# Dynamic Simulation Analysis of Carbon-Steel Hybrid Sucker Rod String in Vertical and Directional Wells

Authors: Xiurong Sun; Xianbing Ji; Weicheng Li; Lijuan Zhang; Yang Song
Journal: Mathematical Problems in Engineering
 (2022)

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## Abstract

Carbon fiber composite continuous sucker rod string is more and more widely used in deep and ultradeep wells because of its light weight, high strength, and corrosion resistance. In order to analyze the dynamic problems of carbon fiber sucker rod string in actual oil wells, a transverse vibration simulation model of carbon fiber and steel (carbon-steel) hybrid rod string excited by buckling deformation in vertical wells is established with the compression buckling deformation of weighting rod. Considering the influence of wellbore trajectory and the constraint of tubing, the transverse vibration simulation model of carbon-steel hybrid rod string in directional wells under borehole trajectory excitation is also established in this paper. The finite difference method is used to discretize the well depth node, the numerical integration method (Newmark-β) is used to discretize the reciprocating periodic time node, and simulation methods for the contact and collision dynamics of rod-tubing in vertical wells and directional wells are formed. Through programming calculation, the distribution laws of transverse displacement, contact force, collision force, and bending stress of carbon-steel hybrid sucker rod string in vertical wells and directional wells along well depth are obtained. The simulation results in vertical wells show that the strong collision between the rod and tubing occurs near the bottom steel rod, while the upper load is small and the rod-tubing collision load of the upper rod of the carbon-steel hybrid rod string is much lower than that of the traditional steel rod string at the same position. Furthermore, the bending stress of the upper carbon fiber is also much less than that of the bottom steel rod. The simulation results in directional wells show that the collision phenomenon of the deflecting section and the bottom weighting rod compression section are the strongest and the rod-tubing contact pressure is also the largest. Second, the impact force of the upper carbon fiber rod is also much lower than that of the steel rod. Again, the maximum bending stress of the whole well occurs near the deviation section where the deviation angle changes suddenly. The transverse vibration mechanical model in directional wells in this paper lays a theoretical foundation and provides theoretical support for the optimal design of fracture and splitting prevention measures of carbon fiber sucker rod.


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## Body

## 1. Introduction

Compared with the traditional steel sucker rod, carbon fiber sucker rods have obvious advantages such as light weight, high strength, corrosion resistance, reducing suspension point load, and increasing pump depth [1] and are more and more widely used in oil fields [2, 3]. Carbon fiber sucker rod string is not used alone, but mixed with steel rod. The mixing system consists of the upper carbon fiber rod and the bottom steel rod or weighting rod [4].At present, the research on the mechanical properties of carbon-steel hybrid rod string system is still based on the theory of traditional steel rod string: that is, the buckling analysis of sucker rod in quasistatic state and the mechanical analysis of longitudinal and transverse vibration in dynamic state.The static buckling deformation of traditional steel sucker rod string has laid a good research foundation for the study of carbon fiber rod string mechanics [5, 6]. Sun et al. have established the simulation model of the buckling configuration of the traditional steel sucker rod string in the tubing and concluded that the buckling configuration below the neutral point has an important impact on the entire rod string deformation and rod-tubing collision [7, 8].Wu et al. and Xing et al. have systematically studied the longitudinal vibration and rod-tubing-liquid coupling vibration of sucker rod string in vertical wells and got the numerical simulation result of top suspension point load, bottom pump axial load, natural frequency of rod string, and so on [9, 10]. Sun et al. established the simulation model of the axial distributed load of the sucker rod string based on the wave equation and further pointed out that the axial distributed load changes along the axial position of the sucker rod string, which has significant nonuniform distribution characteristics [7].Based on the understanding of the alternating shape of sucker rod string in vertical wells in tubing, Sun proposed the rod-tubing lateral collision theory of the traditional sucker rod string under the excitation of buckling deformation in vertical wells [11], but it cannot be applied to the carbon fiber rod string system.The mechanical research of directional well is also based on the traditional steel rod string. Dong and Di established the static finite element model of the traditional steel rod string in the tubing in the directional well: the bending deformation, the eccentric wear position, and the contact pressure between the rod and tubing [12, 13]. Wang et al. and Yang et al. studied the longitudinal vibration of sucker rod string, realizes the simulation of axial distributed load and bottom axial load of sucker rod string [14, 15]. Through the quasistatic method, the bending deformation of sucker rod string in tubing, the eccentric wear position, and the contact pressure of rod-tubing in any instantaneous directional well are also simulated by the finite element method. Yang et al. and Zhu et al. established the simulation model of vertical-horizontal-torsional coupling vibration of sucker rod string in directional wells, which is mainly used to analyze the motion law and force of sucker rod string [16, 17]. The above mechanical model is not based on carbon-steel hybrid rod string.With the strengthening of the application of carbon fiber sucker rod in oil wells, the research on its mechanical properties has gradually attracted much attention. Wang et al. and Zhang et al. theoretically analyzed the over stroke behavior of carbon fiber sucker rod string [18, 19]. Lv et al. obtained the variation laws of longitudinal vibration and natural frequency of carbon fiber sucker rod string [20–22]. The above studies are carried out for the axial movement of carbon fiber sucker rod, which lays a good foundation for the study of the mechanical properties of carbon fiber sucker rod string. The transverse bending deformation of carbon fiber sucker rod is not only constrained by the well wall, but also affected by the wellbore trajectory, which is reflected in the influence of the compression buckling deformation of the bottom steel rod string on the transverse vibration of the integral hybrid rod string in vertical wells and the influence of the wellbore trajectory in the directional well on the transverse vibration of the integral hybrid rod string.At present, the mechanical analysis of carbon fiber rod string does not consider the above effects. Although carbon fiber sucker rods have been applied in actual oil wells in batches, the mechanical mechanism of fracture and splitting of sucker rod body is not well understood, and the mechanical model needs to be further improved. It is urgent to carry out the theoretical research of transverse vibration mechanics based on carbon-steel hybrid rod string.In this paper, the transverse vibration simulation models of carbon-steel hybrid rod string in vertical wells and directional wells are established, respectively. In the vertical well, the excitation of the transverse vibration caused by the buckling deformation of the bottom steel rod is considered. In the directional well, the excitation of the transverse vibration of the integral rod string caused by the wellbore trajectory is considered. The rod string length is discretized into spatial nodesJ along the well depth, and the time of periodic change is discretized into time nodes I. Through simulation analysis, the variation laws of transverse vibration, rod-tubing collision, and bending of hybrid rod string in vertical and directional wells are obtained with well depth and period time, which lays a theoretical foundation for the phenomenon of rod string breaking and splitting failure of carbon fiber sucker rod in oil well.


