 \\ 0 \end{array}] .

$\partial^{2} x_{2} / \partial θ_{c}^{2}$ and $\partial^{2} y_{2} / \partial θ_{c}^{2}$ can be deduced by taking $θ_{c}$ derivative of Eq. (15) as follow:

30

[\begin{array}{l} \frac{\partial^{2} x_{2}}{\partial θ_{c}^{2}} \\ \frac{\partial^{2} y_{2}}{\partial θ_{c}^{2}} \end{array}] = - [\begin{matrix} l_{s} \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{c}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{c}})}^{2} & r_{c} \\ - l_{s} \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{c}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{c}})}^{2} & r_{c} \end{matrix}] [\begin{matrix} s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \\ c o s θ_{c} & s i n θ_{c} \end{matrix}] .

$\partial^{2} x_{3} / \partial θ_{c}^{2}$ and $\partial^{2} y_{3} / \partial θ_{c}^{2}$ are calculated by taking $θ_{c}$ derivative of Eq. (16) as follow:

31

[\begin{array}{l} \frac{\partial^{2} x_{3}}{\partial θ_{c}^{2}} \\ \frac{\partial^{2} y_{3}}{\partial θ_{c}^{2}} \end{array}] = - [\begin{matrix} l \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{c}} & l {(\frac{\partial θ_{2}}{\partial θ_{c}})}^{2} & r_{c} \\ - l \frac{\partial^{2} θ_{2}}{\partial^{2} θ_{c}} & l {(\frac{\partial θ_{2}}{\partial θ_{c}})}^{2} & r_{c} \end{matrix}] [\begin{matrix} s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \\ c o s θ_{c} & s i n θ_{c} \end{matrix}] .

These Eqs. (23) to (31) can be written into a matrix as follow:

32

[\begin{array}{l} \frac{\partial^{2} x_{1}}{\partial θ_{1}^{2}} & \frac{\partial^{2} y_{1}}{\partial θ_{1}^{2}} \\ \frac{\partial^{2} x_{2}}{\partial θ_{1}^{2}} & \frac{\partial^{2} y_{2}}{\partial θ_{1}^{2}} \\ \frac{\partial^{2} x_{2}}{\partial θ_{1} \partial θ_{c}} & \frac{\partial^{2} y_{2}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} x_{2}}{\partial θ_{c}^{2}} & \frac{\partial^{2} y_{2}}{\partial θ_{c}^{2}} \\ \frac{\partial^{2} x_{3}}{\partial {θ_{1}}^{2}} & \frac{\partial^{2} y_{3}}{\partial {θ_{1}}^{2}} \\ \frac{\partial^{2} x_{3}}{\partial θ_{1} \partial θ_{c}} & \frac{\partial^{2} y_{3}}{\partial θ_{1} \partial θ_{c}} \\ \frac{\partial^{2} x_{3}}{\partial θ_{c}^{2}} & \frac{\partial^{2} y_{3}}{\partial θ_{c}^{2}} \end{array}] = [\begin{array}{l} r_{s} & 0 & 0 & 0 \\ r & \pm l_{s} \frac{\partial^{2} θ_{2}}{\partial θ_{1}^{2}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} & 0 \\ 0 & \pm l_{s} \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l_{s} \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} & 0 \\ 0 & \pm l_{s} \frac{\partial^{2} θ_{2}}{\partial θ_{c}^{2}} & l_{s} {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} & r_{c} \\ r & \pm l \frac{\partial^{2} θ_{2}}{\partial θ_{1}^{2}} & l {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} & 0 \\ 0 & \pm l \frac{\partial^{2} θ_{2}}{\partial θ_{1} \partial θ_{c}} & l \frac{\partial θ_{2}}{\partial θ_{1}} \frac{\partial θ_{2}}{\partial θ_{c}} & 0 \\ 0 & \pm l \frac{\partial^{2} θ_{2}}{\partial θ_{c}^{2}} & l {(\frac{\partial θ_{2}}{\partial θ_{1}})}^{2} & r_{c} \end{array}] \times [\begin{matrix} c o s θ_{1} & s i n θ_{1} \\ s i n θ_{2} & c o s θ_{2} \\ c o s θ_{2} & s i n θ_{2} \\ c o s θ_{c} & s i n θ_{c} \end{matrix}] .

In Eq. (32), The meaning of the “±” is that “+” and “-” represent the symbol of the first column and the second column of the solved matrix, respectively.

In addition, it is easily obtained as follows:

33

\frac{\partial^{2} x_{1}}{\partial θ_{1} \partial θ_{c}} = \frac{\partial^{2} y_{1}}{\partial θ_{1} \partial θ_{c}} = \frac{\partial^{2} x_{1}}{\partial {θ_{c}}^{2}} = \frac{\partial^{2} y_{1}}{\partial {θ_{c}}^{2}} = \frac{\partial x_{_{1}}}{\partial θ_{c}} = \frac{\partial y_{1}}{\partial θ_{c}}

= \frac{\partial y_{3}}{\partial θ_{1}} = \frac{\partial y_{3}}{\partial θ_{c}} = \frac{\partial^{2} y_{3}}{\partial {θ_{1}}^{2}} = \frac{\partial^{2} y_{3}}{\partial θ_{1} \partial θ_{c}} = \frac{\partial^{2} y_{3}}{\partial {θ_{c}}^{2}} = 0 .

2.3. Equations of dynamics

Lagrange motion equation for an unconstrained dynamical system is as follow:

34

\frac{d}{d t} (\frac{\partial E}{\partial {\dot{q}}_{j}}) - \frac{\partial E}{\partial q_{j}} + \frac{\partial U}{\partial q_{j}} = Q_{j}, (j = 1,2),

where $E$ and $U$ are the system kinetic and potential energies, respectively. $Q_{j}$ is the nonconservative generalized force corresponding to the generalized coordinate $q_{j}$ , and can be calculated as:

35

Q_{j} = \sum_{i = 1}^{3} {\vec{F}}_{i}^{*} . \frac{\partial {\vec{V}}_{i}}{\partial {\dot{q}}_{j}} + {\vec{M}}_{i}^{*} . \frac{\partial {\vec{ω}}_{i}}{\partial {\dot{q}}_{j}} .

