# 3D-Dynamic Modelling and Performance Analysis of Service Behavior for Beam Pumping Unit

Authors: Feng Zi-Ming; Tan Jing-Jing; Sun Yanan; Zhang De-Shi; Duan Wei-Bo
Journal: Mathematical Problems in Engineering
 (2018)

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## Abstract

In consideration of the rod, the tube, and the liquid column, a 3D dynamic model was established, which could be expressed as a set of partial differential equations. A measured torque curve and a calculated torque curve of Nan1-2-22 oil-well in Daqing oilfield were contrasted with each other which improved the rationality of this model. At last, we researched the influence of the stroke and the frequency of stroke on the displacement of rod, suspension velocity, suspension acceleration, polish rod load, and net torque of gearbox. This 3D dynamic model has a higher calculated accuracy and veracity and could be used to design and optimize the structure of rod pumping and the working process of pumping wells.


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## Body

## 1. Introduction

A fast and accurate calculation of polished rod load was the prerequisite for optimization design of type selection, the reasonable matching design, fault diagnosis, and intelligent control of the beam pumping well system.The earliest rod pumping system design was semiempirical design methods, such as “API Specification for Pumping Units”. This method relied on the plunger diameter, the static fluid load, the rod size(s), the dynamic force, and the friction loads, which were all calculated by the semiempirical formulation. The semiempirical formulation had a lot of limitation for refined calculation. The first semiempirical modelling of rod pumping system was done by Kemelor [1]. Their efforts were then concentrated on the construction of an electrical analogue. Halderson [2] also established an analogue model. Many analogue models were built, but none of them completely and accurately solved the sucker-rod pump problem.Norton [3] developed an analytical solution by an approximation method. This method was partially successful but was never widely applied. The next major development was by Snyder [4], who used a numerical technique to calculate the down hole force and displacement. This method was primarily for diagnosis of operating problem in existing wells. In 1963, Gibbs [5] presented a method that suitably generalized for a wider range of application. Many companies, such as Lufkin Foundry and Machine Company, made this method to be available as a commercial serviced by Sucker Rod Pump Analysis. It is a numerical technique programmed for solution on a digital computer.Chacin and Purcupile [6] dispersed the rod string to be the spring mass system with damping, and they established the ordinary differential equations to describe the lumped mass element vibration law, and they established the system simulation model by use of the numerical integral method. In 1983, Doty and Schmidt [7] established a two-dimensional model of the coupled vibration of rod string and liquid column.Lelia and Evans [8] had conducted further research about dynamic forecasting model of rod string and liquid column with coupling motion. They had carried on two hypotheses to the liquid column: one is that the liquid column was a single phase incompressible liquid, two is that the liquid column was a single-phase microcompressible, and it could be used difference method to calculate the numerical solution. In 1988, Yu [9] considered the fact of general unanchor of oil tubing in China; he comprehensively considered the sucker rod, liquid column, and the tubing string and established a 3D vibration model for prediction of polished rod load, but its limit condition for calculation was limiting its scope of application.In 2010, Shardakov et al. [10] developed a new mathematical model of longitudinal vibrations of the sucker rod string and its numerical implementation. Its model can take into account strongly nonlinear forces resulting from pump valves and Coulomb’s friction. The numerical results indicated that it shows rather good agreement between the numerical and experimental results. In 2013, Jiang et al. [11] developed a coupling mathematical optimized model of the prime motor and the walking beam pumping units to analyze the dynamics performance. In 2015, Ferrigno et al. [12] proposed a calculation algorithm using a combination of the motor performance analysis and the calculations based on API 11E, allowing us to determine the real torque of units in real time from telemetry, eliminating the need to make on-site surveys of the counterweighting of the unit.In 2016, Lao and Zhou [13] developed a new direct calculation method that directly calculates the fluid force acting on the curved cylindrical surface of the rod element. They used the pump dynamometer cards as boundary conditions and solved the wave equations for sucker-rod pumping with more accuracy than before. In 2016, considering the limitation of simulation model of the deep well and ultradeep well, Xing [14] developed an improved simulation model of sucker rod pumping system. Xing concluded that, comparing with the steel rod, carbon fiber, and fiberglass rod, the resonant phenomenon of single rod is more likely to happen for the wire rope sucker rod. However, when sucker rod is double stage rod, the resonant phenomenon of fiberglass rod is more likely to happen than other rods.In this paper, considering the static and dynamic and friction forces of the rod, the tube, and the liquid column, we established a mathematical calculation model named 3D dynamic wave model which was made up of a set of partial differential equations. By programming this dynamic model, we researched the impact of stroke and frequency of stroke on suspension velocity, suspension acceleration, polished rod load, and net torque of gearbox of CYJY10-3-37HB rod pumping. At the same time, the calculated data by this dynamic model had good meeting with the measured data. It provided an optional theoretical support for the type-selection and optimization design, the reasonable matching design, the fault diagnosis, and the intelligent control of the oil pumping well system.