## 2. Simulation Analysis in Vertical Wells

### 2.1. Mechanical Model

Regardless of the torsional deformation of rod string, assuming that the oil tubing is completely vertical, and the axis of rod string coincides with the center of oil tubing.The coordinate system origin is established at the top of the carbon fiber rod string. The rod string in the oil liquid is not only subjected to the reciprocating end loadP(t) at the bottom end, but also subjected to the node load q(x) distributed at different depths of the oil tubing.Based on the above assumptions, the mechanical model of transverse bending deformation of hybrid rod string in vertical wells is established as shown in Figure1.Figure 1
Load model and transverse bending deformation of hybrid rod string. (a) Load model. (b) Transverse bending.
(a)(b)


### 2.2. Mathematical Model

Based on the theory of elastic body dynamics, the differential equation of transverse vibration of sucker rod string in vertical wells is established as follows:(1)ρiAid2udt2=∂Q∂s−εdudt,Q=N∂u∂s−∂M∂s,M=EiIi∂2u∂s2+∂u∂s,N=Pt+∫slqs,tds.(2)x=s−S−uAt,∫slqs,tds=∫sL1q1s,tds+∫L1Lq2s,tds0<x<L1,∫slqs,tds=∫sLq2s,tdsL1<x<L,d2udt2=a∂u∂s+v2∂2u∂s2+2v∂2u∂s∂t+∂2u∂t2.In which,i is the number of rod (i = 1, 2). When i = 1, it represents the carbon fiber material (rod length L1/m)). When i = 2, it represents the steel material (rod length L2/m)). Total length of sucker rod string is L = L1 + L2. N(s, t) is the axial load at instantaneous t at any section s of the rod string, N.u(s,t) is the transverse displacement; Q(s, t) is the shear force at any moving coordinate position point s; M(s, t) is the bending moment at any moving coordinate position point s; P(t) is the axial load at the bottom of the sucker rod string at any instantaneous t, N; S is stroke, m; uA(t) is the suspension point displacement with time; ε is the lateral damping coefficient.The junction of carbon-steel material rod string meets the continuity of displacement, rotation angle, and bending moment, namely, the continuity condition is(3)us=L1−=us=L1+,=duds|s=L1+E1I1d2uds2|s=L1−,=E2I2d2uds2|s=L1+E1I1d3uds3|s=L1−,=E2I2d3uds3|s=L1+.Initial conditions: the rod string is initially in a static state; that is, the rod string lies in the wellbore, the initial state of the rod string central axis coincides with the trajectory line of the wellbore, and the suspension point is at the top dead center at this time. The initial condition can be further expressed as(4)us,0=φs=0,uA0=0,∂u∂ts,0=gs=0.Boundary conditions: the boundary position both top and bottom end of rod string are constrained by transverse displacement and angular displacement. The boundary condition at the top of the carbon fiber rod string can be simplified as a sliding fixed end. The bottom of the steel rod string is also constrained by transverse displacement and angular displacement, whose boundary condition can be simplified as a sliding fixed end. Therefore, the boundary condition of the rod string can be expressed as(5)us,t=0∂u∂ss,t=0,uL,t=0∂u∂sL,t=0.The reason of hybrid rod string producing bending deformation and contacting with the inner wall of the tubing, on the one hand, is the transverse load generated by the viscous resistance of the oil fluid. On the other hand, it is the collision between the bent rod string and the inner wall of the oil tubing, and the motion of nodes rebound after the collision. This process is equivalent to the collision of the impulse theorem, and the contact force is the resultant force of collision force and lateral force generated in the collision process.


### 2.3. Numerical Simulation Method

This (1) is a high-order linear differential equation with variable coefficients, including time variable t and space variable x. When the bending deformation of the rod string contacts with the inner wall of the tubing, it will rebound after collision. The collision process is a nonlinear contact problem. Therefore, the whole analysis process needs to be divided into two parts: solving high-order linear coupled differential equations with variable coefficients and simplifying the collision problem.For the problem of collision here, the commonly used recovery coefficient method is introduced here, that is, when the rod string node collides with the oil tubing wall, the speed along the circumferential radial direction is reversed, while the speed direction and size of the tangential direction remain unchanged, and the motion node falls on the inner wall of the oil pipe after the collision; see the literature [23, 24].It is difficult to solve the higher-order linear coupled differential equations with variable coefficients by the analytical method, and the better way is to use numerical integration. So, this paper adopts the method of combining finite difference and Newmark-β. The finite difference method is used to discrete space variables quantity x, and the Newmark-β method is used for discrete time variable quantity t. The space discrete model is shown in Figure 2. The whole slender rod string is discretized into n elements and N + 1 nodes. Taking the joint position between carbon fiber rod string and steel rod string as the dividing point, steps lengths are ∆x1 and ∆x2, respectively, and the time steps are ∆t:(6)u14=7u1−4u2+u3Δs4,u24=6u2−4u1+u3+u4Δs4,uj4=6uj−4uj−1+uj+1+uj−2+uj+2Δs43≤j≤J−3,uJ−24=6uJ−2−4uJ−1+uJ−3+uJ−4Δs4,uJ−14=7uJ−1−4uJ−2+uJ−3Δs4,u1″=u2−2u1Δs2,uj″=uj+1−2uj+uj−1Δs22≤j≤J−2,uJ−1″=uJ−2−2uJ−1Δs2,u1′=u22Δsuj′=ui+1−ui−12Δs2≤j≤J−2,uJ−1′=−uJ−22Δs.Figure 2
Discrete nodes of carbon-steel hybrid rod string length in vertical wells.Next, the Newmark-β method is used to discretize the time variable t, i.e.,(7)u˙t+Δt=u˙t+1−γu¨t+γu¨t+ΔtΔt,ut+Δt=ut+u˙tΔt+12−βu¨t+βu¨t+ΔtΔt2.In which,β and γ are the integration accuracy parameters. When β ≥ 0.5, γ ≥ 0.25(0.5 + β)2, the numerical method is unconditionally convergent. This paper takes β = 0.5, γ = 0.25, and at this time, the stability and accuracy are both high. The recursive expression is further obtained from (7), i.e.,(8)u¨t+Δt=α0ut+Δt−ut−α2u˙t−α3u¨t,u˙t+Δt=α1ut+Δt−ut−α4u˙t−α5u¨t,α0=1βΔt2α1=γβΔtα2=1βΔt,α3=12β−1α4=γβ−1α5=Δt2γβ−2.The equilibrium differential equation at timet+∆t satisfies as follows:(9)Mu¨t+Δt+Cu˙t+Δt+Kut+Δt=Rt+Δt.Substituting (7) and (8) into (9), the equation about {u}t+∆t is obtained:(10)K¯yt+Δt=R¯t+Δt,in which(11)K¯=K+α0M+α1C,R¯t+Δt=Rt+Δt+Mα0yt+α2y˙t+α3y¨t+Cα1yt+α4y˙t+α5+Δty¨t,in which [K], [M], and [C] represent stiffness matrix, mass matrix, and damping matrix, respectively.After sorting, the discrete form of (10) is expressed by(12)Gi,jk=Aiyj−2k+Bi,j−1kyj−1k+Ci,jkyjk+Di,j+1kyj+1k+Fiyj+2k3≤i≤N−3,Ai=Fi=EiIiΔs4,Bi,j−1k=ρiAi−a2Δs+v2Δs2−vα1Δs−4EiIiΔs4−NΔs2+∂N∂s12Δs−εv2Δs,Cik=6EiIih4+ρiAiα0−2v2Δs2+2N1Δs2+εα1,Di,j+1k=ρiAia2Δs+v2Δs2+vα1Δs−4EiIiΔs4−NΔs2−∂N∂s12Δs+εv2Δs,Gi,jk=ρiAiα0ujk−1+α2u˙jk−1+α3u¨jk−1+ρiAivα1uj+1k−1+α4u˙j+1k−1+α5u¨j+1k−1Δs+ρiAivα1uj−1k−1+α4u˙j−1k−1+α5u¨j−1k−1Δs+εα1ujk−1+α4u˙jk−1+α5u¨jk−1,in which i is the same as the meaning of (1), j is the rod string length node, and k is the time node.When the rod string length node collides with the tubing wall, it is considered that the transverse displacement of rod string exceeds the boundary of the tubing wall. After the collision, the displacement and velocity of the node meet the following relationship:(13)us,t|t+=sgnus,t|t−R−r,dus,tdt|t+=−γedus,tdt|t−.γe is the collision recovery coefficient, and its value is determined by the collision material. For further analysis, see reference [23].Furthermore, the calculation formulas of collision force and transverse pressure are(14)Fi,n=−ρiAi1+γΔτdus,tdt|t−,Fi,s=EiIi∂2u∂s2−∂∂sT∂u∂s.The total contact force of rod-tubing is composed of the resultant force of collision force and transverse pressure.Δτ is the time step of collision, and its value can be found in reference [24].