In Eq. (35), ${\vec{F}}_{i}^{*}$ is the resultant of external force acting at the center of mass. ${\vec{M}}_{i}^{*}$ is the external torque acting on body $i$ . ${\vec{V}}_{i}$ and ${\vec{ω}}_{i}$ are the translational and rotational velocity for the mass center of body $i$ , respectively.

Taking the crankshaft, connecting rod and crosshead of the reciprocating compressor as a system, the kinetic energy and potential energy of the system are:

36

\{\begin{array}{l} E = \sum_{i = 1}^{3} E_{i} = \sum_{i = 1}^{3} \frac{1}{2} m_{i} ({\dot{x}}_{i}^{2} + {\dot{y}}_{i}^{2}) + \sum_{i = 1}^{2} \frac{1}{2} J_{i} {\dot{θ}}_{i}^{2}, \\ U = \sum_{i = 1}^{2} m_{i} g y_{i} . \end{array}

Substituting Eq. (36) into Eq. (34) leads to:

37

\sum_{i = 1}^{2} J_{i} {\ddot{θ}}_{i} \frac{\partial θ_{i}}{\partial q_{j}} + \sum_{i = 1}^{3} m_{i} ({\ddot{x}}_{i} \frac{\partial x_{i}}{\partial q_{j}} + {\ddot{y}}_{i} \frac{\partial y_{i}}{\partial q_{j}}) + g \sum_{i = 1}^{3} m_{i} \frac{\partial y_{i}}{\partial q_{j}} = Q_{j} .

Substitute Eqs. (18) and (22) into Eq. (37). Because the crankshaft works for uniform rotation, the angular acceleration of crankshaft equals zero, Namely, ${\ddot{θ}}_{1} =$ 0. Therefore, differential equation about ${\ddot{θ}}_{c}$ can be written as:

38

A \cdot {\ddot{θ}}_{c} = B \cdot {\dot{θ}}_{c} + C \cdot {\dot{θ}}_{c}^{2} + D,

where A, B, C and D are expressed as:

39

A = J_{2} {(\frac{\partial θ_{2}}{\partial θ_{c}})}^{2} + \sum_{i = 1}^{3} m_{i} [{(\frac{\partial x_{i}}{\partial θ_{c}})}^{2} + {(\frac{\partial y_{i}}{\partial θ_{c}})}^{2}],

40

B = - 2 ω [J_{2} \frac{\partial θ_{2}}{\partial θ_{c}} \cdot \frac{\partial^{2} θ_{2}}{\partial θ_{c} \partial θ_{1}} + \sum_{i = 1}^{3} m_{i} (\frac{\partial x_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} x_{i}}{\partial θ_{1} \partial θ_{c}} + \frac{\partial y_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} y_{i}}{\partial θ_{1} \partial θ_{c}})],

41

C = - [J_{2} \frac{\partial θ_{2}}{\partial θ_{c}} \cdot \frac{\partial^{2} θ_{2}}{\partial θ_{c}^{2}} + \sum_{i = 1}^{3} m_{i} (\frac{\partial x_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} x_{i}}{\partial θ_{c}^{2}} + \frac{\partial y_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} y_{i}}{\partial θ_{c}^{2}})],

42

D = Q_{2} - [J_{2} \frac{\partial^{2} θ_{2}}{\partial θ_{1}} \cdot \frac{\partial θ_{2}}{\partial θ_{c}} + \sum_{i = 1}^{3} m_{i} (\frac{\partial x_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} x_{i}}{\partial θ_{1}^{2}} + \frac{\partial y_{i}}{\partial θ_{c}} \cdot \frac{\partial^{2} y_{i}}{\partial θ_{1}^{2}})] ω^{2} - g \sum_{i = 1}^{3} m_{i} \frac{\partial y_{i}}{\partial θ_{c}} .

Obviously, Eq. (38) is a nonlinear equation.

It is supposed that the centroid of connecting rod is middle position, that is to say, $l = 2 l_{s}$ . Moreover, since the clearance size $r_{c}$ is very small, it can be considered the expression $r_{c} . x + y \approx y$ , where $x$ and $y$ are two expressions that are roughly the same order of magnitude. Substituting Eqs. (9), (17), (19)-(21) and (32) into Eqs. (39)-(42), respectively. The expressions of $A$ , $B$ , $C$ and $D$ can be expressed as follows:

43

A = (a_{1} + \frac{a_{2}}{4}) {(\frac{c o s θ_{c}}{c o s θ_{2}})}^{2} + a_{2} + a_{2} c o s θ_{c} (s i n θ_{c} t a n θ_{2} - c o s θ_{c})

+ a_{3} (t a n θ_{2} c o s θ_{c} - s i n θ_{c})^{2},

where $a_{i} (i = 1, 2, 3)$ are constants, $a_{1} = J_{2} {(r_{c} / l)}^{2}$ , $a_{2} = m_{2} {r_{c}}^{2}$ , $a_{3} = m_{3} {r_{c}}^{2}$ :

44

B = \frac{c o s θ_{1} c o s θ_{c}}{c o s^{4} θ_{2}} [b_{1} s i n θ_{2} c o s θ_{1} + b_{2} s i n (θ_{2} + θ_{c}) + (b_{3} + b_{4}) s i n (θ_{c} - θ_{2})] .

In which, $b_{i} (i = 1, 2, 3, 4)$ are constants, $b_{1} = - 2 ω J_{2} {r_{c}}^{2} r / l^{3},$ $b_{2} = - m_{2} r {r_{c}}^{2} ω / 4 l,$ $b_{3} = 3 b_{2}$ , $b_{4} = - 2 m_{3} r {r_{c}}^{2} ω$ :

45

C = \frac{1}{c o s^{2} θ_{2}} [c_{1} s i n θ_{c} + c_{2} (\frac{5}{16} c o s 2 θ_{2} s i n 2 θ_{c} - \frac{1}{4} c o s 2 θ_{c} s i n 2 θ_{2}) + c_{3} s i n 2 θ_{2}] - \frac{c_{2}}{8} s i n 2 θ_{c} .