## 2. Dynamics Model of Pumping Unit System

The polished rod load of pumping unit was the main basis factor for the optimum design and the swabbing technology design. The polished rod load was made up of the weight of the sucker rod and the liquid column, the inertia load, the load of vibration load, and the friction load. In order to calculate these loads accurately, the mechanical model of rod string was established, and it analyzed the influence factors, respectively. The suspended displacement, the suspended velocity, and the suspended acceleration were depicted in the literatures [15].


### 2.1. Rod-Tube-Fluid 3D Coupling Vibration Model

In order to simplify the dynamic model of rod pump system, the following were assumed:(i)
The beam pumping units are our research object, where rotate speed of gearbox crank is a constant variable.(ii)
There are no gassy bubbles in the liquid column and the liquid densityρf is a constant.(iii)
The resistance of valve is ignored.(iv)
The dynamic viscosity of liquid columnη, the back pressure of wellhead P0, and the intake pressure of pump P1 are all constants.


#### 2.1.1. Dynamic Model of the Oil Rod

The rod element force diagram was as shown in Figure1(a); we can see from the dynamic force equilibrium: (1)ρrAr∂vr∂t=∂Qr∂x+ρrArg1-ρfρr-FrBy the Hooke’s law, the inner force relation of oil rod can be achieved: (2)Qr=ErAr∂u∂xThe following equation can be achieved by a partial derivative with time to the above equation: (3)ErAr∂vr∂x=∂Qr∂twherevr(x,t) is rod velocity, m/s;Qr(x,t) is inner force of rod, N;Er is rigidity of rod, N/m2;Ar is sectional area of rod, m2;ρr is density of rod, kg/m3;ρf is liquid density, kg/m3;Fr is resistance met with rod, N/m;Ff is resistance acted on the liquid, N/m.Figure 1
Dynamic model of rod and liquid column.


#### 2.1.2. Dynamic Model of the Oil Tube

A dynamic analysis of tube element was similar to rod model; two partial differential equations depicted rod movement was achieved as follows:(4)ρrAh-At∂vt∂t=∂Qt∂xρtgAh-At-Ft(5)EtAh-At∂vt∂x=∂Qt∂twherevt(x,t) is tube velocity, m/s;Qt(x,t) is inner force of tube, N;Et is rigidity of tube, N/m2;Ft is resistance met with tube, N/m2;At is inner area of tube, m2;Ah is outer area of tube, m2;ρt is density of tube, kg/m3.


#### 2.1.3. Dynamic Model of Liquid Column

By Assumption (2), the liquid column was treated as elastomer element. The force analysis of liquid element was shown in Figure 1(b); in accordance with force equilibrium condition, the kinematic equation of liquid column was as follows:(6)ρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-Argand(7)Ef∂vf∂x=-∂Pf∂twherevf(x,t) is liquid column velocity, m/s;Pf is pressure of liquid, N/m2;Ff is assistance met with liquid column, N.Combinating (1) to (7), a set of mathematics models depicted the movement of rod-tube-liquid was achieved as follows:(8)ρrAr∂vr∂t=∂fr∂x+ρrArg1-ρfρr-FrErAr∂vr∂x=∂fr∂tρrAh-At∂vt∂t=∂ft∂xρtgAh-At-FtEtAh-At∂vt∂x=∂ft∂tρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-ArgEf∂vf∂x=-∂Pf∂tThe differential equations (8) are a three-dimensional wave mathematics model described the rod-tube-liquid column that can be used to calculate the forces and displacement at arbitrary section of rod.