## 2.1. Mechanical Model

Regardless of the torsional deformation of rod string, assuming that the oil tubing is completely vertical, and the axis of rod string coincides with the center of oil tubing.The coordinate system origin is established at the top of the carbon fiber rod string. The rod string in the oil liquid is not only subjected to the reciprocating end loadP(t) at the bottom end, but also subjected to the node load q(x) distributed at different depths of the oil tubing.Based on the above assumptions, the mechanical model of transverse bending deformation of hybrid rod string in vertical wells is established as shown in Figure1.Figure 1
Load model and transverse bending deformation of hybrid rod string. (a) Load model. (b) Transverse bending.
(a)(b)


## 2.2. Mathematical Model

Based on the theory of elastic body dynamics, the differential equation of transverse vibration of sucker rod string in vertical wells is established as follows:(1)ρiAid2udt2=∂Q∂s−εdudt,Q=N∂u∂s−∂M∂s,M=EiIi∂2u∂s2+∂u∂s,N=Pt+∫slqs,tds.(2)x=s−S−uAt,∫slqs,tds=∫sL1q1s,tds+∫L1Lq2s,tds0<x<L1,∫slqs,tds=∫sLq2s,tdsL1<x<L,d2udt2=a∂u∂s+v2∂2u∂s2+2v∂2u∂s∂t+∂2u∂t2.In which,i is the number of rod (i = 1, 2). When i = 1, it represents the carbon fiber material (rod length L1/m)). When i = 2, it represents the steel material (rod length L2/m)). Total length of sucker rod string is L = L1 + L2. N(s, t) is the axial load at instantaneous t at any section s of the rod string, N.u(s,t) is the transverse displacement; Q(s, t) is the shear force at any moving coordinate position point s; M(s, t) is the bending moment at any moving coordinate position point s; P(t) is the axial load at the bottom of the sucker rod string at any instantaneous t, N; S is stroke, m; uA(t) is the suspension point displacement with time; ε is the lateral damping coefficient.The junction of carbon-steel material rod string meets the continuity of displacement, rotation angle, and bending moment, namely, the continuity condition is(3)us=L1−=us=L1+,=duds|s=L1+E1I1d2uds2|s=L1−,=E2I2d2uds2|s=L1+E1I1d3uds3|s=L1−,=E2I2d3uds3|s=L1+.Initial conditions: the rod string is initially in a static state; that is, the rod string lies in the wellbore, the initial state of the rod string central axis coincides with the trajectory line of the wellbore, and the suspension point is at the top dead center at this time. The initial condition can be further expressed as(4)us,0=φs=0,uA0=0,∂u∂ts,0=gs=0.Boundary conditions: the boundary position both top and bottom end of rod string are constrained by transverse displacement and angular displacement. The boundary condition at the top of the carbon fiber rod string can be simplified as a sliding fixed end. The bottom of the steel rod string is also constrained by transverse displacement and angular displacement, whose boundary condition can be simplified as a sliding fixed end. Therefore, the boundary condition of the rod string can be expressed as(5)us,t=0∂u∂ss,t=0,uL,t=0∂u∂sL,t=0.The reason of hybrid rod string producing bending deformation and contacting with the inner wall of the tubing, on the one hand, is the transverse load generated by the viscous resistance of the oil fluid. On the other hand, it is the collision between the bent rod string and the inner wall of the oil tubing, and the motion of nodes rebound after the collision. This process is equivalent to the collision of the impulse theorem, and the contact force is the resultant force of collision force and lateral force generated in the collision process.