In which, $c_{i} (i = 1,2, 3)$ are constants, $c_{1} = - J_{2} {r_{c}}^{2} / 2 l^{2} + 3 c_{2} / 16 - c_{3},$ $c_{2} = m_{2} {r_{c}}^{2},$ $c_{3} = - m_{3} {r_{c}}^{2} / 2$ :

46

\begin{array}{l} D = d_{1} (- s i n θ_{c} + t a n θ_{2} c o s θ_{c}) - [\frac{d_{2} c o s θ_{c}}{c o s^{4} θ_{2}} (l c o s^{2} θ_{2} s i n θ_{1} + r s i n θ_{2} c o s^{2} θ_{1}) \\ + d_{3} s i n (θ_{c} - θ_{2}) \cdot \frac{c o s θ_{1}}{c o s θ_{2}} + d_{4} (t a n θ_{2} s i n θ_{1} + \frac{r c o s^{2} θ_{1}}{l c o s^{3} θ_{2}}) \\ + d_{5} (s i n θ_{c} c o s θ_{1} + s i n (θ_{c} - θ_{1}))], \end{array}

where:

47

d_{0} = ω^{2} r r_{c} d_{1} = P \cdot r_{c}, d_{2} = \frac{d_{0} J_{2}}{l^{2}}, d_{3} = d_{0} (\frac{m_{2}}{2} + m_{3}),

d_{4} = d_{0} (\frac{m_{2}}{4} + m_{3} + \frac{m_{2}}{4} s i n θ_{c}), d_{5} = \frac{d_{0} m_{2}}{4} .

3. Numerical simulation and dynamic responses analysis

In this previous section, the numerical solution of the clearance angle $θ_{c}$ is solved by the Runge-Kutta method according to the Eqs. (38) and (4). Subsequently, the displacement, velocity and acceleration of the crosshead are also obtained accordingly in the horizontal direction. In this section, we discuss the influence of clearance, subsidence and rotation speed of the crankshaft. Taking the 2D12 model of reciprocating compressor as the research object, the simulation characteristics are presented in Table 1. In addition, the centroids of crankshaft and connecting rod are middle position.

Table 1Dimension for the 2D12 model of reciprocating compressor

Parts	Length (m)	Mass (kg)	Moment of inertia (kg.m²)
Crankshaft	0.12	1	0.0012
Connecting rod	0.6	5	0.15
Crosshead	–	1	–

3.1. Dynamic response of reciprocating compressor system with different clearance sizes

In this subsection, from the perspective of dynamic response, the effects of the reciprocating compressor with different clearance sizes are investigated under the conditions of without subsidence, crankshaft angular velocity 20 rad/s and variable cylinder load shown in Fig. 2. In this study, the revolute joint between the crankshaft and the linkage is used as the clearance for the research. The displacement, velocity, acceleration and acceleration spectrum of the crosshead without/with 0.1 mm, 0.5 mm and 5 mm clearance sizes are shown in Figs. 4 to 7, respectively. It is noteworthy that the clearance size is exaggerated to 5 mm so as to better investigate the dynamics response of the variational clearance sizes for the reciprocating compressor.

Fig. 4Dynamic responses of crosshead without clearance

As can be seen from Figs. 4 to 7, with the increase of clearance sizes, the effects of displacement, velocity, and acceleration increase. It can be observed that the crosshead velocity and acceleration fluctuate more violently than the crosshead displacement. Furthermore, Fig. 4(d), 5(d), 6(d) and 7(d) show the acceleration spectrum using FFT transformation. In Fig. 4(d), it is clear that 3.109 Hz which is the rotational frequency of crankshaft and 6.217 Hz which is two times rotational frequency of crankshaft are displayed without clearance. In Fig. 5(d), In addition to 3.109 Hz and 6.217 Hz, there are very weak other frequency components with 0.1 mm clearance size, and it is distinct that the amplitudes of the other frequency components are lower than 6.217 Hz. In Fig. 6(d), except 3.109 Hz and 6.217 Hz, the other frequency components are obvious with 0.5 mm clearance size, and it is evident that the amplitudes of some other frequency components are higher than 6.217 Hz, but are lower than 3.109 Hz. It can be found that there are 113.5 Hz frequency component and approximate multiplier such as 223.1 Hz and 330.3 Hz in other frequency components. In Fig. 7(d), apart from 3.109 Hz and 6.217 Hz, the other frequency components are extremely obvious with 5mm clearance size, and appear 148.4 Hz frequency component and approximate multiplier such as 287.6 Hz and 448.4 Hz. It is noteworthy that the amplitudes of some other frequency components are higher than 3.109 Hz. Therefore, the results show that besides rotational frequency of crankshaft, the larger the clearance sizes are, the more obvious the other frequency components are, even beyond the amplitude of the rotational frequency components of the crankshaft.

Fig. 5Dynamic responses of crosshead with 0.1 mm clearance

Fig. 6Dynamic responses of crosshead with 0.5 mm clearance

The comparison of response curves of displacement, velocity and acceleration is demonstrated in Figs. 8 to 10, respectively. It can be seen from Figs. 8 to 10 that the variational clearance does not influence the crosshead displacement in a remarkable way, and the crosshead displacement and velocity of the reciprocating compressor without clearance are generally consistent with those of the reciprocating compressor with a different clearance size. When the clearance sizes increase from 0.1 mm to 1 mm, the corresponding maximal deviation values of the displacement increase from the 0.1 mm to 1.0 mm at the low dead point, and the maximal deviation values of velocity increase from 0.002 m/s to 0.042 m/s. In vivid contrast, the crosshead acceleration is dramatically influenced by the clearance sizes and the maximal peak values of crosshead acceleration increase from 77.68 m/s²to 402.6 m/s².

When the clearance size is exaggerated to 5 mm, the corresponding maximal deviation value of the displacement increases to 4.9 mm at the low dead point, and the maximal deviation value of velocity increases to 0.959 m/s, and the maximal peak value of crosshead acceleration increases to 1164 m/s². Distinctly, 5 mm clearance size creates a large vibration response to the crosshead, which is likely to cause the reciprocating compressor system to collapse.

