This document summarizes an application of viscous oil in rod sucker pump systems. It describes how artificial lift is used to increase production rates in oil and gas wells as reservoir pressure declines over time. Sucker rod pumps are a common type of artificial lift, and the API-RP 11L procedure is used to design pumping units by calculating parameters like polished rod loads and torque. However, the original procedure does not account for fluid viscosity. The author developed a computer simulator based on the API-RP 11L procedure to study the effects of viscosity on rod loads and torque. The results showed that viscous fluids can significantly increase polished rod loads and torque requirements. Understanding these viscosity effects is important for properly designing pumping units for heavy oil
Well testing provides essential information for characterizing oil and gas reservoirs and evaluating their economic potential. It involves short-term production of reservoir fluids to estimate deliverability and analyze pressure transients caused by changes in flow rates. Integrated analysis of multiple well tests helps optimize development by assessing near-wellbore conditions, estimating reservoir boundaries and drive mechanisms, and characterizing permeability. Modern testing combines downhole measurements and computer analysis to maximize information about the reservoir.
This resume is for Raafat Sayed Ahmed Bashandy, an Egyptian petroleum engineer with over 15 years of experience. He has a BSc in Petroleum Engineering from Cairo University. His experience includes working as a Production Technology Engineer for Qarun Petroleum Company since 2007 where he has led hydraulic fracturing and artificial lift selection projects. He also has experience working as a Production Engineer and consultant for other Egyptian oil companies. His responsibilities have included well operations, production optimization, and economic evaluations.
Sucker rod pumping short course!!! ~downhole diagnosticenLightNme888
Β
Six-page Petroleum Engineering info-graphic detailing Sucker Rod Pumping of Oil Wells and how to effectively design, operate, and optimize the well's producing efficiency. This is an amazing reference guide for anyone involved with Beam Lift as a means of Artificial Lift!!
www.downholediagnostic.com
Comparison of API610 12th and 11th Editions (1).pdfyusuf699644
Β
This document provides a summary and comparison of key changes between the 12th and 11th editions of API 610, which specifies requirements for centrifugal pumps used in the petroleum, petrochemical, and gas industries. The 12th edition was recently released in January 2021. Some notable changes include new requirements focusing on improved equipment reliability, the introduction of API 691 references, and clarification of parallel pump operation requirements to help ensure pumps operate continuously within their preferred ranges. The presentation also highlights potential issues with pump selection if curve shapes and tolerances are not properly considered.
IRJET- Modelling, Simulation and Testing of Diesel Engine Water PumpIRJET Journal
Β
This document discusses modeling, simulation, and testing of a diesel engine water pump using computational fluid dynamics (CFD). The objective was to obtain a higher head than existing pumps to increase cooling efficiency in diesel engines. The researchers conducted CFD simulations of modifications to the pump design, including adding a splitter to the outlet and increasing or angling the vanes. The simulations predicted increases in head of up to 7 meters with these modifications. The modified design was then experimentally tested and the results were compared to the CFD simulations to validate the model. The increased efficiency was expected to enable more rapid cooling and faster heat dissipation in diesel engines.
Production Optimization using nodal analysis. The nodal systems analysis approach is a very flexible method
that can be used to improve the performance of many well
systems. The nodal systems analysis approach may be used to analyze
many producing oil and gas well problems. The procedure can
be applied to both flowing and artificial
This document provides a preface and overview for a textbook on petroleum production engineering. It discusses how modern computer technologies have revolutionized the petroleum industry and motivated the authors to write this textbook. The textbook is intended to provide production engineers with guidelines for designing, analyzing, and optimizing petroleum production systems using computer-assisted approaches. It covers topics like well performance, artificial lift methods, and production enhancement techniques across 18 chapters in 4 parts. The preface provides details on the intended audience, topics covered, and goals of presenting engineering principles through examples and companion computer programs.
Well testing provides essential information for characterizing oil and gas reservoirs and evaluating their economic potential. It involves short-term production of reservoir fluids to estimate deliverability and analyze pressure transients caused by changes in flow rates. Integrated analysis of multiple well tests helps optimize development by assessing near-wellbore conditions, estimating reservoir boundaries and drive mechanisms, and characterizing permeability. Modern testing combines downhole measurements and computer analysis to maximize information about the reservoir.
This resume is for Raafat Sayed Ahmed Bashandy, an Egyptian petroleum engineer with over 15 years of experience. He has a BSc in Petroleum Engineering from Cairo University. His experience includes working as a Production Technology Engineer for Qarun Petroleum Company since 2007 where he has led hydraulic fracturing and artificial lift selection projects. He also has experience working as a Production Engineer and consultant for other Egyptian oil companies. His responsibilities have included well operations, production optimization, and economic evaluations.
Sucker rod pumping short course!!! ~downhole diagnosticenLightNme888
Β
Six-page Petroleum Engineering info-graphic detailing Sucker Rod Pumping of Oil Wells and how to effectively design, operate, and optimize the well's producing efficiency. This is an amazing reference guide for anyone involved with Beam Lift as a means of Artificial Lift!!
www.downholediagnostic.com
Comparison of API610 12th and 11th Editions (1).pdfyusuf699644
Β
This document provides a summary and comparison of key changes between the 12th and 11th editions of API 610, which specifies requirements for centrifugal pumps used in the petroleum, petrochemical, and gas industries. The 12th edition was recently released in January 2021. Some notable changes include new requirements focusing on improved equipment reliability, the introduction of API 691 references, and clarification of parallel pump operation requirements to help ensure pumps operate continuously within their preferred ranges. The presentation also highlights potential issues with pump selection if curve shapes and tolerances are not properly considered.
IRJET- Modelling, Simulation and Testing of Diesel Engine Water PumpIRJET Journal
Β
This document discusses modeling, simulation, and testing of a diesel engine water pump using computational fluid dynamics (CFD). The objective was to obtain a higher head than existing pumps to increase cooling efficiency in diesel engines. The researchers conducted CFD simulations of modifications to the pump design, including adding a splitter to the outlet and increasing or angling the vanes. The simulations predicted increases in head of up to 7 meters with these modifications. The modified design was then experimentally tested and the results were compared to the CFD simulations to validate the model. The increased efficiency was expected to enable more rapid cooling and faster heat dissipation in diesel engines.
Production Optimization using nodal analysis. The nodal systems analysis approach is a very flexible method
that can be used to improve the performance of many well
systems. The nodal systems analysis approach may be used to analyze
many producing oil and gas well problems. The procedure can
be applied to both flowing and artificial
This document provides a preface and overview for a textbook on petroleum production engineering. It discusses how modern computer technologies have revolutionized the petroleum industry and motivated the authors to write this textbook. The textbook is intended to provide production engineers with guidelines for designing, analyzing, and optimizing petroleum production systems using computer-assisted approaches. It covers topics like well performance, artificial lift methods, and production enhancement techniques across 18 chapters in 4 parts. The preface provides details on the intended audience, topics covered, and goals of presenting engineering principles through examples and companion computer programs.
This thesis investigates production system optimization for submersible pump lifted wells through a case study. A computer program was developed to perform nodal analysis between the reservoir and wellhead, ignoring surface equipment. The program handles pumping of liquid only and liquid with gas. It uses the Hagedorn and Brown correlation to calculate pressures, and the Griffith correlation for bubble flow. The program was applied to 10 wells in the Diyarbakir-GK field, with actual field data input. Outputs were used to evaluate optimum rates, horsepower requirements, and number of pump stages for each well. Comparisons with actual data identified wells operating optimally and inefficiently.
Petroleum Production Engineering, Elsevier (2007) (2).pdfMohammedFouadAmeen
Β
This document provides a preface and overview for a textbook on petroleum production engineering. It was written to provide modern production engineers with information on applying engineering principles to solve problems using computer technologies. The book is organized into four parts covering fundamentals, design principles, artificial lift methods, and production enhancement techniques. It focuses on illustrating principles through examples and provides companion spreadsheet programs to help engineers perform daily work efficiently.
A Comparative CFD Analysis for Air Swirl on Conventional Valve and Modified V...IRJET Journal
Β
1) The document compares the air swirl in a conventional diesel engine valve and a modified valve with skirting using computational fluid dynamics (CFD) analysis.
2) Two engine models are considered - one with a conventional valve and another with a valve that includes added skirting.
3) The CFD analysis finds that the modified valve with skirting produces slightly higher air velocities near the skirting, which leads to increased swirl and turbulence in the cylinder, improving air-fuel mixing compared to the conventional valve design.
IRJET- CFD Flow Analysis of Station PipelineIRJET Journal
Β
This document summarizes a study analyzing the pressure, temperature, and velocity profiles within a station pipeline carrying fuel from booster pumps to a sample point, using computational fluid dynamics (CFD). Three cases were analyzed representing different operating conditions of the booster pumps. The CFD model was developed in ANSYS and divided into two parts due to software limitations. Results showed the pathlines for pressure, temperature, and velocity within the pipeline for each case. Overall, the study used CFD to better understand fuel flow characteristics within the station pipeline under various pump operating scenarios.
IRJET- To Design and Study the Performance Analysis of Single Cylinder Di...IRJET Journal
Β
This document describes a study on the design and performance analysis of a single cylinder diesel engine with variable compression ratio. The study was conducted by modifying a single cylinder diesel engine to allow the compression ratio to be varied between 12-18 by changing the clearance volume using a tilting cylinder head arrangement. Performance tests were conducted on the engine at different compression ratios and the results such as brake power, fuel consumption, efficiencies were compared. The results showed that operating the engine at a lower compression ratio of 15.55:1 using the variable compression ratio technology improved some of the performance parameters compared to a fixed compression ratio of 17.5:1. The document provides details of the methodology, design of the modification, assembly and performance analysis conducted
Performance, Optimization and CFD Analysis of Submersible Pump Impellerijsrd.com
Β
To improve the efficiency of submersible flow pump, Computational Fluid Dynamics (CFD) analysis is one of the advanced tools used in the pump industry. A detailed CFD analysis was done to predict the flow pattern inside the impeller which is an active pump component. From the results of CFD analysis, the velocity and pressure in the outlet of the impeller is predicted. CFD analyses are done using ANSYS CFX software. In this research paper we will modified the impeller design by choosing some parameter.
Reduction of Idle-Hunting in Diesel Fuel Injection PumpIRJET Journal
Β
This document discusses idle hunting in diesel fuel injection pumps. It begins by providing background on diesel fuel injection systems and their components. It then defines idle hunting as engine speed fluctuations above and below the idle speed setting during idling periods. Potential causes of idle hunting are analyzed, including issues related to manufacturing (e.g. improper assembly), materials, and the environment. Data collection methods for investigating idle hunting are presented. Finally, the document describes efforts to address idle hunting specifically in the floating lever component through building trial batches with varying dimensions and testing engine response. Analysis of the trial batches identified a dimension range of 5.6-5.9mm as least prone to causing idle hunting.