## 2.3. Numerical Simulation Method

This (1) is a high-order linear differential equation with variable coefficients, including time variable t and space variable x. When the bending deformation of the rod string contacts with the inner wall of the tubing, it will rebound after collision. The collision process is a nonlinear contact problem. Therefore, the whole analysis process needs to be divided into two parts: solving high-order linear coupled differential equations with variable coefficients and simplifying the collision problem.For the problem of collision here, the commonly used recovery coefficient method is introduced here, that is, when the rod string node collides with the oil tubing wall, the speed along the circumferential radial direction is reversed, while the speed direction and size of the tangential direction remain unchanged, and the motion node falls on the inner wall of the oil pipe after the collision; see the literature [23, 24].It is difficult to solve the higher-order linear coupled differential equations with variable coefficients by the analytical method, and the better way is to use numerical integration. So, this paper adopts the method of combining finite difference and Newmark-β. The finite difference method is used to discrete space variables quantity x, and the Newmark-β method is used for discrete time variable quantity t. The space discrete model is shown in Figure 2. The whole slender rod string is discretized into n elements and N + 1 nodes. Taking the joint position between carbon fiber rod string and steel rod string as the dividing point, steps lengths are ∆x1 and ∆x2, respectively, and the time steps are ∆t:(6)u14=7u1−4u2+u3Δs4,u24=6u2−4u1+u3+u4Δs4,uj4=6uj−4uj−1+uj+1+uj−2+uj+2Δs43≤j≤J−3,uJ−24=6uJ−2−4uJ−1+uJ−3+uJ−4Δs4,uJ−14=7uJ−1−4uJ−2+uJ−3Δs4,u1″=u2−2u1Δs2,uj″=uj+1−2uj+uj−1Δs22≤j≤J−2,uJ−1″=uJ−2−2uJ−1Δs2,u1′=u22Δsuj′=ui+1−ui−12Δs2≤j≤J−2,uJ−1′=−uJ−22Δs.Figure 2
Discrete nodes of carbon-steel hybrid rod string length in vertical wells.Next, the Newmark-β method is used to discretize the time variable t, i.e.,(7)u˙t+Δt=u˙t+1−γu¨t+γu¨t+ΔtΔt,ut+Δt=ut+u˙tΔt+12−βu¨t+βu¨t+ΔtΔt2.In which,β and γ are the integration accuracy parameters. When β ≥ 0.5, γ ≥ 0.25(0.5 + β)2, the numerical method is unconditionally convergent. This paper takes β = 0.5, γ = 0.25, and at this time, the stability and accuracy are both high. The recursive expression is further obtained from (7), i.e.,(8)u¨t+Δt=α0ut+Δt−ut−α2u˙t−α3u¨t,u˙t+Δt=α1ut+Δt−ut−α4u˙t−α5u¨t,α0=1βΔt2α1=γβΔtα2=1βΔt,α3=12β−1α4=γβ−1α5=Δt2γβ−2.The equilibrium differential equation at timet+∆t satisfies as follows:(9)Mu¨t+Δt+Cu˙t+Δt+Kut+Δt=Rt+Δt.Substituting (7) and (8) into (9), the equation about {u}t+∆t is obtained:(10)K¯yt+Δt=R¯t+Δt,in which(11)K¯=K+α0M+α1C,R¯t+Δt=Rt+Δt+Mα0yt+α2y˙t+α3y¨t+Cα1yt+α4y˙t+α5+Δty¨t,in which [K], [M], and [C] represent stiffness matrix, mass matrix, and damping matrix, respectively.After sorting, the discrete form of (10) is expressed by(12)Gi,jk=Aiyj−2k+Bi,j−1kyj−1k+Ci,jkyjk+Di,j+1kyj+1k+Fiyj+2k3≤i≤N−3,Ai=Fi=EiIiΔs4,Bi,j−1k=ρiAi−a2Δs+v2Δs2−vα1Δs−4EiIiΔs4−NΔs2+∂N∂s12Δs−εv2Δs,Cik=6EiIih4+ρiAiα0−2v2Δs2+2N1Δs2+εα1,Di,j+1k=ρiAia2Δs+v2Δs2+vα1Δs−4EiIiΔs4−NΔs2−∂N∂s12Δs+εv2Δs,Gi,jk=ρiAiα0ujk−1+α2u˙jk−1+α3u¨jk−1+ρiAivα1uj+1k−1+α4u˙j+1k−1+α5u¨j+1k−1Δs+ρiAivα1uj−1k−1+α4u˙j−1k−1+α5u¨j−1k−1Δs+εα1ujk−1+α4u˙jk−1+α5u¨jk−1,in which i is the same as the meaning of (1), j is the rod string length node, and k is the time node.When the rod string length node collides with the tubing wall, it is considered that the transverse displacement of rod string exceeds the boundary of the tubing wall. After the collision, the displacement and velocity of the node meet the following relationship:(13)us,t|t+=sgnus,t|t−R−r,dus,tdt|t+=−γedus,tdt|t−.γe is the collision recovery coefficient, and its value is determined by the collision material. For further analysis, see reference [23].Furthermore, the calculation formulas of collision force and transverse pressure are(14)Fi,n=−ρiAi1+γΔτdus,tdt|t−,Fi,s=EiIi∂2u∂s2−∂∂sT∂u∂s.The total contact force of rod-tubing is composed of the resultant force of collision force and transverse pressure.Δτ is the time step of collision, and its value can be found in reference [24].


## 3. Simulation Analysis in Directional Wells

### 3.1. Mechanical Model

In directional wells, the upper carbon fiber sucker rod is regarded as a continuous rod string without coupling, and the bottom influence of the coupling and centralizer of the weighted steel rod is ignored. The overall rod string structure and load diagram in directional wells are shown in Figures3(a) and 3(b), respectively. In order to facilitate modeling, two coordinate systems are established to express the rod string position in the well depth: the first one is the static coordinate system fixed at the top, with the position of well depth being represented by x. The second one is the dynamic coordinate system, with the position of well depth by s.Figure 3
Rod string structure and load model of carbon-steel hybrid rod string in directional wells. (a) Schematic diagram of hybrid rod string. (b) Load model.
(a)(b)In Figure3, q(s,t) or q(x,t) is the axial distributed force at the axis position s or x. P(t) is the concentrated axial force at the bottom of the sucker rod. qu(s,t) or qu (x,t) is the transverse distributed load. L1 and L2 are the lengths of carbon fiber rod and steel rod, respectively. uA(t) is the suspension point position.According to Figure3, further assumptions are made as follows. First the well trajectory appears only in the 2D plane. Second, ignore the effect of torsional deformation of rod string. Third, the axis line of the overall rod string and the center of the tubing coincides with the well trajectory line. Fourth, in addition to the concentrated axial load P(t), the bottom of the weighting rod is also subjected to the distributed load q(s,t) or q(sj,t) at different well depth positions.


### 3.2. Mathematical Model

Based on the theory of elastomer dynamics, the differential equation of transverse vibration of sucker rod string in directional wells is established as follows:(15)ρiAid2udt2=∂Q∂s+N∂αx∂s+qubx,t,Q=N∂u∂s−∂M∂s,M=EiIi∂2u∂s2+∂u∂s,x=s−S−uAt,N=Pt+∫slqs,tds,qubx,t=−ρi−ρlAigsinαx−εdudt,∫slqs,tds=∫sL1q1s,tds+∫L1Lq2s,tds0<s<L1,∫slqs,tds=∫sLq2s,tdsL1<s<L.d2udt2=a∂u∂s+v2∂2u∂s2+2v∂2u∂s∂t+∂2u∂t2.In which,ρi is the material density of corresponding rod number, kg/m3. Ai is the cross-sectional area of rod string. ρl is the oil liquid density, kg/m3. q(s,t) is the axial distributed load at any section position s, N/m. qub(x,t) is the transverse distributed load at any section position s, and N/m. α(x) is the well deviation angle at any static coordinate position x.The continuity conditions are the same as those in Section2.2, the junction of carbon fiber material rod string and steel material rod string both meet the continuity of displacement, and rotation angle and bending moment, namely, the continuity condition are(16)us=L1−=us=L1+duds|s=L1−=duds|s=L1+E1I1d2uds2|s=L1−=E2I2d2uds2|s=L1+E1I1d3uds3|s=L1−=E2I2d3uds3|s=L1+.Initial conditions: the rod string is initially in a static state, also the same as section2.2. That is, the initial condition can be expressed as(17)us,0=φs=0,uA0=0,∂u∂ts,0=gs=0.Boundary conditions: the boundary position between the top of the carbon fiber rod string and the wellhead is also the same as Section2.2. Therefore, the boundary condition of the rod string can be expressed as(18)us,t=0,∂u∂ss,t=0,uL,t=0,∂u∂sL,t=0.