Fig. 7Dynamic responses of crosshead with 5 mm clearance

Fig. 8Comparison of crosshead displacement with different clearance sizes

Fig. 9Comparison of crosshead velocity with different clearance sizes

Fig. 10Comparison of crosshead acceleration with different clearance sizes

3.2. Influence of the crosshead subsidence

As reciprocating compressor works for a period of time, there may be wear between the crosshead and the side of the cylinder, which may cause the crosshead to sink. That is to say, the crosshead produces decentration. Obviously, the crosshead subsidence will exacerbate the vibration of the crosshead and transfer it to the reciprocating compressor body. In this subsection, the influences of subsidence sizes on the dynamic behavior of reciprocating compressor with subsidence of the crosshead are discussed under the conditions of clearance size 1mm, crankshaft angular velocity 20 rad/s and variable cylinder load shown in Fig. 2. The displacement, velocity, and acceleration of the crosshead without/with 0.1 mm, 1 mm and 5 mm subsidence sizes are shown in Figs. 11 to 13, respectively. It is noteworthy that in order to better research the dynamic response of the variational subsidence sizes to the reciprocating compressor, the subsidence size is also exaggerated to 5 mm.

Fig. 11Comparison of crosshead displacement with different subsidence sizes

As can be seen from Figs. 11 to 13, the existence of the subsidence brings a very weak impact for the crosshead displacement, and does not produce strongly effect on the crosshead velocity and acceleration with different subsidence sizes. With the increase in subsidence sizes, as the subsidence sizes increase from 0 mm to 1 mm, the corresponding maximal deviation values of the displacement increase from 0 mm to 0.4 mm at the low dead point, and the maximal deviation values of velocity increase from 0 m/s to 0.059 m/s, and the maximal peak values of crosshead acceleration increase from 402.6 m/s²to 548.1 m/s².

When the subsidence size is exaggerated to 5 mm, the corresponding maximal deviation value of the displacement increases to 0.7 mm at the low dead point, and the maximal deviation value of velocity increases to 0.312 m/s, and the maximal peak value of crosshead acceleration increases to 772.4 m/s². Compared with the dynamic response of without subsidence size, the 5 mm subsidence size increases the slight fluctuation. Thus, the varying subsidence sizes do not have a significant impact on the reciprocating compressor system. The reason may be that in this paper, the flexibility of the connecting rod between the crosshead and the piston is not considered. So, it reduces the impact of the crosshead on the reciprocating compressor.

Distinctly, compared with the effect of the clearance sizes, the oscillating range of crosshead displacement, velocity and acceleration are smaller with subsidence sizes. That is to say, the influence of the clearance is much stronger than the subsidence of the crosshead in the horizontal direction.

Fig. 12Comparison of crosshead velocity with different subsidence sizes

Fig. 13Comparison of crosshead acceleration with different subsidence sizes

3.3. Influence of the input crankshaft angular velocity

In this subsection, the influence of the input crankshaft speed on the dynamic behavior of the reciprocating compressor is reported. In addition, in order to fully understand the dynamic behavior of the crankshaft at the low speed, medium speed and high speed, dynamic responses of the crosshead from 10 rad/s to 150 rad/s are analyzed under the conditions of subsidence 1 mm, clearance size 1 mm and variable cylinder load shown in Fig. 2, as showed in Fig. 14 to 16, respectively.

It is can be seen from Figs. 14 to 16, the changes of the crankshaft angular velocity do not influence the crosshead displacement in a conspicuous manner, but produce evident effects for the crosshead velocity and acceleration. When the crankshaft angular velocities increase from 10 rad/s to 150 rad/s, the corresponding maximal values of the displacement increase from 480.6 mm to 481.1 mm at the low dead point, and the maximal values of the velocity increase from 1.267 m/s to 20.14 m/s, and the maximal peak values of crosshead acceleration increase from 172.7 m/s²to 16010 m/s². In addition, as can be seen from Fig. 14(d), Fig. 15(d) and Fig. 16(d), with the increase in the crankshaft angular velocity, besides rotational frequency of crankshaft, the lower the crankshaft angular velocities are, the more obvious the other frequency components are, even beyond the amplitude of the rotational frequency components.

Fig. 14Dynamic responses of crosshead with the crankshaft speed 10 rad/s

Fig. 15Dynamic responses of crosshead with the crankshaft angular velocity 70 rad/s

When the crankshaft angular velocity is 10 rad/s, except 1.554 Hz which is the rotational frequency of crankshaft and 3.109 Hz which is the double rotational frequency, there are still some other remarkable frequency components that almost submerge the rotational frequency of crankshaft. One can observe 167.9 Hz frequency component and approximate multiplier such as 337.3 Hz in some other frequency components. When the crankshaft angular velocity is 70 rad/s, in addition to the rotational frequency 10.88 Hz and double rotational frequency 22.44 Hz, there are very weak other frequency components, and it is distinct that the amplitudes of the other frequency components are lower than 22.44 Hz. When the crankshaft angular velocity is 150 rad/s, the rotational frequency 24.04 Hz and double rotational frequency 48.04 Hz are more significant than the other frequency components which can be ignored.

Fig. 16Dynamic responses of crosshead with the crankshaft angular velocity 150 rad/s

4. Chaos analysis

Data obtained from a deterministic system can be classified as either periodic or non-periodic data [29]. Non-periodic data may correspond to a quasi-periodic, transient or chaotic motion. Lyapunov exponents produce a method that can distinguish the chaotic and non-chaotic (periodic or quasi-periodic) behavior. Periodic attractors show only negative and zero exponents which indicate convergence to a predictable motion, whereas there is at least one positive exponent for a chaotic system [30, 31]. Hence, one needs to determine the sign of Lyapunov exponents to characterize the behavior of a system. In this section, nonlinear dynamic analysis of the reciprocating compressor crosshead is investigated. We discuss the chaotic and non-chaotic behavior of the crosshead using phase trajectories, Lyapunov exponents and Poincaré section under the different clearance sizes, subsidence sizes and crankshaft angular velocities.