IRJET - Review on Design of Intake Manifold for Air Restricted EngineIRJET Journal
Β
This document reviews the design of intake manifolds for restricted engines used in formula racing events. It discusses several papers that analyzed different intake manifold designs through simulations and testing. The key goals of an intake manifold design are to maximize air flow through the restrictor, evenly distribute air to each cylinder, and improve engine performance metrics like volumetric efficiency and torque. The document examines factors like plenum volume, runner length and geometry, and restrictor shape. Simulation tools like Ricardo WAVE, VECTIS and CFD analysis in ANSYS were used to optimize these design parameters and evaluate manifold designs. The reviewed works aimed to enhance engine power output while meeting the restrictor requirement of racing competitions.
IRJET- Finite Element Simulation of Pressurized FluidIRJET Journal
Β
1) The document describes a finite element simulation of a pressurized fluid using the Smoothed Particle Hydrodynamics (SPH) method in ABAQUS software.
2) It specifically models a typical landing gear shock absorber system for a re-entry vehicle undergoing a simulated landing with 3g acceleration.
3) The analysis determines the optimal orifice diameter and fluid to air volume ratio for maximum shock absorption based on the SPH simulation results. An orifice diameter of 10mm showed the best performance.
Centrifugal Pump Impeller Design by Model to Proto Method and Its Performance...IRJET Journal
Β
This document discusses the design of a centrifugal pump impeller to meet customer specifications for supplying water to a city. It begins by outlining the project requirements and site constraints. It then describes the impeller design process using two methods: 1) the model-to-proto scale ratio method from standard JIS B 8327-2002 to predict proto pump performance based on a model pump, and 2) guidelines from a pump design book. Computational fluid dynamics analysis is used to verify the impeller design before manufacturing. Experimental testing will then validate the physical performance compared to the design parameters.
Study of Time Reduction in Manufacturing of Screws Used in Twin Screw PumpIJMERJOURNAL
Β
ABSTRACT: This paper gives the characteristics of Time reduction in manufacturing of screws for Twin screw pumps. Screws are playing a vital role in the performance of pumps, because pumps give the fluids transfer rate with the help of screws. There is a gap in screws which shows its positiveness. This indicates that we are studying about positive displacements pumps. Positive displacements pumps having no point of contact between screws, because of that there will be no any friction formation. Automation is best for development of product to reduce time in manufacturing of any product. In this paper we also tried to explain this feature of Automation to help reduction of time to manufacture of product to increase productivity.
Mihir's handbook of chemical process engineering (Excerpts)MIHIR PATEL, PMP(R)
Β
This book is aim toward all level of chemical engineers this will aid the them to carry out chemical process engineering in a very practical way. The process engineer can use the excel based calculation templates effectively to do correct and proper process design. Chemical engineering is a very vast and complex field. This book aims to simplify the process engineering design. Design of a chemical plant involves one being adept in technical aspects of process engineering. The book aims at making the chemical engineer proficient in the art of process design.
Included are chemical engineering basics on simulation, stoichiometry, fluid property calculation, dimensionless numbers, thermodynamics and on chemical engineering equipment like pump, compressor, steam turbine, gas turbine, flare, motor, fired heater, incinerator, heat exchanger, distillation column, fractionation column, absorber, stripper, packed column, solar evaporation pond, separator. Utility design of nitrogen, compressed air, water, effluent treatment, steam, condensate, desalination, fuel selection is covered.
Many chemical engineering calculations have been included. Special process items like flame arrestor, demister, feed device, pressure reducing and desuperheating station (PRDS), vortex breaker, electric heater, manual valve have been covered.
Process engineering design criteria, process control, material of construction, specialized process studies, safety studies, precommisioning and commissioning have been covered.
Project engineer will also benefit from information provided on types of project (EPC, EPCM, Cost + Fee, etc) as well as interdisciplinary interaction between various engineering disciplines i.e. process, piping, mechanical, instrumentation, electrical, civil and THSE.
Process engineering documentation like process design basis, process philosophies, process flow diagram (PFD), piping and instrumentation diagram (P&ID), block flow diagram (BFD), DP-DT diagram, material selection diagram (MSD), line list, summaries like utility summary, effluent and emission summary, tie in summary and flare relief load summary have been covered with blank templates. Excerpts from few chapters have been provided.
The present work is the numerical investigation of Spark Ignition (SI) engines to
assess the effect of spark plug positions using open source Computational Fluid Dynamics
(CFD) tool, OpenFoam is used. The standard kβΞ΅ turbulence model is used along with
the Reynolds Averaged Navier Stokes equations for simulating the flow field. Average
piston pressure is tracked for different Crank Angles (CA) from β180o to 180o for two
different sized engines (560cc and 70cc). Results clearly show that spark plug position
affects power output of engine. Spark plug position affect p-ΞΈ graph, hence performance
of engine, this effect is dominant in bigger engine than smaller one. Spark plug position
is expressed in dimensionless form in fraction away from centre
This document is a preface to the 16th edition of the Cameron Hydraulic Data book, published by Ingersoll-Rand as an engineering reference. It provides an overview of updates made to the new edition, including expanded data on liquid flow properties and metric conversions. A detailed index is included at the end to allow readers to quickly find relevant data. Engineers are advised to reference this index to locate information needed for pump selection and application work.
IRJET- Design and Analysis of Catalytic Converter of Automobile EngineIRJET Journal
Β
This document summarizes a study on the design and analysis of a catalytic converter for an automobile engine. The researchers designed a baseline catalytic converter model using CAD software and analyzed it using computational fluid dynamics (CFD) to study the pressure and velocity distribution. They found high pressure losses and non-uniform flow distribution. Various modifications to the honeycomb structure diameter, thickness, and position as well as the inlet and outlet design were tested. The optimal design was found to have a centered inlet, conical inlets/outlets, and a honeycomb structure with 30mm holes positioned at the casing mid-length. This design showed improved uniform flow distribution and reduced pressure losses compared to the baseline design.
International Journal of Engineering Research and Applications (IJERA) is an open access online peer reviewed international journal that publishes research and review articles in the fields of Computer Science, Neural Networks, Electrical Engineering, Software Engineering, Information Technology, Mechanical Engineering, Chemical Engineering, Plastic Engineering, Food Technology, Textile Engineering, Nano Technology & science, Power Electronics, Electronics & Communication Engineering, Computational mathematics, Image processing, Civil Engineering, Structural Engineering, Environmental Engineering, VLSI Testing & Low Power VLSI Design etc.
COMPUTATIONAL FLUID DYNAMIC ANALYSIS OF A PULSE JET ENGINEIRJET Journal
Β
1) The document describes a computational fluid dynamics (CFD) analysis of different designs of a pulse jet engine, specifically investigating the impact of increasing the number of fuel inlets.
2) CFD simulations were conducted using ANSYS CFX software on CAD models created in Creo, including designs with single, three, and five fuel inlets.
3) The results show that designs with more fuel inlets generated higher thrust, pressure, and enthalpy compared to the single inlet design, with the five inlet design performing best.
IRJET- Design and Analysis of Multi Port Fuel Injection CNG Engine Manifo...IRJET Journal
Β
This document describes the design and analysis of a multi-port fuel injection compressed natural gas (CNG) engine intake manifold system. The authors designed the manifold using pressure wave tuning theory to determine the optimal runner lengths. Computational fluid dynamics analysis was performed to evaluate the uniformity of the air-fuel mixture distribution and velocity profiles within the manifold. One-dimensional engine simulations were conducted to compare the performance of the new multi-port fuel injection system to the existing single-port system, finding that the multi-port system provided slightly higher power, torque, and volumetric efficiency.
This document summarizes a paper about flumping, a combination of flowing and pumping where a pumped well also flows from the casing-tubing annulus. The paper presents a methodology to calculate the bottom pressure and gas-oil ratio conditions needed to achieve flumping. It applies the methodology to example well data, presenting production rates and efficiencies for different bottom pressures. The results show that flumping can optimize production by allowing simultaneous pumping and annular flow.
The document discusses inlet distortion testing of the PW308 high-bypass turbofan engine. It tested the engine's response to 180-degree and 90-degree inlet total pressure distortion patterns. The testing showed the engine could operate with up to 6% circumferential distortion. A computational model was able to predict the engine's stability limit under distortion conditions within acceptable error margins, though it had more difficulty modeling the radial distortion of the 90-degree pattern. The results indicate the PW308 engine can operate in aircraft with embedded inlets.
This thesis investigates production system optimization for submersible pump lifted wells through a case study. A computer program was developed to perform nodal analysis between the reservoir and wellhead, ignoring surface equipment. The program handles pumping of liquid only and liquid with gas. It uses the Hagedorn and Brown correlation to calculate pressures, and the Griffith correlation for bubble flow. The program was applied to 10 wells in the Diyarbakir-GK field, with actual field data input. Outputs were used to evaluate optimum rates, horsepower requirements, and number of pump stages for each well. Comparisons with actual data identified wells operating optimally and inefficiently.
Petroleum Production Engineering, Elsevier (2007) (2).pdfMohammedFouadAmeen
Β
This document provides a preface and overview for a textbook on petroleum production engineering. It was written to provide modern production engineers with information on applying engineering principles to solve problems using computer technologies. The book is organized into four parts covering fundamentals, design principles, artificial lift methods, and production enhancement techniques. It focuses on illustrating principles through examples and provides companion spreadsheet programs to help engineers perform daily work efficiently.
A Comparative CFD Analysis for Air Swirl on Conventional Valve and Modified V...IRJET Journal
Β
1) The document compares the air swirl in a conventional diesel engine valve and a modified valve with skirting using computational fluid dynamics (CFD) analysis.
2) Two engine models are considered - one with a conventional valve and another with a valve that includes added skirting.
3) The CFD analysis finds that the modified valve with skirting produces slightly higher air velocities near the skirting, which leads to increased swirl and turbulence in the cylinder, improving air-fuel mixing compared to the conventional valve design.
IRJET- CFD Flow Analysis of Station PipelineIRJET Journal
Β
This document summarizes a study analyzing the pressure, temperature, and velocity profiles within a station pipeline carrying fuel from booster pumps to a sample point, using computational fluid dynamics (CFD). Three cases were analyzed representing different operating conditions of the booster pumps. The CFD model was developed in ANSYS and divided into two parts due to software limitations. Results showed the pathlines for pressure, temperature, and velocity within the pipeline for each case. Overall, the study used CFD to better understand fuel flow characteristics within the station pipeline under various pump operating scenarios.