### 3.3. Numerical Simulation Method

The transverse vibration equation of carbon-steel hybrid rod string is a high-order partial differential equation. The time variablet and the curvilinear coordinate variable s are coupled together, so it is almost impossible to separate the variables to obtain the analytical solution. As Section 2.3, the finite difference method and the Newmark method are combined for numerical analysis to obtain the numerical solution. It should be noted that the finite difference method can solve the linear problem, but this paper presents a special, the curved wellbore of directional well can be regarded as a straight line and then can be simulated according to the finite difference method.The discrete model of carbon-steel hybrid rod string along the coordinate variables is shown in Figure 4 (∆ s is the differential step size). The junction of the two-stage rod meets the continuity condition of (16). The central finite difference method is used to discretize the variables u′, u′′, u′′′, u(4) about s.Figure 4
Discrete nodes of hybrid rod string length of directional well.The simulation method of transverse vibration of hybrid rod string in directional wells is similar to Section2.3. So, the discrete form of equation (11) in directional wells is(19)Gi,jk=Aiyj−2k+Bi,j−1kyj−1k+Ci,jkyjk+Di,j+1kyj+1k+Fiyj+2k3≤i≤N−3,Ai=Fi=EiIiΔs4,Bi,j−1k=ρiAi−a2Δs+v2Δs2−vα1Δs−4EiIiΔs4−NΔs2+∂N∂s12Δs−εv2Δs,Cik=6EiIih4+ρiAiα0−2v2Δs2+2N1Δs2+εα1,Di,j+1k=ρiAia2Δs+v2Δs2+vα1Δs−4EiIiΔs4−NΔs2−∂N∂s12Δs+εv2Δs,Gi,jk=ρiAiα0ujk−1+α2u˙jk−1+α3u¨jk−1+ρiAivα1uj+1k−1+α4u˙j+1k−1+α5u¨j+1k−1Δs+ρiAivα1uj−1k−1+α4u˙j−1k−1+α5u¨j−1k−1Δs−EiIi∂3αx∂s3+N∂αx∂s−ρi−ρlAigsinαx+εα1ujk−1+α4u˙jk−1+α5u¨jk−1.After collision, the node displacement and velocity meet the following relationship:(20)us,t|t+=sgnus,t|t−|R−r,dus,tdt|t+=−γedus,tdt|t−.Accordingly, the calculation formulas of impact force and transverse pressure of directional well rod-tubing are expressed as follows:(21)Fi,n=−ρiAi1+γΔτdus,tdt|t−,Fi,s=EiIi∂2u∂s2+∂3αx∂s3−T∂αx∂s+ρi−ρlAigsinαx−∂∂sT∂u∂s.The total contact force of rod-tubing is composed of the resultant force of collision force and transverse pressure.Δτ is the time step of collision, and its value can be found in reference [24].


## 3.1. Mechanical Model

In directional wells, the upper carbon fiber sucker rod is regarded as a continuous rod string without coupling, and the bottom influence of the coupling and centralizer of the weighted steel rod is ignored. The overall rod string structure and load diagram in directional wells are shown in Figures3(a) and 3(b), respectively. In order to facilitate modeling, two coordinate systems are established to express the rod string position in the well depth: the first one is the static coordinate system fixed at the top, with the position of well depth being represented by x. The second one is the dynamic coordinate system, with the position of well depth by s.Figure 3
Rod string structure and load model of carbon-steel hybrid rod string in directional wells. (a) Schematic diagram of hybrid rod string. (b) Load model.
(a)(b)In Figure3, q(s,t) or q(x,t) is the axial distributed force at the axis position s or x. P(t) is the concentrated axial force at the bottom of the sucker rod. qu(s,t) or qu (x,t) is the transverse distributed load. L1 and L2 are the lengths of carbon fiber rod and steel rod, respectively. uA(t) is the suspension point position.According to Figure3, further assumptions are made as follows. First the well trajectory appears only in the 2D plane. Second, ignore the effect of torsional deformation of rod string. Third, the axis line of the overall rod string and the center of the tubing coincides with the well trajectory line. Fourth, in addition to the concentrated axial load P(t), the bottom of the weighting rod is also subjected to the distributed load q(s,t) or q(sj,t) at different well depth positions.


## 3.2. Mathematical Model

Based on the theory of elastomer dynamics, the differential equation of transverse vibration of sucker rod string in directional wells is established as follows:(15)ρiAid2udt2=∂Q∂s+N∂αx∂s+qubx,t,Q=N∂u∂s−∂M∂s,M=EiIi∂2u∂s2+∂u∂s,x=s−S−uAt,N=Pt+∫slqs,tds,qubx,t=−ρi−ρlAigsinαx−εdudt,∫slqs,tds=∫sL1q1s,tds+∫L1Lq2s,tds0<s<L1,∫slqs,tds=∫sLq2s,tdsL1<s<L.d2udt2=a∂u∂s+v2∂2u∂s2+2v∂2u∂s∂t+∂2u∂t2.In which,ρi is the material density of corresponding rod number, kg/m3. Ai is the cross-sectional area of rod string. ρl is the oil liquid density, kg/m3. q(s,t) is the axial distributed load at any section position s, N/m. qub(x,t) is the transverse distributed load at any section position s, and N/m. α(x) is the well deviation angle at any static coordinate position x.The continuity conditions are the same as those in Section2.2, the junction of carbon fiber material rod string and steel material rod string both meet the continuity of displacement, and rotation angle and bending moment, namely, the continuity condition are(16)us=L1−=us=L1+duds|s=L1−=duds|s=L1+E1I1d2uds2|s=L1−=E2I2d2uds2|s=L1+E1I1d3uds3|s=L1−=E2I2d3uds3|s=L1+.Initial conditions: the rod string is initially in a static state, also the same as section2.2. That is, the initial condition can be expressed as(17)us,0=φs=0,uA0=0,∂u∂ts,0=gs=0.Boundary conditions: the boundary position between the top of the carbon fiber rod string and the wellhead is also the same as Section2.2. Therefore, the boundary condition of the rod string can be expressed as(18)us,t=0,∂u∂ss,t=0,uL,t=0,∂u∂sL,t=0.