### 2.2. Calculation of Damping Force Effected on the Oil Rod

The damping forces of the rod included three parts, of which the viscosity forceFrf acts on the per unit length of rod surface by the liquid; the viscosity force Fcf acts on the rod coupling; and the friction force Fr acts on the per unit length of rod by the tube. The friction force was important depending on the well slope, but difficult to calculate.The viscosity force action on the per unit length of the rod by liquid was as follows:(9)Frf=12ρfvfvfπDrC1The damping force acting on the every rod couplings by liquid was as follows:(10)Fc=12ρfvfvfAc-ArC2Assuming that the length of a rod was l, then the damping force acting on the convert unit length of rod was as follows:(11)Fcf=ρfvfvfAc-ArC22lSo, the resistance force of the rod was(12)Fr=Fcf+Frf=ρfvfvfAc-ArC22l+12ρfvfvfπDrC1where C1and C2 were the nondimensional damping factors of the rod and the coupling, respectively.(13)C1=24Re1±Re′Re0.2+0.39·DrDt(14)C2=5.2×104Dc/Dt-0.3812.77±1.69Re′/ReRewhereDr is the diameter of rod;Dt is the inner diameter of tube.Reynolds numbersRe and Re′ were related to the liquid velocity and the rod velocity, which were calculated by the following equations, respectively.(15)Re=vfDt-Drρfμ(16)Re′=vrDt-Drρfμwhereμ is the dynamic viscosity of liquid, Pa·s.Equations (13)-(16) were put in (12), so Fr was as follows:(17)Fr=12ηπDrDt-Dr+2.77×5.2×10424DcDt-0.3812.57π4Dc2-Dr2Dt-Drlvf±12η·πDrDt-Dr0.2+0.39DrDt+2.77×0.61×5.2×10424DcDt-0.3812.57π4Dc2-Dr2Dt-DrlvrWhen vf and vr had the same sign, they are positive or otherwise negative sign, so the above equation was as follows at last: (18)Fr=br·vr-bfr·vf(19)br=12πη0.2+0.39·DrDt+2.19724·DcDr-0.3812.57·Dc/Dr2-11/Dr·1Dt/Dr-1(20)bfr=12πη1+1.601×10424DcDt-0.3812.57·Dc/Dr2-11/Dr·1Dt/Dr-1In a similar way, the resistance force acting on the tube was as follows:(21)Ft=btvt-bftvf(22)bt=12πη0.2+0.39DrDt1Dt/Dr-1(23)bft=12πη·1Dt/Dr-1And the resistance force acting on the liquid column was as follows:(24)Ff=-Fr+Ft


### 2.3. Gearbox Net Torque

The gearbox output axial-torque was made of polished rod load torque, balance torque, walking bean inertial torque, and crank inertial torque. When the working velocity is constant, the calculate formula generally ignored the influent of walking beam inertia and crank inertia [15].(25)Tnh=ηbmW-B+JbAεbTF¯-Msin⁡θ+τ+Jp3ε


## 2.1. Rod-Tube-Fluid 3D Coupling Vibration Model

In order to simplify the dynamic model of rod pump system, the following were assumed:(i)
The beam pumping units are our research object, where rotate speed of gearbox crank is a constant variable.(ii)
There are no gassy bubbles in the liquid column and the liquid densityρf is a constant.(iii)
The resistance of valve is ignored.(iv)
The dynamic viscosity of liquid columnη, the back pressure of wellhead P0, and the intake pressure of pump P1 are all constants.