IRJET- To Design and Study the Performance Analysis of Single Cylinder Di...IRJET Journal
Β
This document describes a study on the design and performance analysis of a single cylinder diesel engine with variable compression ratio. The study was conducted by modifying a single cylinder diesel engine to allow the compression ratio to be varied between 12-18 by changing the clearance volume using a tilting cylinder head arrangement. Performance tests were conducted on the engine at different compression ratios and the results such as brake power, fuel consumption, efficiencies were compared. The results showed that operating the engine at a lower compression ratio of 15.55:1 using the variable compression ratio technology improved some of the performance parameters compared to a fixed compression ratio of 17.5:1. The document provides details of the methodology, design of the modification, assembly and performance analysis conducted
Performance, Optimization and CFD Analysis of Submersible Pump Impellerijsrd.com
Β
To improve the efficiency of submersible flow pump, Computational Fluid Dynamics (CFD) analysis is one of the advanced tools used in the pump industry. A detailed CFD analysis was done to predict the flow pattern inside the impeller which is an active pump component. From the results of CFD analysis, the velocity and pressure in the outlet of the impeller is predicted. CFD analyses are done using ANSYS CFX software. In this research paper we will modified the impeller design by choosing some parameter.
Reduction of Idle-Hunting in Diesel Fuel Injection PumpIRJET Journal
Β
This document discusses idle hunting in diesel fuel injection pumps. It begins by providing background on diesel fuel injection systems and their components. It then defines idle hunting as engine speed fluctuations above and below the idle speed setting during idling periods. Potential causes of idle hunting are analyzed, including issues related to manufacturing (e.g. improper assembly), materials, and the environment. Data collection methods for investigating idle hunting are presented. Finally, the document describes efforts to address idle hunting specifically in the floating lever component through building trial batches with varying dimensions and testing engine response. Analysis of the trial batches identified a dimension range of 5.6-5.9mm as least prone to causing idle hunting.
IRJET - Review on Design of Intake Manifold for Air Restricted EngineIRJET Journal
Β
This document reviews the design of intake manifolds for restricted engines used in formula racing events. It discusses several papers that analyzed different intake manifold designs through simulations and testing. The key goals of an intake manifold design are to maximize air flow through the restrictor, evenly distribute air to each cylinder, and improve engine performance metrics like volumetric efficiency and torque. The document examines factors like plenum volume, runner length and geometry, and restrictor shape. Simulation tools like Ricardo WAVE, VECTIS and CFD analysis in ANSYS were used to optimize these design parameters and evaluate manifold designs. The reviewed works aimed to enhance engine power output while meeting the restrictor requirement of racing competitions.
IRJET- Finite Element Simulation of Pressurized FluidIRJET Journal
Β
1) The document describes a finite element simulation of a pressurized fluid using the Smoothed Particle Hydrodynamics (SPH) method in ABAQUS software.
2) It specifically models a typical landing gear shock absorber system for a re-entry vehicle undergoing a simulated landing with 3g acceleration.
3) The analysis determines the optimal orifice diameter and fluid to air volume ratio for maximum shock absorption based on the SPH simulation results. An orifice diameter of 10mm showed the best performance.
Centrifugal Pump Impeller Design by Model to Proto Method and Its Performance...IRJET Journal
Β
This document discusses the design of a centrifugal pump impeller to meet customer specifications for supplying water to a city. It begins by outlining the project requirements and site constraints. It then describes the impeller design process using two methods: 1) the model-to-proto scale ratio method from standard JIS B 8327-2002 to predict proto pump performance based on a model pump, and 2) guidelines from a pump design book. Computational fluid dynamics analysis is used to verify the impeller design before manufacturing. Experimental testing will then validate the physical performance compared to the design parameters.
Study of Time Reduction in Manufacturing of Screws Used in Twin Screw PumpIJMERJOURNAL
Β
ABSTRACT: This paper gives the characteristics of Time reduction in manufacturing of screws for Twin screw pumps. Screws are playing a vital role in the performance of pumps, because pumps give the fluids transfer rate with the help of screws. There is a gap in screws which shows its positiveness. This indicates that we are studying about positive displacements pumps. Positive displacements pumps having no point of contact between screws, because of that there will be no any friction formation. Automation is best for development of product to reduce time in manufacturing of any product. In this paper we also tried to explain this feature of Automation to help reduction of time to manufacture of product to increase productivity.
Mihir's handbook of chemical process engineering (Excerpts)MIHIR PATEL, PMP(R)
Β
This book is aim toward all level of chemical engineers this will aid the them to carry out chemical process engineering in a very practical way. The process engineer can use the excel based calculation templates effectively to do correct and proper process design. Chemical engineering is a very vast and complex field. This book aims to simplify the process engineering design. Design of a chemical plant involves one being adept in technical aspects of process engineering. The book aims at making the chemical engineer proficient in the art of process design.
Included are chemical engineering basics on simulation, stoichiometry, fluid property calculation, dimensionless numbers, thermodynamics and on chemical engineering equipment like pump, compressor, steam turbine, gas turbine, flare, motor, fired heater, incinerator, heat exchanger, distillation column, fractionation column, absorber, stripper, packed column, solar evaporation pond, separator. Utility design of nitrogen, compressed air, water, effluent treatment, steam, condensate, desalination, fuel selection is covered.
Many chemical engineering calculations have been included. Special process items like flame arrestor, demister, feed device, pressure reducing and desuperheating station (PRDS), vortex breaker, electric heater, manual valve have been covered.
Process engineering design criteria, process control, material of construction, specialized process studies, safety studies, precommisioning and commissioning have been covered.
Project engineer will also benefit from information provided on types of project (EPC, EPCM, Cost + Fee, etc) as well as interdisciplinary interaction between various engineering disciplines i.e. process, piping, mechanical, instrumentation, electrical, civil and THSE.
Process engineering documentation like process design basis, process philosophies, process flow diagram (PFD), piping and instrumentation diagram (P&ID), block flow diagram (BFD), DP-DT diagram, material selection diagram (MSD), line list, summaries like utility summary, effluent and emission summary, tie in summary and flare relief load summary have been covered with blank templates. Excerpts from few chapters have been provided.
The present work is the numerical investigation of Spark Ignition (SI) engines to
assess the effect of spark plug positions using open source Computational Fluid Dynamics
(CFD) tool, OpenFoam is used. The standard kβΞ΅ turbulence model is used along with
the Reynolds Averaged Navier Stokes equations for simulating the flow field. Average
piston pressure is tracked for different Crank Angles (CA) from β180o to 180o for two
different sized engines (560cc and 70cc). Results clearly show that spark plug position
affects power output of engine. Spark plug position affect p-ΞΈ graph, hence performance
of engine, this effect is dominant in bigger engine than smaller one. Spark plug position
is expressed in dimensionless form in fraction away from centre
This document is a preface to the 16th edition of the Cameron Hydraulic Data book, published by Ingersoll-Rand as an engineering reference. It provides an overview of updates made to the new edition, including expanded data on liquid flow properties and metric conversions. A detailed index is included at the end to allow readers to quickly find relevant data. Engineers are advised to reference this index to locate information needed for pump selection and application work.
IRJET- Design and Analysis of Catalytic Converter of Automobile EngineIRJET Journal
Β
This document summarizes a study on the design and analysis of a catalytic converter for an automobile engine. The researchers designed a baseline catalytic converter model using CAD software and analyzed it using computational fluid dynamics (CFD) to study the pressure and velocity distribution. They found high pressure losses and non-uniform flow distribution. Various modifications to the honeycomb structure diameter, thickness, and position as well as the inlet and outlet design were tested. The optimal design was found to have a centered inlet, conical inlets/outlets, and a honeycomb structure with 30mm holes positioned at the casing mid-length. This design showed improved uniform flow distribution and reduced pressure losses compared to the baseline design.
International Journal of Engineering Research and Applications (IJERA) is an open access online peer reviewed international journal that publishes research and review articles in the fields of Computer Science, Neural Networks, Electrical Engineering, Software Engineering, Information Technology, Mechanical Engineering, Chemical Engineering, Plastic Engineering, Food Technology, Textile Engineering, Nano Technology & science, Power Electronics, Electronics & Communication Engineering, Computational mathematics, Image processing, Civil Engineering, Structural Engineering, Environmental Engineering, VLSI Testing & Low Power VLSI Design etc.
COMPUTATIONAL FLUID DYNAMIC ANALYSIS OF A PULSE JET ENGINEIRJET Journal
Β
1) The document describes a computational fluid dynamics (CFD) analysis of different designs of a pulse jet engine, specifically investigating the impact of increasing the number of fuel inlets.
2) CFD simulations were conducted using ANSYS CFX software on CAD models created in Creo, including designs with single, three, and five fuel inlets.
3) The results show that designs with more fuel inlets generated higher thrust, pressure, and enthalpy compared to the single inlet design, with the five inlet design performing best.
IRJET- Design and Analysis of Multi Port Fuel Injection CNG Engine Manifo...IRJET Journal
Β
This document describes the design and analysis of a multi-port fuel injection compressed natural gas (CNG) engine intake manifold system. The authors designed the manifold using pressure wave tuning theory to determine the optimal runner lengths. Computational fluid dynamics analysis was performed to evaluate the uniformity of the air-fuel mixture distribution and velocity profiles within the manifold. One-dimensional engine simulations were conducted to compare the performance of the new multi-port fuel injection system to the existing single-port system, finding that the multi-port system provided slightly higher power, torque, and volumetric efficiency.
This document summarizes a paper about flumping, a combination of flowing and pumping where a pumped well also flows from the casing-tubing annulus. The paper presents a methodology to calculate the bottom pressure and gas-oil ratio conditions needed to achieve flumping. It applies the methodology to example well data, presenting production rates and efficiencies for different bottom pressures. The results show that flumping can optimize production by allowing simultaneous pumping and annular flow.
The document discusses inlet distortion testing of the PW308 high-bypass turbofan engine. It tested the engine's response to 180-degree and 90-degree inlet total pressure distortion patterns. The testing showed the engine could operate with up to 6% circumferential distortion. A computational model was able to predict the engine's stability limit under distortion conditions within acceptable error margins, though it had more difficulty modeling the radial distortion of the 90-degree pattern. The results indicate the PW308 engine can operate in aircraft with embedded inlets.