## 3.3. Numerical Simulation Method

The transverse vibration equation of carbon-steel hybrid rod string is a high-order partial differential equation. The time variablet and the curvilinear coordinate variable s are coupled together, so it is almost impossible to separate the variables to obtain the analytical solution. As Section 2.3, the finite difference method and the Newmark method are combined for numerical analysis to obtain the numerical solution. It should be noted that the finite difference method can solve the linear problem, but this paper presents a special, the curved wellbore of directional well can be regarded as a straight line and then can be simulated according to the finite difference method.The discrete model of carbon-steel hybrid rod string along the coordinate variables is shown in Figure 4 (∆ s is the differential step size). The junction of the two-stage rod meets the continuity condition of (16). The central finite difference method is used to discretize the variables u′, u′′, u′′′, u(4) about s.Figure 4
Discrete nodes of hybrid rod string length of directional well.The simulation method of transverse vibration of hybrid rod string in directional wells is similar to Section2.3. So, the discrete form of equation (11) in directional wells is(19)Gi,jk=Aiyj−2k+Bi,j−1kyj−1k+Ci,jkyjk+Di,j+1kyj+1k+Fiyj+2k3≤i≤N−3,Ai=Fi=EiIiΔs4,Bi,j−1k=ρiAi−a2Δs+v2Δs2−vα1Δs−4EiIiΔs4−NΔs2+∂N∂s12Δs−εv2Δs,Cik=6EiIih4+ρiAiα0−2v2Δs2+2N1Δs2+εα1,Di,j+1k=ρiAia2Δs+v2Δs2+vα1Δs−4EiIiΔs4−NΔs2−∂N∂s12Δs+εv2Δs,Gi,jk=ρiAiα0ujk−1+α2u˙jk−1+α3u¨jk−1+ρiAivα1uj+1k−1+α4u˙j+1k−1+α5u¨j+1k−1Δs+ρiAivα1uj−1k−1+α4u˙j−1k−1+α5u¨j−1k−1Δs−EiIi∂3αx∂s3+N∂αx∂s−ρi−ρlAigsinαx+εα1ujk−1+α4u˙jk−1+α5u¨jk−1.After collision, the node displacement and velocity meet the following relationship:(20)us,t|t+=sgnus,t|t−|R−r,dus,tdt|t+=−γedus,tdt|t−.Accordingly, the calculation formulas of impact force and transverse pressure of directional well rod-tubing are expressed as follows:(21)Fi,n=−ρiAi1+γΔτdus,tdt|t−,Fi,s=EiIi∂2u∂s2+∂3αx∂s3−T∂αx∂s+ρi−ρlAigsinαx−∂∂sT∂u∂s.The total contact force of rod-tubing is composed of the resultant force of collision force and transverse pressure.Δτ is the time step of collision, and its value can be found in reference [24].


## 4. Simulation Result

### 4.1. Basic Parameters

Both vertical and directional wells are 2200 m deep. The wellbore trajectory of vertical well is an idealized vertical wellbore, and the curved trajectory of directional well is shown in Figure5. Combination form of carbon-steel hybrid rod string is as follows: 19 mm × 1650 m + 25 mm × 550 m. The upper part is continuous carbon fiber sucker rod, and the lower part is steel weighting rod. The respective elastic modulus is E1 = 103 GPa and E2 = 206 GPa, respectively. Other corresponding parameters in both well types are shown in Figure 6.Figure 5
Wellbore trajectory of directional well.Figure 6
Basic parameters of simulation interface.


### 4.2. Simulation Results of Impact Force and Contact Pressure

#### 4.2.1. The Impact Force and Contact Pressure in Vertical Wells

Through numerical simulation of vertical well, the variation laws of rod string with well depth and time are obtained as shown in Figure7, which shows two different results between the traditional steel rod and new carbon-steel hybrid rod string in this paper. It can be seen that the similarities between Figures 7(a) and 7(b) are the largest impact force with the same level value distributed on the steel rod at bottom. However, the impact contact force of the upper part in new carbon-steel hybrid rod string in Figure 7(a) is greatly reduced compared with the traditional steel rod string in the same position in Figure 7(b). This means that the carbon fiber rod string can effectively reduce the contact and collision of rod-tubing, especially in the upper part of the wellbore and prolong the service life of the rod accordingly.Figure 7
Variation of collision contact force with well depth. (a) Carbon-steel hybrid rod string. (b) Traditional steel rod string.
(a)(b)


#### 4.2.2. The Impact Force and Contact Pressure in Directional Wells

Through the simulation analysis of the transverse vibration of carbon-steel hybrid rod string in directional wells, the variation laws of rod string transverse displacement, collision force, and contact force of rod-tubing with well depth and time are obtained, as shown in Figure8.Figure 8
Simulation results of carbon-steel hybrid rod string. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)It can be seen from Figure8 that the largest transverse displacement is at the bottom steel rod with almost all the rod string nodes attached to the oil well wall. Second, except for the deflecting section of wellbore, the collision force of the upper carbon fiber sucker rod is significantly lower than that of the bottom steel rod. At the inclined section and the bottom steel rod part, the collision force increases significantly. Again, the area with the maximum contact force occurs in the deviation section with large deviation angle, which indicates that the eccentric wear of rod-tubing in the deviation section will be the most serious.Figures9(a)–9(c) show the simulation results of traditional steel rod string in directional wells under the same condition as carbon fiber rod string. It can be seen from the comparison between Figures 8 and 9 that the maximum transverse displacement of the new and old rod string system occurs all in the compression section of the bottom rod. Again, the collision force and contact force of the rod-tubing at the inclined section are almost the largest, indicating that the inclined section has a significant impact on the collision and extrusion of rod-tubing.Figure 9
Simulation results of traditional steel rod. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)


### 4.3. Bending Stress Simulation Results

#### 4.3.1. Bending Stress in Vertical Wells

After further processing of the vertical well numerical simulation results, the bending stress distribution of the rod string after dynamic deformation in the tubing is obtained, as shown in Figure10. We can get the bending stress of new carbon-steel hybrid rod string (1650–2200 m) from Figure 10(a) and the bending stress of new carbon-steel hybrid rod string (0–1650 m) from Figure 10(b), and also bending stress of traditional steel rod string (0–2200 m) from Figure 10(c).Figure 10
Variation of bending stress of new and traditional rod string in vertical wells. (a) Bending stress of new carbon-steel hybrid rod string (1650–2200 m). (b) Bending stress of new carbon-steel hybrid rod string (0–1650 m). (c) Bending stress of traditional steel rod string (0–2200 m).
(a)(b)(c)It can be seen from the figure that the maximum bending stress of carbon-steel rod increases with the increase of well depth in a stroke. The maximum bending stress of the upper carbon fiber rod (0–1650 m) can reach 30 MPa compared with the bottom steel rod (1650–2200 m) 150 MPa. The bending stress of the traditional steel rod (0–1650 m) reaches 80Mpa. Although the bending stress does not exceed their yield limit, the stress of the traditional steel rod in the wellbore is mostly reciprocating wear and fatigue failure. On the contrary, the bending stress of carbon fiber rod is greatly reduced, and the service life of carbon fiber rod is greatly prolonged.