### 2.1.1. Dynamic Model of the Oil Rod

The rod element force diagram was as shown in Figure1(a); we can see from the dynamic force equilibrium: (1)ρrAr∂vr∂t=∂Qr∂x+ρrArg1-ρfρr-FrBy the Hooke’s law, the inner force relation of oil rod can be achieved: (2)Qr=ErAr∂u∂xThe following equation can be achieved by a partial derivative with time to the above equation: (3)ErAr∂vr∂x=∂Qr∂twherevr(x,t) is rod velocity, m/s;Qr(x,t) is inner force of rod, N;Er is rigidity of rod, N/m2;Ar is sectional area of rod, m2;ρr is density of rod, kg/m3;ρf is liquid density, kg/m3;Fr is resistance met with rod, N/m;Ff is resistance acted on the liquid, N/m.Figure 1
Dynamic model of rod and liquid column.


### 2.1.2. Dynamic Model of the Oil Tube

A dynamic analysis of tube element was similar to rod model; two partial differential equations depicted rod movement was achieved as follows:(4)ρrAh-At∂vt∂t=∂Qt∂xρtgAh-At-Ft(5)EtAh-At∂vt∂x=∂Qt∂twherevt(x,t) is tube velocity, m/s;Qt(x,t) is inner force of tube, N;Et is rigidity of tube, N/m2;Ft is resistance met with tube, N/m2;At is inner area of tube, m2;Ah is outer area of tube, m2;ρt is density of tube, kg/m3.


### 2.1.3. Dynamic Model of Liquid Column

By Assumption (2), the liquid column was treated as elastomer element. The force analysis of liquid element was shown in Figure 1(b); in accordance with force equilibrium condition, the kinematic equation of liquid column was as follows:(6)ρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-Argand(7)Ef∂vf∂x=-∂Pf∂twherevf(x,t) is liquid column velocity, m/s;Pf is pressure of liquid, N/m2;Ff is assistance met with liquid column, N.Combinating (1) to (7), a set of mathematics models depicted the movement of rod-tube-liquid was achieved as follows:(8)ρrAr∂vr∂t=∂fr∂x+ρrArg1-ρfρr-FrErAr∂vr∂x=∂fr∂tρrAh-At∂vt∂t=∂ft∂xρtgAh-At-FtEtAh-At∂vt∂x=∂ft∂tρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-ArgEf∂vf∂x=-∂Pf∂tThe differential equations (8) are a three-dimensional wave mathematics model described the rod-tube-liquid column that can be used to calculate the forces and displacement at arbitrary section of rod.


## 2.1.1. Dynamic Model of the Oil Rod

The rod element force diagram was as shown in Figure1(a); we can see from the dynamic force equilibrium: (1)ρrAr∂vr∂t=∂Qr∂x+ρrArg1-ρfρr-FrBy the Hooke’s law, the inner force relation of oil rod can be achieved: (2)Qr=ErAr∂u∂xThe following equation can be achieved by a partial derivative with time to the above equation: (3)ErAr∂vr∂x=∂Qr∂twherevr(x,t) is rod velocity, m/s;Qr(x,t) is inner force of rod, N;Er is rigidity of rod, N/m2;Ar is sectional area of rod, m2;ρr is density of rod, kg/m3;ρf is liquid density, kg/m3;Fr is resistance met with rod, N/m;Ff is resistance acted on the liquid, N/m.Figure 1
Dynamic model of rod and liquid column.


## 2.1.2. Dynamic Model of the Oil Tube

A dynamic analysis of tube element was similar to rod model; two partial differential equations depicted rod movement was achieved as follows:(4)ρrAh-At∂vt∂t=∂Qt∂xρtgAh-At-Ft(5)EtAh-At∂vt∂x=∂Qt∂twherevt(x,t) is tube velocity, m/s;Qt(x,t) is inner force of tube, N;Et is rigidity of tube, N/m2;Ft is resistance met with tube, N/m2;At is inner area of tube, m2;Ah is outer area of tube, m2;ρt is density of tube, kg/m3.