1. APPLICATIONS OF VISCOUS OIL IN A
ROD SUCKER PUMP SYSTEM
By
Utkarsh Bhargava
Submitted in Partial Fulfillment of the Requirements for the
Master of Petroleum Engineering
New Mexico Institute of Mining and Technology
Department of Petroleum Engineering
Socorro, New Mexico
November 9th
, 2015
2. ABSTRACT
When producing a well for some amount of time, there always comes a moment when there
is not enough natural energy in the reservoir for oil to rise to the surface. The pressure
decreases significantly over time which will, in turn, decrease production. Artificial lift is
a process used in production engineering on oil and gas wells that can solve these problems
through a variety of pumps and lifts by reducing the bottomhole pressure and thereby
increasing the production rate of the well. This stimulation is necessary for about 95% of
all oil and gas wells, of which the majority being sucker-rod pumps; beam pumping is the
most common artificial lift method used in the industry. There are many aspects of a sucker
rod pump that must be designed very carefully to not only avoid failure, but to also ensure
safety of the operators. The API-RP 11L procedure is a trial and error method based on
correlations of research test data which, in summary, helps the designer to calculate the
important parameters of a pumping unit. These include polished rod loads, torque,
horsepower, etc. based on the preliminary selection of components through a series of
steps. However, there is a limitation of the API-RP 11L procedure; it does not take into
account the viscosity of the oil when predicting pump displacement and associated loads.
In this work, a computer simulator was developed according to the API-RP 11L procedure
to predict the important output parameters of a pumping unit. Many of the operating
characteristics used to calculate these output parameters are found in tables and figures,
but in order to implement them into a program, these plots had to be digitized. The effect
of heavy oil also was investigated by introducing an original equation for the frictional
pressure losses gradient. This equation was used in order to predict the magnitude of
increase of the peak polished rod load (PPRL), minimum polished rod load (MPRL) and
peak torque (PT). Studies were also done to see the effect the length of the rod and viscosity
has on the rod loads and torque, respectively. Efficiency was also incorporated in this study,
as the effect of the inertial forces and dynamic fluid loads were seen when studying the
relationship between both polished rod loads and polished rod horsepower and efficiency.
Based on the simulator results and sensitivity analysis, the API-RP 11L procedure is an
effective tool to predict pump displacement, polished rod loads, torque requirements, and
horsepower within certain bounds of some parameters of inviscid fluids. From the results
of the simulator and the equation developed, it has been determined that heavy oil has a
major effect on rod loads and torque on a sucker rod pumping unit. For example, oil with
a viscosity of 6000 centipoise can add almost 3500 psi onto the polished rod loads that a
sucker rod pump can handle and about 130000 in-lbf of torque. Viscosity effect
comparisons between three of the most common pumping units: conventional, air balanced,
and Mark II are also found in this work. The incorporation of efficiency and its relationship
with the polished rod loads and polished rod horsepower (PRHP) is also quite a significant
finding: with an increase in the efficiency, a decrease in the PPRL and PRHP are seen,
while an increase in the MPRL is observed.
Keywords: Artificial Lift Methods, Sucker Rod Pump, API-RP 11L procedure, heavy oil
applications
3. ii
ACKNOWLEDGEMENTS
I would like to express my sincere appreciation to my committee members: Dr. Her-Yuan
Chen, Dr. Guoyin Zhang, and my primary research advisor, Dr. Tan Nguyen, for providing
me the opportunity to embark on this project.
I would also like to thank all the staff, students and faculty of the Petroleum Engineering
department of New Mexico Institute of Mining and Technology, particularly Dr. Thomas
Engler and Mrs. Karen Balch.
To my family and friends in the United States and in India, thank you all for your
unyielding love and support. God bless you all.
Your assistance and support has been invaluable throughout the duration of my graduate
studies.
4. iii
TABLE OF CONTENTS
LIST OF TABLES............................................................................................................. iv
LIST OF FIGURES .............................................................................................................v
LIST OF ABBREVIATIONS AND SYMBOLS ............................................................. vii
1. INTRODUCTION .........................................................................................................1
2. LITERATURE REVIEW ..............................................................................................3
2.1. API-RP 11L Procedure .........................................................................................3
2.2. Pumping Units Summary......................................................................................6
2.2.1. Conventional Units ......................................................................................6
2.2.2. Air Balanced Units.......................................................................................7
2.2.3. Mark II Units................................................................................................8
2.3. Efficiency vs. Viscosity ........................................................................................9
2.4. Sucker Rod Pump for Viscous Oil......................................................................10
2.5. Annular Flow Frictional Pressure Drop..............................................................11
3. OBJECTIVE ................................................................................................................12
4. DIGITIZATION OF API-RP 11L PLOTS..................................................................13
5. FRICTIONAL PRESSURE LOSSES GRADIENT DEVELOPMENT......................20
6. RESULTS AND DISCUSSIONS................................................................................26
6.1. Results.................................................................................................................26
6.1.1. Polished Rod Load Results........................................................................29
6.1.2. Peak Torque Results ..................................................................................36
6.1.3. Efficiency Results......................................................................................42
6.2. Discussions .........................................................................................................44
7. CONCLUDING REMARKS.......................................................................................47
8. FUTURE WORK.........................................................................................................48
9. REFERENCES ............................................................................................................49
10. APPENDIX..................................................................................................................51
5. iv
LIST OF TABLES
Table 1: Equations for Output Parameters in API-RP 11L: Conventional Unitsβ¦β¦β¦β¦.13
6. v
LIST OF FIGURES
Figure 1: Dimensionless Plunger Stroke Factor API-RP 11L plot (Takacs, 2015)β¦β¦...β¦4
Figure 2: Dimensionless PPRL API-RP 11L plot (Takacs, 2015)β¦β¦β¦β¦β¦.................β¦4
Figure 3: Dimensionless MPRL API-RP 11L plot (Takacs, 2015)β¦β¦β¦β¦β¦β¦β¦...β¦β¦5
Figure 4: Dimensionless Peak Torque API-RP 11L plot (Takacs, 2015)β¦β¦............β¦β¦..5
Figure 5: Dimensionless PRHP API-RP 11L plot (Takacs, 2015)β¦β¦β¦.β¦β¦.β¦β¦β¦β¦..6
Figure 6: Conventional & Reverse Mark Pumping Units Photo (Lufkin, 2013)β¦β¦β¦β¦...7
Figure 7: Air Balanced Pumping Units Photo (Lufkin, 2013)β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦...8
Figure 8: Mark II Pumping Units Photo (Lufkin, 2013)β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦..9
Figure 9: Relationship between pump efficiency and viscosity (Herzog, 2005)β¦β¦β¦β¦.9
Figure 10: API-RP 11L Dimensionless Plunger Stroke Plot (Takacs, 2015)β¦...β¦β¦β¦...14
Figure 11: Digitization of Dimensionless Plunger Stroke Plotβ¦β¦β¦β¦β¦β¦β¦.β¦β¦β¦..14
Figure 12: API-RP 11L Dimensionless PPRL Plot (Takacs, 2015)β¦...β¦β¦..β¦..β¦β¦β¦.15
Figure 13: Digitization of Dimensionless PPRL Plotβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦.β¦β¦β¦15
Figure 14: API-RP 11L Dimensionless MPRL Plot (Takacs, 2015)β¦β¦β¦β¦β¦.β¦β¦..β¦16
Figure 15: Digitization of Dimensionless MPRL Plotβ¦β¦β¦β¦β¦β¦β¦β¦..β¦β¦β¦β¦β¦..16
Figure 16: API-RP 11L Dimensionless PT Plot (Takacs, 2015)β¦...β¦β¦β¦..β¦β¦β¦β¦....17
Figure 17: Digitization of Dimensionless PT Plotβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦.β¦β¦β¦β¦.17
Figure 18: API-RP 11L Dimensionless PRHP Plot (Takacs, 2015)β¦β¦β¦β¦β¦β¦.β¦β¦...18
Figure 19: Digitization of Dimensionless PRHP Plotβ¦β¦β¦β¦..β¦β¦β¦...β¦β¦β¦β¦β¦β¦18
Figure 20: Diagram for Rod Movement in Tubular (Li, 2012)β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦....20
Figure 21: PPRL: SPE 20152 vs Simulator Comparisonsβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦...β¦26
Figure 22: MPRL: SPE 20152 vs Simulator Comparisonsβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦.27
Figure 23: PT: SPE 20152 vs Simulator Comparisonsβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦27
Figure 24: PPHP: SPE 20152 vs Simulator Comparisonsβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦...28
Figure 25: CBE: SPE 20152 vs Simulator Comparisonsβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦28
Figure 26: Conventional Units: Viscosity Effect on Polished Rod Loads at 5000 ft...β¦β¦29
Figure 27: Comparison of the PPRL of the Three Units at 5000 ftβ¦β¦β¦β¦β¦β¦β¦β¦β¦..30
Figure 28: Comparison of the MPRL of the Three Units at 5000 ftβ¦β¦β¦β¦β¦β¦β¦β¦β¦.30
Figure 29: Conventional Units: Effect of Viscosity and Length on PPRLβ¦β¦β¦β¦..β¦β¦31
Figure 30: Conventional Units: Effect of Viscosity and Length on MPRLβ¦β¦β¦β¦.β¦β¦32
Figure 31: Conventional Units: % Increase of PPRL at 5000 ft due to Viscosityβ¦β¦β¦β¦33
Figure 32: Conventional Units: % Increase of MPRL at 5000 ft due to Viscosityβ¦...β¦β¦33
Figure 33: Comparisons of PPRL % Increase of the Three Units at 5000 ftβ¦β¦β¦β¦β¦β¦34
Figure 34: Comparisons of MPRL % Increase of the Three Units at 5000 ft...β¦β¦β¦β¦β¦35
Figure 35: Conventional Units: Effect of Viscosity on PT (Upstroke / Downstroke)β¦β¦.36
Figure 36: Air Balanced Units: Effect of Viscosity on PT (Upstroke / Downstroke)..β¦β¦37
Figure 37: Mark II Units: Effect of Viscosity on PT (Upstroke / Downstroke)β¦β¦...β¦β¦38
Figure 38: Comparisons of Peak Torque Upstroke of the Three Units at 5000 ftβ¦..β¦..β¦39
Figure 39: Comparisons of Peak Torque Downstroke of the Three Units at 5000 ftβ¦...β¦39
Figure 40: Conventional Units: Effect of Viscosity and Length on Peak Torqueβ¦β¦β¦β¦40
Figure 41: Conventional Units: % Increase of Peak Torque at 5000 ft due to Viscosity.β¦41