#### 4.3.2. Bending Stress in Directional Wells

Based on the above simulation model of carbon-steel hybrid rod string in directional wells, the bending stress of hybrid rod string after transverse vibration deformation in tubing is obtained, as shown in Figure11(a). The second model replaces the upper carbon fiber rod string with steel rod with the same size to obtain the bending stress, as shown in Figure 8(b). It can be seen from Figures 11(a) and 11(b) that, whether it is an integral steel rod or a carbon and steel hybrid rod string, when the sucker rod string reciprocates in the directional well, the bending stress at the inclined section is almost the largest in the whole well.Figure 11
Change of bending stress of carbon fiber hybrid rod string and traditional steel rod string in directional well. (a) Change of bending stress of carbon fiber hybrid rod string. (b) Variation of bending stress of traditional steel rod string.
(a)(b)In the above two comparative models, the maximum bending stress of the above two kinds of rod forms appears near the inclined section. The simulation results are consistent with the fact that the actual rod string is the easiest to be damaged at the inclined section.


## 4.1. Basic Parameters

Both vertical and directional wells are 2200 m deep. The wellbore trajectory of vertical well is an idealized vertical wellbore, and the curved trajectory of directional well is shown in Figure5. Combination form of carbon-steel hybrid rod string is as follows: 19 mm × 1650 m + 25 mm × 550 m. The upper part is continuous carbon fiber sucker rod, and the lower part is steel weighting rod. The respective elastic modulus is E1 = 103 GPa and E2 = 206 GPa, respectively. Other corresponding parameters in both well types are shown in Figure 6.Figure 5
Wellbore trajectory of directional well.Figure 6
Basic parameters of simulation interface.


## 4.2. Simulation Results of Impact Force and Contact Pressure

### 4.2.1. The Impact Force and Contact Pressure in Vertical Wells

Through numerical simulation of vertical well, the variation laws of rod string with well depth and time are obtained as shown in Figure7, which shows two different results between the traditional steel rod and new carbon-steel hybrid rod string in this paper. It can be seen that the similarities between Figures 7(a) and 7(b) are the largest impact force with the same level value distributed on the steel rod at bottom. However, the impact contact force of the upper part in new carbon-steel hybrid rod string in Figure 7(a) is greatly reduced compared with the traditional steel rod string in the same position in Figure 7(b). This means that the carbon fiber rod string can effectively reduce the contact and collision of rod-tubing, especially in the upper part of the wellbore and prolong the service life of the rod accordingly.Figure 7
Variation of collision contact force with well depth. (a) Carbon-steel hybrid rod string. (b) Traditional steel rod string.
(a)(b)


### 4.2.2. The Impact Force and Contact Pressure in Directional Wells

Through the simulation analysis of the transverse vibration of carbon-steel hybrid rod string in directional wells, the variation laws of rod string transverse displacement, collision force, and contact force of rod-tubing with well depth and time are obtained, as shown in Figure8.Figure 8
Simulation results of carbon-steel hybrid rod string. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)It can be seen from Figure8 that the largest transverse displacement is at the bottom steel rod with almost all the rod string nodes attached to the oil well wall. Second, except for the deflecting section of wellbore, the collision force of the upper carbon fiber sucker rod is significantly lower than that of the bottom steel rod. At the inclined section and the bottom steel rod part, the collision force increases significantly. Again, the area with the maximum contact force occurs in the deviation section with large deviation angle, which indicates that the eccentric wear of rod-tubing in the deviation section will be the most serious.Figures9(a)–9(c) show the simulation results of traditional steel rod string in directional wells under the same condition as carbon fiber rod string. It can be seen from the comparison between Figures 8 and 9 that the maximum transverse displacement of the new and old rod string system occurs all in the compression section of the bottom rod. Again, the collision force and contact force of the rod-tubing at the inclined section are almost the largest, indicating that the inclined section has a significant impact on the collision and extrusion of rod-tubing.Figure 9
Simulation results of traditional steel rod. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)


## 4.2.1. The Impact Force and Contact Pressure in Vertical Wells

Through numerical simulation of vertical well, the variation laws of rod string with well depth and time are obtained as shown in Figure7, which shows two different results between the traditional steel rod and new carbon-steel hybrid rod string in this paper. It can be seen that the similarities between Figures 7(a) and 7(b) are the largest impact force with the same level value distributed on the steel rod at bottom. However, the impact contact force of the upper part in new carbon-steel hybrid rod string in Figure 7(a) is greatly reduced compared with the traditional steel rod string in the same position in Figure 7(b). This means that the carbon fiber rod string can effectively reduce the contact and collision of rod-tubing, especially in the upper part of the wellbore and prolong the service life of the rod accordingly.Figure 7
Variation of collision contact force with well depth. (a) Carbon-steel hybrid rod string. (b) Traditional steel rod string.
(a)(b)


## 4.2.2. The Impact Force and Contact Pressure in Directional Wells

Through the simulation analysis of the transverse vibration of carbon-steel hybrid rod string in directional wells, the variation laws of rod string transverse displacement, collision force, and contact force of rod-tubing with well depth and time are obtained, as shown in Figure8.Figure 8
Simulation results of carbon-steel hybrid rod string. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)It can be seen from Figure8 that the largest transverse displacement is at the bottom steel rod with almost all the rod string nodes attached to the oil well wall. Second, except for the deflecting section of wellbore, the collision force of the upper carbon fiber sucker rod is significantly lower than that of the bottom steel rod. At the inclined section and the bottom steel rod part, the collision force increases significantly. Again, the area with the maximum contact force occurs in the deviation section with large deviation angle, which indicates that the eccentric wear of rod-tubing in the deviation section will be the most serious.Figures9(a)–9(c) show the simulation results of traditional steel rod string in directional wells under the same condition as carbon fiber rod string. It can be seen from the comparison between Figures 8 and 9 that the maximum transverse displacement of the new and old rod string system occurs all in the compression section of the bottom rod. Again, the collision force and contact force of the rod-tubing at the inclined section are almost the largest, indicating that the inclined section has a significant impact on the collision and extrusion of rod-tubing.Figure 9
Simulation results of traditional steel rod. (a) Transverse displacement varies with well depth and time. (b) The impact force varies with well depth and time. (c) Rod-tubing contact force varies with well depth and time.
(a)(b)(c)