## 2.1.3. Dynamic Model of Liquid Column

By Assumption (2), the liquid column was treated as elastomer element. The force analysis of liquid element was shown in Figure 1(b); in accordance with force equilibrium condition, the kinematic equation of liquid column was as follows:(6)ρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-Argand(7)Ef∂vf∂x=-∂Pf∂twherevf(x,t) is liquid column velocity, m/s;Pf is pressure of liquid, N/m2;Ff is assistance met with liquid column, N.Combinating (1) to (7), a set of mathematics models depicted the movement of rod-tube-liquid was achieved as follows:(8)ρrAr∂vr∂t=∂fr∂x+ρrArg1-ρfρr-FrErAr∂vr∂x=∂fr∂tρrAh-At∂vt∂t=∂ft∂xρtgAh-At-FtEtAh-At∂vt∂x=∂ft∂tρfAt-Ar∂vf∂t=-At-Ar∂pf∂x-Ff+ρfAt-ArgEf∂vf∂x=-∂Pf∂tThe differential equations (8) are a three-dimensional wave mathematics model described the rod-tube-liquid column that can be used to calculate the forces and displacement at arbitrary section of rod.


## 2.2. Calculation of Damping Force Effected on the Oil Rod

The damping forces of the rod included three parts, of which the viscosity forceFrf acts on the per unit length of rod surface by the liquid; the viscosity force Fcf acts on the rod coupling; and the friction force Fr acts on the per unit length of rod by the tube. The friction force was important depending on the well slope, but difficult to calculate.The viscosity force action on the per unit length of the rod by liquid was as follows:(9)Frf=12ρfvfvfπDrC1The damping force acting on the every rod couplings by liquid was as follows:(10)Fc=12ρfvfvfAc-ArC2Assuming that the length of a rod was l, then the damping force acting on the convert unit length of rod was as follows:(11)Fcf=ρfvfvfAc-ArC22lSo, the resistance force of the rod was(12)Fr=Fcf+Frf=ρfvfvfAc-ArC22l+12ρfvfvfπDrC1where C1and C2 were the nondimensional damping factors of the rod and the coupling, respectively.(13)C1=24Re1±Re′Re0.2+0.39·DrDt(14)C2=5.2×104Dc/Dt-0.3812.77±1.69Re′/ReRewhereDr is the diameter of rod;Dt is the inner diameter of tube.Reynolds numbersRe and Re′ were related to the liquid velocity and the rod velocity, which were calculated by the following equations, respectively.(15)Re=vfDt-Drρfμ(16)Re′=vrDt-Drρfμwhereμ is the dynamic viscosity of liquid, Pa·s.Equations (13)-(16) were put in (12), so Fr was as follows:(17)Fr=12ηπDrDt-Dr+2.77×5.2×10424DcDt-0.3812.57π4Dc2-Dr2Dt-Drlvf±12η·πDrDt-Dr0.2+0.39DrDt+2.77×0.61×5.2×10424DcDt-0.3812.57π4Dc2-Dr2Dt-DrlvrWhen vf and vr had the same sign, they are positive or otherwise negative sign, so the above equation was as follows at last: (18)Fr=br·vr-bfr·vf(19)br=12πη0.2+0.39·DrDt+2.19724·DcDr-0.3812.57·Dc/Dr2-11/Dr·1Dt/Dr-1(20)bfr=12πη1+1.601×10424DcDt-0.3812.57·Dc/Dr2-11/Dr·1Dt/Dr-1In a similar way, the resistance force acting on the tube was as follows:(21)Ft=btvt-bftvf(22)bt=12πη0.2+0.39DrDt1Dt/Dr-1(23)bft=12πη·1Dt/Dr-1And the resistance force acting on the liquid column was as follows:(24)Ff=-Fr+Ft


## 2.3. Gearbox Net Torque

The gearbox output axial-torque was made of polished rod load torque, balance torque, walking bean inertial torque, and crank inertial torque. When the working velocity is constant, the calculate formula generally ignored the influent of walking beam inertia and crank inertia [15].(25)Tnh=ηbmW-B+JbAεbTF¯-Msin⁡θ+τ+Jp3ε


## 3. Dynamic Performance Analysis of Beam Pumping Unit

### 3.1. Comparison between Measured Data and Calculated Data

Figure2 was the net torque curves of Nan1-2-22 oil-well in Daqing oilfield, which were measured and calculated, respectively. Its rod pumping was CYJ10-3-37HB running with 3 stroke, 6 frequency of stroke, and 990 m pump depth. The calculated torque curve was calculated by the 3D rod-tube-liquid column wave equation built in this paper. Seen from Figure 2, the two curves of torque had the similar variation tendency that proved the 3D wave equation could be used to design the beam pumping units of oilfield.Figure 2
Torque comparison of Nan1-2-22 between measured data and calculated data.