Figure 42: Conventional Units: Effect of Efficiency and Viscosity on PPRLβ¦..β¦β¦...β¦42
7. vi
Figure 43: Conventional Units: Effect of Efficiency and Viscosity on MPRLβ¦.β¦β¦...β¦43
Figure 44: Polished Rod Horsepower (HP) vs Efficiencyβ¦β¦β¦β¦β¦β¦β¦β¦β¦β¦β¦...β¦44
Figure 45: Air Balanced Units: Viscosity Effect on Polished Rod Loads at 5000 ftβ¦β¦β¦51
Figure 46: Mark II Units: Viscosity Effect on Polished Rod Loads at 5000 ftβ¦β¦β¦β¦β¦.51
Figure 47: Air Balanced Units: Effect of Viscosity and Length on PPRL...β¦β¦β¦β¦β¦β¦52
Figure 48: Air Balanced Units: Effect of Viscosity and Length on MPRL.β¦β¦β¦β¦β¦β¦52
Figure 49: Air Balanced Units: % Increase of PPRL at 5000 ft due to Viscosity.β¦β¦β¦β¦53
Figure 50: Air Balanced Units: % Increase of MPRL at 5000 ft due to Viscosity...β¦β¦β¦53
Figure 51: Mark II Units: Effect of Viscosity and Length on PPRLβ¦β¦β¦β¦β¦β¦β¦β¦β¦54
Figure 52: Mark II Units: Effect of Viscosity and Length on MPRLβ¦β¦..β¦β¦β¦β¦β¦β¦54
Figure 53: Mark II Units: % Increase of PPRL at 5000 ft due to Viscosity β¦β¦β¦β¦β¦β¦55
Figure 54: Mark II Units: % Increase of MPRL at 5000 ft due to Viscosityβ¦β¦β¦β¦β¦β¦55
Figure 55: Conventional Units: Effect of Viscosity and Length on PT (Upstroke)β¦β¦.β¦56
Figure 56: Conventional Units: Effect of Viscosity and Length on PT (Downstroke)β¦β¦56
Figure 57: Air Balanced Units: Effect of Viscosity and Length on PT (Upstroke)β¦..β¦β¦57
Figure 58: Air Balanced Units: Effect of Viscosity and Length on PT (Downstroke)β¦.β¦57
Figure 59: Mark II Units: Effect of Viscosity and Length on PT (Upstroke)β¦...β¦β¦β¦β¦58
Figure 60: Mark II Units: Effect of Viscosity and Length on PT (Downstroke)β¦..β¦β¦β¦58
Figure 61: Air Balanced Units: Effect of Viscosity and Length on PTβ¦β¦β¦β¦β¦β¦β¦β¦59
Figure 62: Air Balanced Units: % Increase of Peak Torque at 5000 ft due to Viscosity..β¦59
Figure 63: Mark II Units: Effect of Viscosity and Length on Peak Torque.β¦β¦β¦β¦β¦β¦60
Figure 64: Mark II Units: % Increase of Peak Torque at 5000 ft due to Viscosity...β¦β¦β¦60
Figure 65: Air Balanced Units: Effect of Efficiency and Viscosity on PPRLβ¦.....β¦β¦β¦61
Figure 66: Air Balanced Units: Effect of Efficiency and Viscosity on MPRL...β¦β¦β¦.β¦61
Figure 67: Mark II Units: Effect of Efficiency and Viscosity on PPRLβ¦β¦β¦......β¦β¦β¦62
Figure 68: Mark II Units: Effect of Efficiency and Viscosity on MPRLβ¦β¦β¦.....β¦β¦β¦62
8. vii
LIST OF ABBREVIATIONS AND SYMBOLS
psi Pounds per square inch (unit of pressure)
In-lbf Inch-pound force (unit of torque)
cp Centipoise (unit of viscosity)
PPRL Peak Polished Rod Load
MPRL Minimum Polished Rod Load
PT Peak Torque (in-lbf)
PRHP Polished Rod Horsepower (HP)
CBE Counterbalance Effect (lbf)
PD Pump Displacement
N Pumping Speed (spm β strokes per minute)
S Surface Stroke Length (in)
Sp Plunger Stroke Length (in)
kr Spring constant of the rod string
Fo/Skr Dimensionless Rod Stretch
N/No Dimensionless Pump Speed
N/Nβo Dimensionless Pump Speed (with rod-tapering)
ππ Efficiency
API American Petroleum Institute
ππ Shear Stress
ππ Viscosity
Ξ³ Shear Rate
r1 Inner Radius (Rod)
r2 Outer Radius (Rod to Wall)
u, v Velocity
ur Velocity of Rod
π’π’οΏ½ Average Flow Velocity
Q Flow Rate
dPf / dL Frictional Pressure Drop
9. This thesis is accepted on behalf of the
Faculty of the Institute by the following committee:
Tan Nguyen
Advisor
Her Yuan Chen
Committee Member
Guoyin Zhang
Committee Member
11/9/15
Date
I release this document to the New Mexico Institute of Mining and Technology.
Utkarsh Bhargava 11/9/15
Studentβs Signature Date
10. 1
CHAPTER 1
INTRODUCTION
Artificial lift assists in the downhole process of extracting oil by decreasing the bottomhole
pressure in the reservoir. These various methods are very important techniques in the
industry and must be used in the majority pressure deficient wells. Without the presence of
artificial lift, it would be impossible to meet current demands. As mentioned before, this
stimulation is necessary for about 95% of all oil/gas wells (Hyne, 2012). Sucker-rod lifting,
or beam pumping, is the most common artificial lift method used in the industry. About
750,000 out of the 2 million oil wells around the world use sucker rod pumps as their choice
of artificial method. In the United States alone, sucker rod pumps account for about
350,000 wells which also takes into account the 80% of all US oil wells that produce a
maximum of 10 barrels per day (Lea, 2014). Because these pumping systems occupy lots
of space and are very heavy, they are primarily found on onshore locations.
There are many different parts of a sucker rod pumping system, which include the surface
equipment (prime mover, gear reducer and pumping unit) and the downhole equipment
(sucker rod string and subsurface pump). The prime mover simply supplies power to the
system; these are most often internal combustion engines, but can also be electric motors.
The gear reducer stabilizes the speed and torque of the pump. The power supplied by the
prime mover is generally very high speed and low torque, while the pumping unit,
conversely, requires low speed and high torque (Kelly, 2000). The gear reducer is essential
in this alteration. The pumping unit reciprocates the motion of the prime mover and gear
reducer. The latter two exhibit rotational behavior, while the pumping unit establishes a
vertical motion. The pumping unit also includes the counterweight (for conventional and
Mark II units) or the compressed air assembly (for air balanced units) which evenly
distribute the weight of the rod string. The pumping unit on the surface is connected to the
subsurface pump via a sucker rod string, which also enables the subsurface pump to have
a vertical motion from its usual rotational motion. A pump jack is also vital as it is
connected to the downhole pump at the bottom of the well by many interconnected sucker
rods. Sucker rods maintain about 25-30 feet in length with several choices in diameter
ranging from Β½ inch to 1 β inch; these are joined together via couplings.
Before detailing how the system works, it should be noted that sucker rod pumps work by
positive displacement of the fluid and not by centrifugal force. First, as stated earlier, the
prime mover supplies power to the gear reducer; the gear reducer not only reduces the
angular velocity, but increases the relative torque. The crank turns counterclockwise and
lifts the counterweight, which, in turn pivots the beam and submerges the plunger, which
signifies the beginning of the downstroke stage and the end of the upstroke stage. For a
closer examination of the pump cycle, these two stages are very important in the
functioning of the pump. There are two valves needed: the standing valve and traveling
valve. These are located at the bottom of the tubing and at the bottom of the sucker rods,
respectively. Fluid flow dictates the opening and closing of these valves. The downstroke
11. 2
stage is marked by the opening of the traveling valve and the closing of the standing valve.
This means no fluid can leave the well, and only flow into the plunger. The standing valve
must be closed as there is fluid being carried above it and the fluid is moving upward
towards the traveling valve, which is open. Conversely, the upstroke stage is discernable
by the traveling valve closing and the standing valve opening. In this stage, while more
fluid is pumped into well, fluid not only in the plunger, but also above it is lifted out of the
casing. This cycle repeats itself when the top of the stroke is reached by the plunger, as the
downstroke process happens again where the traveling valve opens and standing valve
closes. These two valves work together to move the fluid up the tubing toward the surface
in what is known as the pump cycle.
This process works quite well for inviscid fluids or low viscosity fluids, however, there are
challenges that lead to pumping oil of heavier crudes. Heavy oil is characterized by very
low API grades (10Μ to 22.3Μ), low hydrogen to carbon ratios, and high specific gravities.
They also contain large amounts of asphaltic content along with sulfur, nitrogen and other
heavy metals (Halliburton, 2009). Along with having very little to no flowability due to
their high viscosity, heavy oil is also quite difficult and costly to produce. The viscosity of
these crudes range from a couple hundred centipoise to 10,000 cp. Most heavy oils are also
found in poorly consolidated sands (Halliburton, 2009), which present many challenges in
themselves. The reservoirs that contain heavy oil influence both cementing and the
wellbore integrity. Maintaining the pressure throughout the system, controlling the heat
transfer, and having a means of effective sand control becomes infinitely more important
in the production of such reservoirs.
It is difficult to recover these oils in their natural state through ordinary production
methods; increasing the temperature (adding heat) or dilution may be required for the oil
to flow through the pipeline. However, this work focuses on the conventional method of
extraction in determining the viability that a regular sucker rod pumping system has for
producing heavy oil.
12. 3
CHAPTER 2
LITERATURE REVIEW
2.1 API-RP 11L Procedure
The API-RP 11L procedure is a trial and error method based upon many correlations of
research test data. It contains three steps: the preliminary selection of components,
calculating the operating characteristics with formulas, tables and figures, and lastly,
finding the pump displacement and associated loads from those characteristics. To proceed
with the API-RP 11L procedure and calculate all of the output parameters, a minimum
amount of information must be known. This information is based on the preliminary
components chosen: pump depth, fluid level, pumping speed, surface stroke length,
specific gravity, pump plunger diameter, the nominal tubing diameter, and the design and
size of the sucker rod. The API-RP 11L procedure adopted and expanded upon work
conducted by the Midwest Research Institute in 1964 that ran numerous computer
simulations over many different operating conditions (Takacs, 2015). The work conducted
is a function of two dimensionless variables: pump speed and rod stretch. The
dimensionless pump speed quantity may be expressed as N/No or N/Nβo. N/No is defined
as the pump speed in strokes per minute (N) divided by (No), the natural frequency of the
string, while N/Nβo is simply (N/No)/Fc, where Fc is a frequency factor of the rod string;
this is based off the rod API grade and plunger diameter. The dimensionless rod stretch is
noted as Fo/Skr; this is defined as the weight of the fluid imposed on the rods divided by
the product of the polished rod stroke length and the spring constant of the rod string. After
these dimensionless qualities are calculated, then the dimensionless variables to help
calculate the associated loads and stresses can be calculated. These include the plunger
stroke, the pump displacement, the peak and minimum polished rod loads, the polished rod
horsepower, the peak torque, and the counterbalance effect. This is normally done with
plots and figures, however, these plots have been digitized and equations have been
generated for the most important parameters when simulating a pumping system.