Fig. 17 shows the phase trajectories of displacement-velocity and velocity-acceleration for the crosshead when the reciprocating compressor has neither clearance nor subsidence. Obviously, under such ideal conditions reciprocating compressor has regular periodic motion.

Fig. 17The phase trajectories of displacement-velocity and velocity-acceleration without clearance and subsidence

a)

b)

Fig. 18 and Fig. 19 show that the phase trajectories of displacement-velocity and |velocity-acceleration for the crosshead under the conditions of subsidence size 1 mm, crankshaft angular velocity 20 rad/s and variable cylinder load with 0.1 mm, 0.5 mm,1 mm and 5 mm clearance sizes, respectively. It is noteworthy that in order to better investigate the dynamic behavior of the varying clearance size to the reciprocating compressor, the clearance size is exaggerated to 5 mm.

It is can be seen from Fig. 18 and Fig. 19, the change of the clearance sizes produces evident effect for the shape of phase trajectories. With the increase of the clearance sizes, the phase trajectories of velocity–acceleration are more and more like the $\infty$ -character. Fig. 24(a) shows all calculated Lyapunov exponents by Wolf [32] method for the crosshead acceleration with 0.1 mm, 0.5 mm, 1 mm and 5 mm clearance sizes. The largest Lyapunov exponents $λ_{i}$ have been calculated for clearance sizes $r c_{1} =$ 0.1 mm, $r c_{2} =$ 0.5 mm, $r c_{3} =$ 1 mm and $r c_{4} =$ 5 mm. The values of the largest Lyapunov exponents are $λ_{1} =$ 1.57 to the corresponding $r c_{1} =$ 0.1 mm, $λ_{2} =$ 0.68 to the corresponding $r c_{2} =$ 0.5 mm, $λ_{3} =$ 0.62 to the corresponding $r c_{3} =$ 1 mm, and $λ_{4} =$ 0.59 to the corresponding $r c_{4} =$ 5 mm. One can see a decrease in values of the largest Lyapunov exponents as the clearance sizes increase, but the downward trend is gradually slowed down.

Fig. 18The phase trajectories of displacement-velocity with different clearance sizes: a) 0.1 mm, b) 0.5 mm, c) 1 mm, d) 5 mm

Fig. 19The phase trajectories of velocity-acceleration with different clearance sizes: a) 0.1 mm, b) 0.5 mm, c) 1 mm, d) 5 mm

Fig. 20 and Fig. 21 show that the phase trajectories of displacement-velocity and velocity-acceleration for the crosshead under the conditions of clearance size 1 mm, crankshaft angular velocity 20 rad/s and variable cylinder load with 0 mm, 0.1 mm, 1 mm and 5 mm subsidence sizes, respectively. It is noteworthy that in order to better study the dynamic behavior of the varying subsidence size to the reciprocating compressor, the subsidence size is also exaggerated to 5 mm.

As can be seen from Fig. 20 and Fig. 21, the changes of the subsidence sizes produce weak influence for the shape of phase trajectory. It is visible that the phase trajectory of the crosshead vibration does not close for each revolution. Fig. 24(b) shows all calculated Lyapunov exponents for the crosshead acceleration with 0 mm, 0.1mm, 1 mm and 5 mm subsidence sizes. The largest Lyapunov exponents $λ_{i}$ have been computed for subsidence sizes $d_{1} =$ 0 mm, $d_{2} =$ 0.1 mm, $d_{3} =$ 1 mm and $d_{4} =$ 5 mm. The values of the largest Lyapunov exponents are $λ_{1} =$ 0.51 to the corresponding $d_{1} =$ 0 mm, $λ_{2} =$ 0.53 to the corresponding $d_{2} =$ 0.1 mm, $λ_{3} =$ 0.62 to the corresponding $d_{3} =$ 1 mm, and $λ_{4} =$ 0.52 to the corresponding $d_{4} =$ 5 mm.

Fig. 20The phase trajectories of displacement-velocity with different subsidence sizes: a) 0 mm, b) 0.1 mm, c) 1 mm, d) 5 mm

Fig. 21The phase trajectories of velocity-acceleration with different subsidence sizes: a) 0 mm, b) 0.1 mm, c) 1 mm, d) 5 mm

Fig. 22The phase trajectories of displacement–velocity with different angular velocities: a) 10 rad/s, b) 20 rad/s, c) 70 rad/s, d) 150 rad/s

Fig. 23The phase trajectories of velocity-acceleration with different angular velocities: a) 10 rad/s, b) 20 rad/s, c) 70 rad/s, d) 150 rad/s

Fig. 22 and Fig. 23 show that the phase trajectories of displacement-velocity and velocity-acceleration for the crosshead under the conditions of clearance size 5 mm, subsidence size 1 mm and variable cylinder load with 10 rad/s, 20 rad/s, 70 rad/s and 150 rad/s crankshaft angular velocities, respectively. It is can be seen from Fig. 22 and Fig. 23, the changes of the crankshaft angular velocity produce remarkable effects on the shape of phase trajectories，the higher the crankshaft angular velocity, the more regular the trajectory. In addition, with the decrease of the crankshaft angular velocities, the phase trajectories of velocity-acceleration are more and more like the $\infty$ -character. Fig. 24(c) shows all calculated Lyapunov exponents for the crosshead acceleration with 10 rad/s, 20 rad/s, 70 rad/s and 150 rad/s crankshaft angular velocities. The largest Lyapunov exponents $λ_{i}$ have been computed for crankshaft angular velocities $ω_{11} =$ 10 rad/s, $ω_{12} =$ 20 rad/s, $ω_{13} =$ 70 rad/s and $ω_{14} =$ 150 rad/s. The values of the largest Lyapunov exponents are $λ_{1} =$ 0.97 to the corresponding $ω_{11} =$ 10 rad/s, $λ_{2} =$ 0.59 to the corresponding $ω_{12} =$ 20 rad/s, $λ_{3} =$ 0.23 to the corresponding $ω_{13} =$ 70 rad/s, and $λ_{4} =$ 1.5 to the corresponding $ω_{14} =$ 150 rad/s.