## 4.3. Bending Stress Simulation Results

### 4.3.1. Bending Stress in Vertical Wells

After further processing of the vertical well numerical simulation results, the bending stress distribution of the rod string after dynamic deformation in the tubing is obtained, as shown in Figure10. We can get the bending stress of new carbon-steel hybrid rod string (1650–2200 m) from Figure 10(a) and the bending stress of new carbon-steel hybrid rod string (0–1650 m) from Figure 10(b), and also bending stress of traditional steel rod string (0–2200 m) from Figure 10(c).Figure 10
Variation of bending stress of new and traditional rod string in vertical wells. (a) Bending stress of new carbon-steel hybrid rod string (1650–2200 m). (b) Bending stress of new carbon-steel hybrid rod string (0–1650 m). (c) Bending stress of traditional steel rod string (0–2200 m).
(a)(b)(c)It can be seen from the figure that the maximum bending stress of carbon-steel rod increases with the increase of well depth in a stroke. The maximum bending stress of the upper carbon fiber rod (0–1650 m) can reach 30 MPa compared with the bottom steel rod (1650–2200 m) 150 MPa. The bending stress of the traditional steel rod (0–1650 m) reaches 80Mpa. Although the bending stress does not exceed their yield limit, the stress of the traditional steel rod in the wellbore is mostly reciprocating wear and fatigue failure. On the contrary, the bending stress of carbon fiber rod is greatly reduced, and the service life of carbon fiber rod is greatly prolonged.


### 4.3.2. Bending Stress in Directional Wells

Based on the above simulation model of carbon-steel hybrid rod string in directional wells, the bending stress of hybrid rod string after transverse vibration deformation in tubing is obtained, as shown in Figure11(a). The second model replaces the upper carbon fiber rod string with steel rod with the same size to obtain the bending stress, as shown in Figure 8(b). It can be seen from Figures 11(a) and 11(b) that, whether it is an integral steel rod or a carbon and steel hybrid rod string, when the sucker rod string reciprocates in the directional well, the bending stress at the inclined section is almost the largest in the whole well.Figure 11
Change of bending stress of carbon fiber hybrid rod string and traditional steel rod string in directional well. (a) Change of bending stress of carbon fiber hybrid rod string. (b) Variation of bending stress of traditional steel rod string.
(a)(b)In the above two comparative models, the maximum bending stress of the above two kinds of rod forms appears near the inclined section. The simulation results are consistent with the fact that the actual rod string is the easiest to be damaged at the inclined section.


## 4.3.1. Bending Stress in Vertical Wells

After further processing of the vertical well numerical simulation results, the bending stress distribution of the rod string after dynamic deformation in the tubing is obtained, as shown in Figure10. We can get the bending stress of new carbon-steel hybrid rod string (1650–2200 m) from Figure 10(a) and the bending stress of new carbon-steel hybrid rod string (0–1650 m) from Figure 10(b), and also bending stress of traditional steel rod string (0–2200 m) from Figure 10(c).Figure 10
Variation of bending stress of new and traditional rod string in vertical wells. (a) Bending stress of new carbon-steel hybrid rod string (1650–2200 m). (b) Bending stress of new carbon-steel hybrid rod string (0–1650 m). (c) Bending stress of traditional steel rod string (0–2200 m).
(a)(b)(c)It can be seen from the figure that the maximum bending stress of carbon-steel rod increases with the increase of well depth in a stroke. The maximum bending stress of the upper carbon fiber rod (0–1650 m) can reach 30 MPa compared with the bottom steel rod (1650–2200 m) 150 MPa. The bending stress of the traditional steel rod (0–1650 m) reaches 80Mpa. Although the bending stress does not exceed their yield limit, the stress of the traditional steel rod in the wellbore is mostly reciprocating wear and fatigue failure. On the contrary, the bending stress of carbon fiber rod is greatly reduced, and the service life of carbon fiber rod is greatly prolonged.


## 4.3.2. Bending Stress in Directional Wells

Based on the above simulation model of carbon-steel hybrid rod string in directional wells, the bending stress of hybrid rod string after transverse vibration deformation in tubing is obtained, as shown in Figure11(a). The second model replaces the upper carbon fiber rod string with steel rod with the same size to obtain the bending stress, as shown in Figure 8(b). It can be seen from Figures 11(a) and 11(b) that, whether it is an integral steel rod or a carbon and steel hybrid rod string, when the sucker rod string reciprocates in the directional well, the bending stress at the inclined section is almost the largest in the whole well.Figure 11
Change of bending stress of carbon fiber hybrid rod string and traditional steel rod string in directional well. (a) Change of bending stress of carbon fiber hybrid rod string. (b) Variation of bending stress of traditional steel rod string.
(a)(b)In the above two comparative models, the maximum bending stress of the above two kinds of rod forms appears near the inclined section. The simulation results are consistent with the fact that the actual rod string is the easiest to be damaged at the inclined section.


## 5. Conclusions

In this paper, the dynamic simulation models of carbon-steel hybrid rod string in vertical wells and in directional wells are established, and the dynamic behavior of hybrid rod string above in tubing is simulated and analyzed with the following conclusions.In vertical wells, the severe collision between the carbon-steel hybrid rod string and the oil tubing is near the bottom, which is consistent with the actual situation of the oilfield. Second, the collision of the upper carbon fiber rod is obviously weak and low, which indicates that the eccentric wear of the carbon-steel hybrid rod string mainly occurs at the bottom of the steel rod. However, the eccentric wear of the traditional pure steel rod string almost occurs in the whole well. Therefore, the eccentric wear of carbon-steel hybrid rod is greatly reduced and also more and more widely used. Again, the stress of bending deformation of rod string in tubing does not exceed the allowable stress of the material itself in vertical wells, which is still deformed within the elastic range. This proves that the failure of the rod string is mainly fatigue wear.In directional wells, the contact force at inclined section is almost at the maximum in the whole well, where the transverse vibrating collision phenomenon is almost the most intense. Second, whether it is a new type of carbon-steel rod string or a traditional pure steel rod string, the bending stress at the inclined section is nearly the largest. Again, carbon fiber sucker rod instead of pure steel rod string can significantly reduce the impact force and prolong the service life of rod string.The transverse vibration simulation analysis in this paper provides the result that the carbon fiber sucker rod itself has low collision contact force, which means that the carbon fiber sucker rod can prolong the pump inspection cycle and improve the service life of oil wells. The research results lay a theoretical foundation for the practical application of carbon fiber sucker rod string in oil field.



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*Source: 5239355-2022-06-29.xml*