API-RP 11L plots: With the calculation of both the dimensionless rod stretch and
dimensionless pump speed, the following plots enable the operator to calculate the
dimensionless groups that will allow the final calculation for the output pumping
parameters. For example, in Fig. 1, with a dimensionless pump speed of 0.274 and rod
stretch of 0.13, the plot can be used to find the (Sp/S) value of 0.98.
15. 6
Figure 5: Dimensionless PRHP API-RP 11L plot (Takacs, 2015)
2.2 Pumping Units Summary
The three most common sucker rod pumping units are conventional, air balanced, and Mark
II units. A summary of the geometry of these pumping units are described in order to help
explain some of the results below.
2.2.1 Conventional Units
Conventional units are the most common in the industry and the simplest to operate; they
are require the least amount of maintenance and are the standard for all operating pumping
units. These systems allow for the widest range of sizes that are available and are the
cheapest in terms of operating costs than the other pumping units. Conventional units and
Mark II units both employ counterweights in order to balance the load of the fluid and rod
with the surface equipment, however, the air balanced units use compressed air instead of
counterweights.
16. 7
Figure 6: Conventional & Reverse Mark Pumping Units Photo (Lufkin, 2013)
2.2.2 Air Balanced Units
The use of compressed air as opposed to the counterweights allows for more control of the
counterbalance, as adjustments can be made without having to stop the system. This is
beneficial as these systems generally are of lower weight than the conventional systems,
and thus more portable, allowing their use offshore.
17. 8
Figure 7: Air Balanced Pumping Units Photo (Lufkin, 2013)
2.2.3 Mark II Units
The Mark II units have a very unique geometry; it uses a lever system that is design to
decrease upstroke acceleration and decrease the peak rod load (Lufkin, 2013). This unique
geometry also is designed to produce a slower upstroke and faster downstroke, which
decreases the torque on the gear reducer up to 35%. Common in both the air balanced and
Mark II units, as opposed to the conventional units, is the difference in the position of the
gear reducer. The gear reducer in the air balanced and Mark II units is located underneath
the equalizer and away from the Samson post. In the two former units, the gear reducer is
moved towards the Samson posts turning in the preferred direction of rotation. This
geometry creates an upstroke that occurs in the crank rotation of 195Β° and a downstroke of
165Β°. This change of geometry from the usual 180Β° reduces the acceleration at the
beginning of the upstroke where the load is the greatest, which results in the decrease of
the polished rod load. This shift in the gear reducer also creates a scenario that decreases
the maximum torque factor on the upstroke and increases the maximum downstroke torque
factor. A greater mechanical advantage is created for lifting the heavy load on the upstroke
and a lower mechanical advantage for the reduced load on the downstroke (Lufkin, 2013).
18. 9
Figure 8: Mark II Pumping Units Photo (Lufkin, 2013)
2.3 Efficiency vs. Viscosity
Figure 9: Relationship between pump efficiency and viscosity (Herzog, 2005)
Fig. 9, from the Machinery Lubrication Publication, shows that as the viscosity increases,
there is an associated increase in the volumetric efficiency, however a decrease in the
mechanical efficiency. Volumetric efficiency refers to the comparison of the actual fluid
flow out of a pump and the flow based on internal leakage and flow losses. The mechanical
efficiency deals with the frictional losses and energy required to overcome the drag force
and have constant flow (Rudnick, 2013). These parameters are both heavily influenced by
19. 10
viscosity changes. High viscosity fluids lead to higher flow resistances, which leads to a
decrease the mechanical efficiency, however increase in viscosity leads to an increase in
the volumetric efficiency as the slip decreases and there is also less leakage with viscous
oils than lighter oils. As can also be seen from Fig. 9, there is a range of the viscosity that
optimizes both efficiencies along with the overall efficiency. The overall efficiency is
defined as the product of the mechanical and volumetric efficiencies.
2.4 Sucker Rod Pump for Viscous Oil
Viscous oil is pumped quite frequently in many parts of the world, not only with
progressive cavity pumps, but also with sucker rod pumps. The study conducted in SPE
2152 (Juch, 1969), took place in Venezuela, as most of the crude oil pumped in Venezuela
is very viscous with 9Μ to 16Μ API gravities and with viscosities that are as high as 10,000
cp. Because of this, there is a growing need to improve the pump efficiencies when dealing
with a viscous reservoir. A new line of sucker rod pumps were introduced as a result. The
new technology of streamlined pumps have improved the production performance of
viscous crude wells in Venezuela (Juch, 1969).
Two very important problems arise when dealing with pumping viscous oil. With viscous
oils, there is more of a resistance to flow which causes severe pressure variance over time.
This can be damaging to the pump performance due to huge energy losses as well as gas
leaks, not to mention the pump and equipment wear. Also, issues are seen in the upstroke
and downstroke phases of the pump. The valve positions that allow for fluid flow are
delayed depending on the API gravity, which affects not only the pump efficiency, but also
the pump performance (Juch, 1969).
However, there are techniques that aid in pump design that enable pumping of viscous oils.
One such method involves the use of a friction ring hold-down mechanism. This involves
the use of Monel plungers, as regular plungers are not very efficient in high viscous and
corrosive wells. Monel plungers are much sturdier and made from corrosion resistant
materials (Black, 2015), which help to get a higher hold-down force than with regular
plungers. Monel plungers also enable higher flow capacity with a higher hold-down force.
Another method involves the use of ring valves; they reside in rod guides and sit in the rim
of the tube connector (Juch, 1969). The installation of a ring valve enables the traveling
valve to open earlier on the downstroke, which not only addresses the problem of the valve
actions to be delayed for viscous oil, but also allow for the downstroke stage to occur
without any problems. Conversely, the standing valves also open earlier on the upstroke,
which causes a major decrease in the pressure differential across the standing valve on the
downstroke. This decrease in pressure drop greatly improves the volumetric efficiency
(Juch, 1969). Also, the use of a ring valve allows for loads during the pump cycle (PPRL,
MPRL, etc.) to occur in a more gradual fashion and improve the load distribution.
20. 11
2.5 Annular Flow Frictional Pressure Drop
The annular flow frictional pressure drop equation for Newtonian fluids is:
ππππππ
ππππ
=
8πππ’π’οΏ½
οΏ½ππ2
2+ππ1
2β
ππ2
2βππ1
2
ln
ππ2
ππ1
οΏ½
(1)
It can be seen that Eq. (1) is quite similar to the equation derived (Eq. 38), in chapter 5,
with the only difference being the incorporation of the velocity of the rod. The boundary
conditions in order to find the two constants for Eq. (1) were different, being:
B.C. 1: r = r1 ο u = 0
B.C. 2: r = r2 ο u = 0
These two boundary conditions imply the velocity will equal 0 at both r1 and r2, which
removes the velocity of the rod and solely bases the frictional pressure drop on the average
flow velocity and the viscosity.
21. 12
CHAPTER 3
OBJECTIVE
The goal of this work is threefold.
First, all of the plots in the API-RP 11L procedure were digitized in order to get a single
equation for each output parameter solely based on the dimensionless rod stretch and
dimensionless pump speed.
Secondly, these equations along with others from the API-RP 11L procedure were coded
into a simulator using Microsoft Excel VBA. This is the working simulator that is used to
calculate the output parameters, such as polished rod loads, torque, horsepower etc., for
any and all inputs that the user enters.
Lastly, the effect of viscosity was studied. Because the API-RP 11L procedure is limited
to inviscid flow, there are no heavy oil applications associated with it. A new equation for
the frictional pressure losses gradient was developed and was used in conjunction with
the output parameters from the simulator to further study the effect viscosity has on pump
characteristics and the magnitude to which they are affected.
22. 13
CHAPTER 4
DIGITIZATION OF API-RP 11L PLOTS
Digitization is defined as the process of extracting numerical data values from graphs in
scientific publications (Rohatgi, 2015). In the case of the API-RP 11L procedure, to
calculate output parameters without the use of plots and instead with equations, the plots
had to be digitized. These plots were recreated and manipulated in Excel using the solver
macro add-in; the distance between the differences of the squares of the two plots was
minimized to get the best results possible. To get accurate results, a 10% error had to be
used or else the solver could not complete the iteration process. The plots found in literature
to calculate the dimensionless groups also needed to be manipulated and an equation was
generated for each of them found. As it can be seen, the plots only allow for a certain bound
in these two dimensionless groups, in some cases, (0 - 0.6) for the pump speed and (0.1 -
0.5) for the rod stretch, while an equation would allow for the calculation outside of these
parameters. The equations for the various output parameters are below and each of these
includes a dimensionless group that can be calculated using the equation generated based
on the digitization of each plot in literature.
Table 1: Equations for Output Parameters in API-RP 11L: Conventional Units
It can be seen from Table 1 that to calculate the PPRL, the dimensionless group of F1/Skr
needs to be calculated. The effective weight of the rods in fluid is simply based on the
weight of the rods in air and specific gravity of the fluid. This is also seen for the
dimensionless group F2/Skr to calculate the MPRL, Sp/S (Ideal and Actual Pump
Displacement), 2T/S2
kr (Peak Torque) and F3/Skr (PRHP). All of these dimensionless
groups can be found using the equations that were generated based on the digitization of
the plots found in literature. The digitization results involve the specific equation generated
for each output parameter dependent upon the dimensionless pump speed (N/No or N/Nβo)
and rod stretch (Fo/Skr), as explained in the literature review section. These are seen below:
23. 14
Figure 10: API-RP 11L Dimensionless Figure 11: Digitization of Dimensionless
Plunger Stroke Plot (Takacs, 2015) Plunger Stroke Plot
Eq. (2) generated for the plunger stroke divided by the surface stroke in terms of
dimensionless pumping speed and dimensionless rod stretch is:
ππππ
ππ
= β288.464 οΏ½
ππ
ππππ
β² οΏ½
6
+ 464.4255 οΏ½
ππ
ππππ
β² οΏ½
5
β 285.941 οΏ½
ππ
ππππ
β² οΏ½
4
+ 88.94985 οΏ½
ππ
ππππ
β² οΏ½
3
β
13.189 οΏ½
ππ
ππππ
β² οΏ½
2
+ 1.124451 οΏ½
ππ
ππππ
β² οΏ½ + 5.554806 οΏ½
πΉπΉππ
ππππππ
οΏ½
4
β 7.0981 οΏ½
πΉπΉππ
ππππππ
οΏ½
3
+ 3.325249 οΏ½
πΉπΉππ
ππππππ
οΏ½
2
β
1.54031 οΏ½
πΉπΉππ
ππππππ
οΏ½ + 0.994469 (2)
Eq. (2) along with the rest have been generated in dimensionless pump speed to the 6th
degree polynomial and dimensionless rod stretch to the 4th
degree in order to get the most
accurate results possible. These equations were also generated in order to exceed the
bounds of these plots. Fig. 10 is only valid for the range of the dimensionless pump speed
from 0 to 0.6 and the dimensionless rod stretch from 0.05 to 0.5. Eqs. (1-6) using the solver
macro add-in allow for the calculation at ranges outside of these limits, if desired. As it can
be seen, while the digitization and solver coefficient finder was done to the best of its
ability, there is a degree of uncertainty at N/Nβo = 0.2 to N/Nβo = 0.35 at all of the
dimensionless rod stretch values with about a 5% error, however the model was optimized
at all other ranges.