Fig. 24Lyapunov exponents with different clearance sizes, subsidence sizes and angular velocities

a) Lyapunov exponents with different clearance sizes

b) Lyapunov exponents with different subsidence sizes

c) Lyapunov exponents with different angular velocities

Obviously, the signs of the largest Lyapunov exponents are positive for different clearance sizes, subsidence sizes and angular velocities, indicating the exponential separation of nearby trajectories as time evolves, that is to say, the reciprocating compressor system is characterized by chaotic behavior with the faults of clearance and subsidence. Therefore, one can deduce at this point the chaotic behavior of the reciprocating compressor system. The trajectories shown in figure are associated with the motion around the attractor and show the classical characteristics of chaotic motion.

In addition, in order to better analyze the chaos of the reciprocating compressor system, the Poincaré section method is applied in this study. Figs. 25 to 28 are the Poincaré portraits corresponding to Figs. 17, 19, 21 and 23, respectively. Whether there is chaos in a system can be judged by observing the intercept point on the Poincare section. When the Poincare section has and has only one fixed point or a few discrete points, the movement is periodic. When the Poincare section is a closed curve, the movement is quasi-periodic. When the Poincare section is a piece of dense points with a fractal structure, the movement is chaos.

As illustrated in Fig. 25, When the reciprocating compressor system does not have clearance and subsidence, the Poincare sections have only one fixed point, which indicates that the reciprocating compressor is a periodic system in the absence of fault. However, as can be seen from Figs. 26 to 28, obviously, the reciprocating compressor system of the single cylinder with clearance and subsidence has chaotic behavior, which is consistent with the judgment result of the maximum Lyapunov index.

Fig. 25The Poincaré portraits of displacement-velocity and velocity-acceleration without clearance and subsidence

a) Crosshead displacement (m)

b) Crosshead velocity (m/s)

Fig. 26The Poincaré portraits for (velocity, acceleration) with different clearance sizes: a) 0.1 mm, b) 0.5 mm, c) 1 mm, d) 5 mm

Fig. 27The Poincaré portraits for (velocity, acceleration) with different subsidence sizes: a) 0 mm, b) 0.1 mm, c) 1 mm, d) 5 mm

Fig. 28The Poincaré portraits for (velocity, acceleration) with different angular velocities: a) 10 rad/s, b) 20 rad/s, c) 70 rad/s, d) 150 rad/s

5. Conclusions

In this work, the nonlinear dynamics of reciprocating compressor of single cylinder with subsidence of the crosshead and clearance between crankshaft and connecting rod are investigated. Dynamics differential equations are established based on the Lagrangian approach. Runge-Kutta method is used to solve the dynamics differential equations by MATLAB software.

Under the condition of the varying cylinder pressure in a cycle, the dynamics responses of reciprocating compressor cylinder are analyzed in the horizontal direction with the changes of clearance sizes, subsidence sizes and crankshaft angular velocities. The numerical simulation results show that the displacement, velocity and acceleration of the crosshead are slightly effected with the increase of the subsidence sizes, but the displacement, velocity and acceleration of the crosshead are significantly affected as the increase of the clearance sizes and crankshaft angular velocities. In addition, the response spectrums of the crosshead acceleration are drawn by using the fast Fourier transform. The results display that besides the rotation frequency of crankshaft, some other frequency components are more and more obvious and even submerge the rotation frequency components in the spectrum with the increase of the clearance sizes. The change in crankshaft angular velocities is just the opposite of the change in the clearance. That is to say, as the crankshaft angular velocities increase, some other frequency components are becoming weaker than the rotation frequency components.

Using Lyapunov exponents and Poincaré section, the stability of the reciprocating compressor system with clearance and subsidence is investigated. The signs of the largest Lyapunov exponents calculated by Wolf method are positive, and the Poincare section is a piece of dense points with a fractal structure for this nonlinear system with clearance and subsidence, indicating the existence of strange attractors and chaos phenomena. In addition, the mechanism exhibits different chaotic motion trajectories with the changes of clearance, subsidence and crankshaft angular velocity, in which the shapes of the phase trajectories significantly change with the variation of clearance and the crankshaft angular velocity, and inconspicuously vary as the change of subsidence.

References

Elhaj M., Gub F., Ballb A. D. Numerical simulation and experimental study of a two-stage reciprocating compressor for condition monitoring. Mechanical Systems and Signal Processing, Vol. 22, 2008, p. 374-389.

Publisher
Almasi A. A new study and model for the mechanism of process reciprocating compressors and pumps. Proceedings of the Institution of Mechanical Engineers, Part E: Journal of Process Mechanical Engineering, Vol. 224, 2010, p. 143-148.

Publisher
Dupac M., Beale D. G. Dynamic analysis of a flexible linkage mechanism with cracks and clearance. Mechanism and Machine Theory, Vol. 45, 2010, p. 1909-1923.

Search CrossRef
Chen G. J., Zou L. Q., Zhao H. Y. An improved local mean decomposition method and its application for fault diagnosis of reciprocating compressor. Journal of Vibroengineering, Vol. 18, Issue 3, 2016, p. 1474-1485.

Publisher
Zhao H. Y., Xu M. Q., Wang J. D. Local mean decomposition based on rational hermite interpolation and its application for fault diagnosis of reciprocating compressor. Journal of Mechanical Engineering, Vol. 51, Issue 1, 2015, p. 83-9.

Publisher
Zhao H. Y., Wang J. D., Hui H. A feature extraction method based on HLMD and MFE for bearing clearance fault of reciprocating compressor. Measurement, Vol. 89, 2016, p. 34-43.

Publisher
Farzaneh-Gord M., Khoshnazar H. Valve fault detection for single-stage reciprocating compressors. Journal of Natural Gas Science and Engineering, Vol. 35, 2016, p. 1239-1248.

Publisher
Pichler K., Lughofer E., Pichler M. Fault detection in reciprocating compressor valves under varying load conditions. Mechanical Systems and Signal Processing, Vol. 70, Issue 71, 2016, p. 104-119.