### 3.2. Basic Structure Parameters and Swabbing Parameters

CYJY10-3-37HB was selected as objects to analyze its performance; the structure parameters and swabbing parameters were shown in Table1 and Table 2, respectively.Table 1
Structure parameters and swabbing parameters.
Structure Parameters Value Fore-arm Length (mm) 3000 Aft-arm Length (mm) 1920 Linkage Rod Length (mm) 3350 Horizontal Throw (mm) 2500 Crank Radius (mm) 880/740/600 Centre-Height (mm) 5290Table 2
Oil well condition and swabbing parameters.
Swabbing Parameters Value Frequency of stroke (min−1) 3, 6, 9 Stroke (m) 2, 2.5, 3 Depth of Plunger (m) 980 Working Fluid Level (m) 550 Pump Diameter (mm) 56 Rod Diameter (mm) 19/22 Tube Diameter (mm) 76 Water Cut (%) 92


### 3.3. Analysis of Performance of CYJY10-3-37HB

The stroke length of beam pumping units was decided by the length of crank. For a specific type of pumping unit, the crank length was correlated with strokes one-to-one. It was a linear proportional relationship between the suspension velocity and length of crank, with the increase of stroke; the absolute peak value of suspension velocity (peak value and valley value) increased. From Figure3 we could see that, on the upstroke, the peak velocity shifted to 70 degrees of the crank angle. It is shown that the larger stroke was not of benefit for the actual balance effect to the beam pumping unit.Figure 3
Impact of stroke on the suspension velocity.For CYJY10-3-37HB, the crank length determined the stroke size. From Figure4, we could see that the direct proportion relationship between the stroke and the suspension acceleration was linear; the peak values of the acceleration curve of the three strokes obviously reflected the linear proportional relationship between them. The suspension acceleration was relatively larger near the top dead center; at this point the additional load also was large; therefore, it was noted that the start pumping point should avoid the top dead center.Figure 4
Impact of stroke on the suspension acceleration.The pumping velocity reflects the rotation speed of electrical motor; the rotation speed was also the crank speed. The suspension peak velocity was direct proportion to frequency of stroke. The peak values of the three curves can be seen from Figure5; the change of frequency of stroke did not change the phase angle of the peak suspension velocity on the upstroke, and the position of the crank angle was generally located at 85 degree. Therefore, the phase angle of the balance weight was not affected by the frequency of stroke, but it affects the weight of the counterweight.Figure 5
Impact of the frequency of stroke on the suspension velocity.Figure6 showed that the frequency of stroke is quadratic proportional to suspension acceleration. With the frequency of stroke increasing, suspension acceleration would rapidly increase. Therefore, the increasing of frequency of stroke would cause a sharp increase of dynamic polished rod load. Especially at the top dead point, suspension acceleration increased very significantly.Figure 6
Impact of frequency of stroke on suspension acceleration.As shown in Figure7, the impact of stroke on the maximum and minimum polished rod load was not large; comparing to 2m, the maximum polished rod load of 2.5m and 3m stroke increased by 1.37% and 4.66%, respectively, and the minimum polished rod load reduced by 4.64% and 8.80%, respectively. With the stroke increasing, the entire work area increased.Figure 7
Impact of stroke on the polished rod load.As shown in Figure8, the impact of frequency of stroke on the maximum and minimum polished rod load was very obvious. Comparing to the 3 frequency of stroke, the maximum polished rod load of 6 and 9 frequency of stroke increased by 10.26% and 22.31%, respectively, the minimum load decreased by 9.61% and 19.62%, respectively. Increasing of frequency of stroke would increase the suspension acceleration, so that the inertial load would increase. This also contributed to the rapid increasing of polished rod load with the increase of the frequency of stroke.Figure 8
Impact of frequency of stroke on polished rod load.Figure9 was a diagram of the torque curves comparison with different frequency of stroke in the case where the torque balance (torque balance is the ratio between the downstroke and upstroke peak torques) was one. With the frequency of stroke increasing, the peak torque increased. Comparing to 3 frequency of stroke, the maximum torque of 6 and 9 frequency of stroke increased by 16.98% and 65.03%, respectively, but the valley values were all small. The structure features of CYJY10-3-37HB pumping unit could not avoid the negative torque mainly distributed in the scope of 102 degrees to 135 degrees and nearly the dead point. The increasement of frequency of stroke would have bigger influence on the torque curves.Figure 9
Impact on torque by frequency of stroke.Figure10 shows the effect of stroke on torque curve of beam pumping unit when the torque degree of balance was one. Increasement of the stroke could cause a larger increase of peak torque, comparing to the 2m and the maximum torque of 2.5m and 3m stroke increased by 30.68% and 69.27%, respectively. The absolute valley value increased very little; only the 3m stroke was more obvious than the other two. Seen from the increasement ratio, stroke would influence the torque more than the frequency of stroke, especially the negative value in the valley much more than the frequency of stroke.Figure 10
Stroke’s impact on torque.