24. 15
Figure 12: API-RP 11L Dimensionless Figure 13: Digitization of Dimensionless
PPRL plot (Takacs, 2015) PPRL plot
Eq. (3) generated for the peak polished rod load dimensionless group (F1/Skr) in terms of
dimensionless pumping speed and dimensionless rod stretch is:
πΉπΉ1
ππππππ
= β187.783 οΏ½
ππ
ππππ
οΏ½
6
+ 341.1534 οΏ½
ππ
ππππ
οΏ½
5
β 210.786 οΏ½
ππ
ππππ
οΏ½
4
+ 55.62392 οΏ½
ππ
ππππ
οΏ½
3
β
5.58467 οΏ½
ππ
ππππ
οΏ½
2
+ .748049 οΏ½
ππ
ππππ
οΏ½ + 1.252434 οΏ½
πΉπΉππ
ππππππ
οΏ½
4
β .39606 οΏ½
πΉπΉππ
ππππππ
οΏ½
3
β .90549 οΏ½
πΉπΉππ
ππππππ
οΏ½
2
+
1.225137 οΏ½
πΉπΉππ
ππππππ
οΏ½ β 0.13983 (3)
The digitization for the peak polished rod load, as can be seen from Fig. 12, turned out
quite well in reference to the plot in literature on the left. The only slight outliers may
potentially occur with very small Fo/Skr values and high N/No values. However, for all
other values of both rod stretch and pump speed the results are deemed quite strong.
26. 17
The digitization for the minimum polished rod load also, similarly to the peak polished
rod load, came out to be quite accurate compared with the plot found in literature, with all
of the predicted values being less than 5% from the actual values.
Figure 16: API-RP 11L Dimensionless Figure 17: Digitization of Dimensionless
PT plot (Takacs, 2015) PT plot
Eq. (5) generated for the peak torque dimensionless group (2ππ/ππ2
ππππ) in terms of
dimensionless pumping speed and dimensionless rod stretch is:
2ππ
ππ2 ππππ
= β74.9862 οΏ½
ππ
ππππ
β² οΏ½
6
+ 132.8622 οΏ½
ππ
ππππ
β² οΏ½
5
β 87.8538 οΏ½
ππ
ππππ
β² οΏ½
4
+ 27.16812 οΏ½
ππ
ππππ
β² οΏ½
3
β
3.52134 οΏ½
ππ
ππππ
β² οΏ½
2
+ .663331 οΏ½
ππ
ππππ
β² οΏ½ + 5.705248 οΏ½
πΉπΉππ
ππππππ
οΏ½
4
β 5.62858 οΏ½
πΉπΉππ
ππππππ
οΏ½
3
+ 1.028574 οΏ½
πΉπΉππ
ππππππ
οΏ½
2
+
.573612 οΏ½
πΉπΉππ
ππππππ
οΏ½ β 0.037408 (5)
The digitization for the peak torque dimensionless group presented quite a distinct
challenge. As can be seen from Fig. 16, the rod stretch value (Fo/Skr) at 0.5 varying the
dimensionless pump speed presents very odd behavior for the torque factor needed in order
to calculate the peak torque needed for the system. It was handled to the best of the solverβs
ability, while keeping in mind the other values, and along with the rest of the rod stretch
values gives accurate results anyhow.
28. 19
The digitization of the polished rod horsepower dimensionless group also presented a
similar challenge to the torque. However, in this case, the rod stretch values of 0.4 and 0.6
demonstrate equal behavior at low pump speeds, however deviate from each other at higher
pump speeds. This behavior, along with the other rod stretch groups, did not allow for
simply one equation to model their behavior, as the results compared to the actual API-RP
11L plot were quite inaccurate. A piecewise function was then attributed to the calculation
of the dimensionless group to calculate the polished rod horsepower to account for the
behavior at the 0.4 and 0.6 Fo/Skr groups.
29. 20
CHAPTER 5
FRICTIONAL PRESSURE LOSSES GRADIENT DEVELOPMENT
Figure 20: Diagram for Rod Movement in Tubular (Li, 2012)
The momentum eq. is applied for an incompressible fluid, a 1-D, isothermal, and steady
state system, while assuming no convection. Cylindrical coordinates were also used in the
derivation. The relationship between Ο and
ππππππ
ππππ
(the frictional pressure drop gradient) can
be written as:
ππ =
ππ
2
ππππππ
ππππ
+
ππ1
ππ
(8)
For Newtonian fluids:
ππ = ππππ = βππ
ππππ
ππππ
=
ππ
2
ππππππ
ππππ
+
ππ1
ππ
(9)
Dividing by the viscosity on both sides and multiplying by dr:
βππππ = οΏ½
ππ
2ππ
ππππππ
ππππ
+
ππ1
ππππ
οΏ½ ππππ (10)
Downstroke
Friction
Force
ππ1
ππ2
30. 21
Eq. (11) gives the general form of the velocity profile with c1 and c2 as the two integral
constants:
π£π£ = β
ππ2
4ππ
ππππππ
ππππ
β
ππ1
ππ
ln ππ + ππ2 (11)
To model the velocity profile, two boundary conditions are needed to find c1 and c2. During
the upstroke, there are two movements: the upward movement of the rod and the fluid flow
in the annulus between the rods and production casing. The boundary conditions can be
established based on Fig. 20. When r = r1, the velocity is taken as the velocity of the rod
and when r = r2, the velocity at the wall, is 0.
B.C. 1: r = r1 ο u = ur
B.C. 2: r = r2 ο u = 0
Solving these equations with the two boundary conditions and rearranging leads to the
velocity profile below:
π’π’(ππ) =
1
4ππ
ππππ
ππππ
οΏ½(ππ2
2
β ππ2) β (ππ2
2
β ππ1
2)
lnοΏ½
ππ2
ππ
οΏ½
lnοΏ½
ππ2
ππ1
οΏ½
οΏ½ + π’π’ππ (12)
The flow rate can be calculated as:
ππ = β« π’π’(ππ)2ππππ ππππ (13)
Plugging in the velocity profile, the equation can be rewritten as:
π’π’(ππ)2ππππ ππππ = οΏ½οΏ½
1
4ππ
ππππ
ππππ
(ππ2
2
β ππ2) + π’π’ππ β
1
4ππ
ππππ
ππππ
(ππ2
2
β ππ1
2)οΏ½
lnοΏ½
ππ2
ππ
οΏ½
lnοΏ½
ππ2
ππ1
οΏ½
οΏ½ 2ππππ ππππ (14)
ππ = β« οΏ½
1
4ππ
ππππ
ππππ
οΏ½(ππ2
2
β ππ2) β (ππ2
2
β ππ1
2)
lnοΏ½
ππ2
ππ
οΏ½
lnοΏ½
ππ2
ππ1
οΏ½
οΏ½ + π’π’πποΏ½ 2ππππ ππππ (15)
ππ = 2ππ β« οΏ½
1
4ππ
ππππ
ππππ
οΏ½(ππ2
2
β ππ2) β (ππ2
2
β ππ1
2)
lnοΏ½
ππ2
ππ
οΏ½
lnοΏ½
ππ2
ππ1
οΏ½
οΏ½ + π’π’πποΏ½ ππ ππππ
ππ2
ππ1
(16)
35. 26
CHAPTER 6
RESULTS AND DISCUSSIONS
6.1 Results
Following the digitization plots in Chapter 4, the viscosity effect plots are presented below.
As described in the literature review section, the API-RP 11L process works primarily for
inviscid or very low viscosity fluid. The digitized equations (Eqs. 1-6) in conjunction with
Eq. (38) were imbedded into the simulator to study the effect of fluid viscosity on the pump
design parameters such as PPRL, MPRL, and PT. The simulator also was used to study the
effect of efficiency on these parameters.
Before the viscosity results are shown, the accuracy of the simulator must be established
in order to validate the results. When comparing the results of the simulator to those in
literature, the results correlate quite well. This was found both with the SPE 20152 paper
(Jennings, 1989) and different presentations outlining examples of the API-RP 11L
procedure. When comparing the results of the simulator to SPE 20152, the main outliers
occur in the PT and the PPRL, with the computer simulator under-predicting these two
factors. However, the estimated MPRL, the CBE and the PRHP are quite close to those in
literature, being less than 5% off the actual values in the published paper. The differences
can be attributed to the digitization; the process using the solver technique is a good
estimation tool to try and fit the data, however, exact results were not seen. A graphical
comparison of the five important parameters (PPRL, MPRL, PT, PRHP, CBE) between
SPE 20152 and the simulator developed of all three units are shown:
Figure 21: PPRL: SPE 20152 vs Simulator Comparisons
36. 27
Figure 22: MPRL: SPE 20152 vs Simulator Comparisons
Figure 23: PT: SPE 20152 vs Simulator Comparisons
37. 28
Figure 24: PRHP: SPE 20152 vs Simulator Comparisons
Figure 25: CBE: SPE 20152 vs Simulator Comparisons
38. 29
6.1.1 Polished Rod Load Results
Figure 26: Conventional Units: Viscosity Effect on Polished Rod Loads at 5000 ft
Fig. 26 shows quantitatively how the fluid viscosity affects the PPRL and MPRL for a
conventional pumping unit. As the fluid viscosity increases, the friction between the fluids
and the rods as well as the fluid and production casing increase also. This leads to higher
polished rods. A 10.053% increase in the PPRL and a 21.961% increase in the MPRL are
observed when the fluid viscosity varies from 0 to 4000 cp. Due to the fact that some heavy
oils have viscosities as high as 10,000 cp, this increase is quite significant and must be
taken into account when designing a pumping unit. Similar plots to that of Fig. 26 can be
seen in the Appendix for air balanced and Mark II units.