Publisher
Tran V. T., AlThobiani F., Ball A. An approach to fault diagnosis of reciprocating compressor valves using Teager–Kaiser energy operator and deep belief networks. Expert Systems with Applications, Vol. 41, 2014, p. 4113-4122.

Publisher
Qin Q. Q., Jiang Z. N., Feng K. A novel scheme for fault detection of reciprocating compressor valves based on basis pursuit, wave matching and support vector machine. Measurement, Vol. 45, Issue 5, 2012, p. 897-908.

Publisher
Zhao H. Y., Ji Y. D., Wang J. D. Dynamic analysis of reciprocating compressor transmission mechanism with joint clearance. Fluid Machinery, Vol. 41, Issue 3, 2013, p. 15-33.

Search CrossRef
Zhao H. Y., Xu M. Q., Wang J. D. A parameters optimization method for planar joint clearance model and its application for dynamic s simulation of reciprocating compressor. Journal of Sound and Vibration, Vol. 344, 2015, p. 416-433.

Publisher
Earles S. W. E., Wu C. L. S. Motion analysis of a rigid link mechanism with clearance at a bearing using Lagrangian mechanics and digital computation. Mechanisms, 1973, p. 83-89.

Search CrossRef
Zhang X. C., Zhang X. M. A comparative study of planar 3-RRR and 4-RRR mechanisms with joint clearances. Robotics and Computer-Integrated Manufacturing, Vol. 40, 2016, p. 24-33.

Publisher
Selçuk Erkaya, İbrahim Uzmay Modeling and simulation of joint clearance effects on mechanisms having rigid and flexible links. Journal of Mechanical Science and Technology, Vol. 28, Issue 8, 2014, p. 2979-2986.

Publisher
Feng B., Morita N., Torii T. A new optimization method for dynamic design of planar mechanism with clearances at joints. ASME, Vol. 124, Issue 1, 2002, p. 68-73.

Publisher
Dubowsky S., Freudenstein F. Dynamic analysis of mechanical systems with clearances. Part 1: Formulation of dynamic model. Journal of Engineering for Industry, Vol. 93, Issue 1, 1971, p. 305-309.

Publisher
Dubowsky S., Freudenstein F. Dynamic analysis of mechanical systems with clearances. Part 2: Dynamic response. Journal of Engineering for Industry, Vol. 93, Issue 1, 1971, p. 310-316.

Publisher
Flores P., Ambrosio J., Claro J.C.P., Lankarani H.M. Dynamic behavior of planar rigid multi-body systems including revolute joints with clearance. Proceedings of the Institution of Mechanical Engineers, Part K: Journal of Multi-body Dynamics, Vol. 221, Issue 2, 2007, p. 161-174.

Publisher
Flores P., Lankarani H. M. Dynamic response of multibody systems with multiple clearance joints. Journal Compute Nonlinear Dynamics, Vol. 7, Issue 3, 2011, p. 636-647.

Publisher
Machado M., Costa J., Seabra E., Flores P. The effect of the lubricated revolute joint parameters and hydrodynamic force models on the dynamic response of planar multibody systems. Nonlinear Dynamics, Vol. 69, Issues 1-2, 2012, p. 635-654.

Publisher
Tian Q., Zhang Y. Q., Chen L. P., Yang J. Z. Simulation of planar flexible multibody systems with clearance and lubricated revolute joints. Nonlinear Dynamics, Vol. 60, 2010, p. 489-511.

Publisher
Flores P. A parametric study on the dynamic response of planar multibody systems with multiple clearance joints. Nonlinear Dynamics, Vol. 61, Issue 61, 2010, p. 633-653.

Publisher
Flores P., Ambrósio J., Claro J. C. P., Lankarani H. M., Koshy C. S. Lubricated revolute joints in rigid multibody systems. Nonlinear Dynamics, Vol. 56, Issue 3, 2009, p. 277-295.

Publisher
Flores P., Lankarani H. M. Spatial rigid-multibody systems with lubricated spherical clearance joints: modeling and simulation. Nonlinear Dynamics, Vol. 60, Issue 1, 2010, p. 99-114.

Publisher
Xu L. X., Han Y. C. A method for contact analysis of revolute joints with noncircular clearance in a planar multibody system. Proceedings of the Institution of Mechanical Engineers Part K: Journal Multi-body Dynamics, Vol. 230, Issue 4, 2016, p. 589-605.

Publisher
Farahan S. B., Ghazavi M. R., Rahmanian S. Bifurcation in a planar four-bar mechanism with revolute clearance joint. Nonlinear Dynamics, Vol. 87, 2017, p. 955-973.

Publisher
Wang Z., Tian Q., Hu H. Nonlinear dynamics and chaotic control of a flexible multibody system w ith uncertain joint clearance. Nonlinear Dynamics, Vol. 86, Issue 3, 2016, p. 1571-1597.

Publisher
Nayfeh A. H., Balachandran B. Applied Nonlinear Dynamics. John Wiley and Sons, Inc., New York, 1995.

Publisher
Dupac M., Beale D. G. Dynamic analysis of a flexible linkage mechanism with cracks and clearance. Mechanism and Machine Theory, Vol. 45, Issue 12, 2010, p. 1909-1923.

Publisher
Dupac M., Marghitu D. B. Nonlinear dynamics of a flexible mechanism with impact. Journal of Sound and Vibration, Vol. 289, Issues 4-5, 2006, p. 952-966.

Publisher
Wolf A., Swift J. B., Swinney H. L., Vastano J. A. Determining Lyapunov exponents from a time series Physica D, Vol. 16, 1985, p. 285-317.