## 3.1. Comparison between Measured Data and Calculated Data

Figure2 was the net torque curves of Nan1-2-22 oil-well in Daqing oilfield, which were measured and calculated, respectively. Its rod pumping was CYJ10-3-37HB running with 3 stroke, 6 frequency of stroke, and 990 m pump depth. The calculated torque curve was calculated by the 3D rod-tube-liquid column wave equation built in this paper. Seen from Figure 2, the two curves of torque had the similar variation tendency that proved the 3D wave equation could be used to design the beam pumping units of oilfield.Figure 2
Torque comparison of Nan1-2-22 between measured data and calculated data.


## 3.2. Basic Structure Parameters and Swabbing Parameters

CYJY10-3-37HB was selected as objects to analyze its performance; the structure parameters and swabbing parameters were shown in Table1 and Table 2, respectively.Table 1
Structure parameters and swabbing parameters.
Structure Parameters Value Fore-arm Length (mm) 3000 Aft-arm Length (mm) 1920 Linkage Rod Length (mm) 3350 Horizontal Throw (mm) 2500 Crank Radius (mm) 880/740/600 Centre-Height (mm) 5290Table 2
Oil well condition and swabbing parameters.
Swabbing Parameters Value Frequency of stroke (min−1) 3, 6, 9 Stroke (m) 2, 2.5, 3 Depth of Plunger (m) 980 Working Fluid Level (m) 550 Pump Diameter (mm) 56 Rod Diameter (mm) 19/22 Tube Diameter (mm) 76 Water Cut (%) 92