Publisher

Cited by

Perspectives in Dynamical Systems I — Applications

Tomé S. N. Guenka | Marcela R. Machado

(2024)

Nonlinear analysis of complex mechanisms with multi-clearances considering dry friction and lubricated joints

(2023)

Coupling rub-impact dynamics of double translational joints with subsidence for time-varying load in a planar mechanical system

Shungen Xiao | Shulin Liu | Mengmeng Song | Nie Ang | Hongli Zhang

(2020)

Nonlinear dynamics of coupling rub-impact of double translational joints with subsidence considering the flexibility of piston rod

(2020)

2020 4th Annual International Conference on Data Science and Business Analytics (ICDSBA)

Shouguo Cheng

(2020)

2019 3rd International Conference on Electronic Information Technology and Computer Engineering (EITCE)

Shouguo Cheng

(2019)

Positive Displacement Machines

Ibrahim A. Sultan | Truong H. Phung

(2019)

Mechanism Design of Equivalent Simulation of Cylinder Pressure Load in Reciprocating Compressor Fault System

(2019)

Dynamic analysis of reciprocating compressor with two revolute joint clearances

Shouguo Cheng | Huwei Chen

(2019)

Analysis of Vertical Vibration Mechanism of Reciprocating Compressors considering Flexibility of Piston Rod and Crosshead Subsidence

(2019)

Nonlinear dynamic response of reciprocating compressor system with rub-impact fault caused by subsidence

Shungen Xiao | Shulin Liu | Feng Jiang | Mengmeng Song | Shouguo Cheng

(2019)

Dynamic analysis of the moving mechanism of the reciprocating compressor with clearance joints

Qingfeng Xiao | Shulin Liu | Ang Nie | Shungen Xiao | Shouguo Cheng

(2018)

About this article

Received

16 June 2017

Accepted

20 August 2017

Published

15 November 2017

SUBJECTS

Fault diagnosis based on vibration signal analysis

DOI

https://doi.org/10.21595/jve.2017.18771

Keywords

reciprocating compressor

dynamics

clearance

subsidence

chaos

Acknowledgements

This work is supported by the Natural Science Foundation of China (Grant No. 51575331 and Grant No. 51175316), Fujian Natural Science Foundation (Grant No. 2015J01643), and Talents Cultivation Program for Outstanding Young Scientists in Fujian Universities (Grant No. MIN Education (2015) 54). These supports are gratefully acknowledged.

Author Contributions

In this paper, Shungen Xiao is responsible for the writing of the entire paper, the realization of the core ideas and so on. Shulin Liu is the advocate of the core idea. Shouguo Cheng helps the first author to debug the programs of the dynamics equation. Xiaogan Xue assists the first author to establish a mathematical model of cylinder pressure. Mengmeng Song helps the first author to analyze the influence of the clearance size. Xin Sun helps the first author to debug the programs of the Lyapunov exponents.

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.

Previous article in issue Previous Next article in issue Next

Research article

2019 11 28

Dynamic analysis of slider-crank mechanism with clearance fault

Shungen Xiao, Mengmeng Song, Zexiong Zhang

Research article

2018 09 24

Dynamic analysis of the moving mechanism of the reciprocating compressor with clearance joints

Qingfeng Xiao, Shulin Liu, Ang Nie, Shungen Xiao, Shouguo Cheng

Research article

2018 05 22

Dynamic analysis of reciprocating compressor with a translational joint clearance

Shouguo Cheng

Research article

2018 02 15

Study on kinetic characteristics of a reciprocating mechanism with clearances

Yan Zou, Cheng Xu, Shao Min Luo

S. Xiao, S. Liu, S. Cheng, X. Xue, M. Song, and X. Sun, “Dynamic analysis of reciprocating compressor with clearance and subsidence,” Journal of Vibroengineering, Vol. 19, No. 7, pp. 5061–5085, Nov. 2017, https://doi.org/10.21595/jve.2017.18771

Copy Extrica

Copied to clipboard!

TY  - JOUR
DO  - 10.21595/jve.2017.18771
UR  - https://doi.org/10.21595/jve.2017.18771
TI  - Dynamic analysis of reciprocating compressor with clearance and subsidence
T2  - Journal of Vibroengineering
AU  - Liu, Shulin
AU  - Xiao, Shungen
AU  - Cheng, Shouguo
AU  - Xue, Xiaogang
AU  - Song, Mengmeng
AU  - Sun, Xin
PY  - 2017
DA  - 2017/11/15
PB  - JVE International Ltd.
SP  - 5061-5085
IS  - 7
VL  - 19
SN  - 1392-8716
ER  - 

Copy Ris

Copied to clipboard!

@article{Liu_2017,
	doi = {10.21595/jve.2017.18771},
	url = {https://doi.org/10.21595/jve.2017.18771},
	year = 2017,
	month = {nov},
	publisher = {{JVE} International Ltd.},
	volume = {19},
	number = {7},
	pages = {5061--5085},
	author = {Shulin Liu and Shungen Xiao and Shouguo Cheng and Xiaogang Xue and Mengmeng Song and Xin Sun},
	title = {Dynamic analysis of reciprocating compressor with clearance and subsidence},
	journal = {Journal of Vibroengineering}
}

Copy Bibtex

Copied to clipboard!

[1]S. Liu, S. Xiao, S. Cheng, X. Xue, M. Song, and X. Sun, “Dynamic analysis of reciprocating compressor with clearance and subsidence,” Journal of Vibroengineering, vol. 19, no. 7, pp. 5061–5085, Nov. 2017, doi: 10.21595/jve.2017.18771.

Copy IEEE

Copied to clipboard!

Liu, Shulin, Shungen Xiao, Shouguo Cheng, Xiaogang Xue, Mengmeng Song, and Xin Sun. “Dynamic Analysis of Reciprocating Compressor with Clearance and Subsidence.” Journal of Vibroengineering 19, no. 7 (November 15, 2017): 5061–85. https://doi.org/10.21595/jve.2017.18771.

Copy Chicago

Copied to clipboard!

Dynamic analysis of reciprocating compressor with clearance and subsidence

Abstract

1. Introduction

2. System model of reciprocating compressor with clearance and subsidence

2.1. Model of cylinder pressure

2.2. Equations of motion

2.3. Equations of dynamics

3. Numerical simulation and dynamic responses analysis

3.1. Dynamic response of reciprocating compressor system with different clearance sizes

3.2. Influence of the crosshead subsidence

3.3. Influence of the input crankshaft angular velocity

4. Chaos analysis

5. Conclusions

References

Cited by

About this article

Related Articles