## 3.3. Analysis of Performance of CYJY10-3-37HB

The stroke length of beam pumping units was decided by the length of crank. For a specific type of pumping unit, the crank length was correlated with strokes one-to-one. It was a linear proportional relationship between the suspension velocity and length of crank, with the increase of stroke; the absolute peak value of suspension velocity (peak value and valley value) increased. From Figure3 we could see that, on the upstroke, the peak velocity shifted to 70 degrees of the crank angle. It is shown that the larger stroke was not of benefit for the actual balance effect to the beam pumping unit.Figure 3
Impact of stroke on the suspension velocity.For CYJY10-3-37HB, the crank length determined the stroke size. From Figure4, we could see that the direct proportion relationship between the stroke and the suspension acceleration was linear; the peak values of the acceleration curve of the three strokes obviously reflected the linear proportional relationship between them. The suspension acceleration was relatively larger near the top dead center; at this point the additional load also was large; therefore, it was noted that the start pumping point should avoid the top dead center.Figure 4
Impact of stroke on the suspension acceleration.The pumping velocity reflects the rotation speed of electrical motor; the rotation speed was also the crank speed. The suspension peak velocity was direct proportion to frequency of stroke. The peak values of the three curves can be seen from Figure5; the change of frequency of stroke did not change the phase angle of the peak suspension velocity on the upstroke, and the position of the crank angle was generally located at 85 degree. Therefore, the phase angle of the balance weight was not affected by the frequency of stroke, but it affects the weight of the counterweight.Figure 5
Impact of the frequency of stroke on the suspension velocity.Figure6 showed that the frequency of stroke is quadratic proportional to suspension acceleration. With the frequency of stroke increasing, suspension acceleration would rapidly increase. Therefore, the increasing of frequency of stroke would cause a sharp increase of dynamic polished rod load. Especially at the top dead point, suspension acceleration increased very significantly.Figure 6
Impact of frequency of stroke on suspension acceleration.As shown in Figure7, the impact of stroke on the maximum and minimum polished rod load was not large; comparing to 2m, the maximum polished rod load of 2.5m and 3m stroke increased by 1.37% and 4.66%, respectively, and the minimum polished rod load reduced by 4.64% and 8.80%, respectively. With the stroke increasing, the entire work area increased.Figure 7
Impact of stroke on the polished rod load.As shown in Figure8, the impact of frequency of stroke on the maximum and minimum polished rod load was very obvious. Comparing to the 3 frequency of stroke, the maximum polished rod load of 6 and 9 frequency of stroke increased by 10.26% and 22.31%, respectively, the minimum load decreased by 9.61% and 19.62%, respectively. Increasing of frequency of stroke would increase the suspension acceleration, so that the inertial load would increase. This also contributed to the rapid increasing of polished rod load with the increase of the frequency of stroke.Figure 8
Impact of frequency of stroke on polished rod load.Figure9 was a diagram of the torque curves comparison with different frequency of stroke in the case where the torque balance (torque balance is the ratio between the downstroke and upstroke peak torques) was one. With the frequency of stroke increasing, the peak torque increased. Comparing to 3 frequency of stroke, the maximum torque of 6 and 9 frequency of stroke increased by 16.98% and 65.03%, respectively, but the valley values were all small. The structure features of CYJY10-3-37HB pumping unit could not avoid the negative torque mainly distributed in the scope of 102 degrees to 135 degrees and nearly the dead point. The increasement of frequency of stroke would have bigger influence on the torque curves.Figure 9
Impact on torque by frequency of stroke.Figure10 shows the effect of stroke on torque curve of beam pumping unit when the torque degree of balance was one. Increasement of the stroke could cause a larger increase of peak torque, comparing to the 2m and the maximum torque of 2.5m and 3m stroke increased by 30.68% and 69.27%, respectively. The absolute valley value increased very little; only the 3m stroke was more obvious than the other two. Seen from the increasement ratio, stroke would influence the torque more than the frequency of stroke, especially the negative value in the valley much more than the frequency of stroke.Figure 10
Stroke’s impact on torque.


## 4. Conclusion

To accurately and reliably calculate the dynamic load of the rod pumping, we considered the rod, the tube, and the liquid column and established a 3D dynamic wave model of rod pumping, which were made up of a set of partial differential equations. By a comparison between the tested torque curve and the calculated torque curve, this advanced model was proved to be more reliable and more accurate than other semiempirical model. We analyzed the working performance of beam pumping units with type of CYJY10-3-37HB. Calculated results indicated that, with the increasing of stroke and frequency of stroke, suspension peak velocity, suspension peak acceleration, polished rod load, and peak torque of gearbox increased. Stroke effect on peak torque of gearbox, which is very important for system optimization design, was much bigger than the effect of the frequency of stroke. This 3D dynamic wave model considered the liquid column load in this paper had higher accuracy than the semiempirical, 1D and 2D equations. This paper provided a valuable theoretical model for the pumping well system. In the future, we may improve this 3D model to be suitable for deviated wells and horizontal wells, also to be suitable for high gas fractions wells.



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*Source: 9205251-2018-07-12.xml*