10.053% increase
21.961% increase
39. 30
Figure 27: Comparison of the PPRL of the Three Units at 5000 ft
Figure 28: Comparison of the MPRL of the Three Units at 5000 ft
40. 31
The effect viscosity has on the polished rod loads at 5000 ft for both air balanced units and
Mark II units is similar to that seen in the conventional unit (Fig. 26), however with
different magnitudes. Figs. 27 and 28 show the magnitudes of the PPRL and MPRL of all
three pumping units. It can be seen from both of these plots that conventional units have
larger PPRL and MPRL than air balanced and Mark II units. The geometry of both of these
units as described in the literature review chapter help to explain why the polished rod
loads are lower than those of the conventional unit. The position of the gear reducer in both
of these systems allow for more degrees of the crank travel on the upstroke (180Β° to 195Β°),
and this decreases the loads. Also unique to the Mark II units is a lever system that is also
used to further decrease the upstroke acceleration and decrease the rod load (Lufkin, 2013).
Figure 29: Conventional Units: Effect of Viscosity and Length on PPRL
41. 32
Figure 30: Conventional Units: Effect of Viscosity and Length on MPRL
The results from Figs. 26-28 are simply shown for a rod that is 5000 ft in length for all
three pumping units. In Figs. 29 and 30, the length of the rod is varied in the simulator
developed along with the viscosity from 0 to 6000 cp for the conventional unit to see the
effect both of these factors have on the PPRL and MPRL. As the length of the rod increases,
the loads increase as well due to more friction. The trends are otherwise similar to those
seen at only 5000 ft, with a gradual increase of load due to viscosity. However, it can be
seen that as the length of the rod increases, the increase of viscosity has a greater impact
on the increase of the polished rod loads. This is to say that as the length of the rod
increases, the effect of viscosity is much greater. This is because of the βrod heavyβ
phenomenon where the counterbalance effect (counterweights for the conventional and
Mark II units) of the rods is greater than the effect of the weights, which causes more stress
on the rods. It should be noted that based on the results for the polished rod loads, the effect
of viscosity can be neglected at 500 centipoise or below, with only about a 1.5% increase
on the PPRL and a 2.7% increase on the MPRL.
42. 33
Figure 31: Conventional Units: Percent Increase of PPRL at 5000 ft due to Viscosity
Figure 32: Conventional Units: Percent Increase of MPRL at 5000 ft due to Viscosity
43. 34
Figs. 31 and 32 show both the magnitudes (bars) of the PPRL and MPRL at 5000 ft on the
left y-axis and the percent increase (line) due to viscosity of these loads on the right y-axis.
It can be seen that for conventional units, when increasing the viscosity from 0 to 6000 cp,
the increase of the PPRL is about 15% and the increase of the MPRL is 33%. Again, it
should be noted that based on purely the polished rod loads, the effect of viscosity can be
neglected at 500 centipoise or below. The results for the effect of viscosity and length as
well as the percent increase are quite similar for the air balanced and Mark II units as seen
in the appendix.
Figure 33: Comparisons of PPRL Percent Increase of the Three Units at 5000 ft
44. 35
Figure 34: Comparisons of MPRL Percent Increase of the Three Units at 5000 ft
Figs. 33 and 34 show the comparisons of the percent increase for both the PPRL and the
MPRL for all of the three pumping units at 5000 feet. There is about a 14-16% increase
evident in the PPRL for all three pumping units when the viscosity is increased from 0 to
6000 cp and a 32-40% increase in the MPRL for the three pumping units. It can be seen
that in both of these plots, the Mark II units have a higher percent increase in the loads due
to the viscosity increase than the conventional and air balanced units. Due to the geometry
and the lever system, the Mark II units are designed to decrease the rod load. However,
with the effect of viscosity affecting all of the pumping units similarly, the lower magnitude
initially with the inviscid fluid in the Mark II units will cause the increase to be of a higher
rate with high viscosity fluid than the other pumping units. Again, with the increase of the
fluid viscosity, the friction between both the fluid and the rods and the fluid and the casing
are also higher which causes these increases of the polished rod loads. These percent
increases are quite significant to study when designing a pumping system as some oil can
have a viscosity of up to 10,000 cp.
45. 36
6.1.2 Peak Torque Results
Figure 35: Conventional Units: Effect of Viscosity on Peak Torque (Upstroke /
Downstroke)
Moving from the effect viscosity has on the polished rod loads, there is also a sizable
impact it has on the peak torque, both on the upstroke and downstroke as well as the overall
torque. In Figs. 35-37, the peak torque in both the upstroke and downstroke are presented
for all three pumping units. There are similar increases in the peak torque on the upstroke,
due to the increased stress put on the rod and more friction with increased viscosity as the
fluid is being carried to the surface. There are also similar decreases associated with the
peak torque on the downstroke as for all the pumping units, the heavier the oil is, the less
torque needed to lower the plunger after the fluid has been unloaded on the surface. The
different behavior is discussed beneath each plot. In Fig. 35, for the conventional units, the
peak torque on the upstroke demonstrates an increase of 35% over 4000 cp and the peak
torque on the downstroke experiences about a 39% decrease over 4000 cp. This is the
expected behavior for the conventional unit with more torque needed on the upstroke for
an inviscid fluid than on the downstroke.
35.305% increase
39.041% decrease
46. 37
Figure 36: Air Balanced Units: Effect of Viscosity on Peak Torque (Upstroke /
Downstroke)
Fig. 36 shows the behavior of the peak torque on the upstroke and downstroke for an air
balanced unit. There is about a 36% increase on the upstroke at 4000 cp and a 35% decrease
on the downstroke at 4000 cp. This is a distinct difference from Fig. 35 as it can be seen
that more torque is needed at low viscosity on the downstroke in air balanced units than
conventional units. This phenomenon is also seen in the Mark II units and explained below.
35.463% decrease
36.096% increase
47. 38
Figure 37: Mark II Units: Effect of Viscosity on Peak Torque (Upstroke / Downstroke)
When comparing both Figs. 36 and 37 with Fig. 35, it can be seen that more torque is
needed on the downstroke for inviscid fluids in the air balanced and Mark II units than in
conventional systems. This is much more evident for the Mark II units in Fig. 37, however.
This can be explained from the geometry of both the air balanced and Mark II units. Both
of these pumping units employ more degrees of crank travel on the upstroke, which leads
to a 195Β° upstroke. This change with the shifting of the gear reducer, first and foremost,
reduces the polished rod loads by decreasing the acceleration on the upstroke stage where
the greatest load can be seen. However, the unique position of the gear reducer also has
consequences for the torque. Because the gear reducer is shifted from underneath the
equalizer (conventional) towards the Samson post, the cross-yoke, located by the
horsehead, is forward of the gear reducer (air balanced, Mark II). In lifting the heavier load
on the upstroke, a greater mechanical advantage is created, and a lesser mechanical
advantage is created for the reduced downstroke load. Because of this, both the maximum
torque factor on the upstroke decreases and the maximum torque factor on the downstroke
increases (Lufkin, 2013). This shift is more evident in the Mark II units and can be seen in
Fig. 37, and to a lesser extent in the air balanced units in Fig. 36 as well. Also, with some
heavy oils having viscosity as high as 10,000 cp, this very high increase in torque must be
considered in the pumping unit design.
32.798% decrease
40.702% increase
48. 39
Figure 38: Comparisons of Peak Torque Upstroke of the Three Units at 5000 ft
Figure 39: Comparisons of Peak Torque Downstroke of the Three Units at 5000 ft
Figs. 38 and 39 simply compare the magnitudes of the peak torque on the upstroke and
downstroke for all three pumping systems at 5000 feet. These results agree with the
49. 40
geometry as well as the features described in the literature review section for the Mark II
units. This unit not only helps to lower the power costs and the size of the prime mover,
but also reduce the torque requirements on the gear reducer up to 35% (Lufkin, 2013).
Figure 40: Conventional Units: Effect of Viscosity and Length on Peak Torque
Fig. 40 shows the relationship between the length of the rod and viscosity on the overall
peak torque for a conventional unit. This is the expected result: an exponential increase of
torque as the length increases with the effect of viscosity being much greater at high
lengths. This is again because of the βrod heavyβ phenomenon where the counterbalance
effect (counterweights for the conventional and Mark II units) of the rods is greater than
the effect of the weights, which causes more stress on the rods. This plot also shows that,
similarly to the polished rod loads, at fluid viscosities 500 cp and below, the viscosity
effects can be neglected, with only a 4.4% increase in the PT.
50. 41
Figure 41: Conventional Units: Percent Increase of Peak Torque at 5000 ft due to
Viscosity
Fig. 41 shows the magnitudes of the peak torque at 5000 feet along with the percent
increase at the different viscosities from 0 to 6000 cp for a conventional unit. This plot
shows that for a 6000 cp fluid, there is approximately a 53% increase in the peak torque
required. When compared to the polished rod load percent increase plots (Figs. 31-32), it
can be concluded that heavy oil has a greater impact on the torque requirements than the
polished rod load requirements. This is even more prominent due to the fact that some
heavy oils have viscosities up to 10,000 cp, which may even double the torque needed in a
pumping unit. This will shift major emphasis on design considerations.
51. 42
6.1.3 Efficiency Results
Figure 42: Conventional Units: Effect of Efficiency and Viscosity on PPRL
From the general relationship of viscosity and efficiency seen in Fig. 9, there are also
correlations seen with each of these variables on the polished rod loads, as seen in Figs. 42
and 43. As the efficiency was increased in the simulator, both the stroke speed (N) and the
plunger stroke length (Sp) decreased. The equation for the stroke speed is:
ππ =
ππβπ΅π΅ππ
0.1166βππβπ·π·ππ
2βππ
(39)
The plunger stroke length is a function of both the dimensionless rod stretch and
dimensionless pump speed as found in the digitization chapter. Because the change in
efficiency has a direct relationship with the stroke speed and it is used in the calculation of
the dimensionless pump speed, the efficiency has a direct relationship with both of these
parameters. The change in the dimensionless pump speed impacts all of the plots involved
in the digitization, however, most notably, the polished rod loads. The range of efficiency
that was observed was from 0.75 to 1; pump efficiency is ordinarily a fraction around 0.9,
and values outside of this range were resulting in abnormal output.
52. 43
Figure 43: Conventional Units: Effect of Efficiency and Viscosity on MPRL
Figs. 42 and 43 show the effect of efficiency on the polished rod loads for conventional
units only. These results are similar to those of air balanced and Mark II units and those
plots can be found in the Appendix section. From Figs. 42 and 43, it can be seen that as the
pump efficiency increases from 0.75 to 1, the PPRL slightly decreases, while the MPRL
slightly increases; this is due to fluid inertia effects. Pump efficiency affects the dynamic
fluid load on the plunger (Svinos, 2008). Because sucker rod pumps employ high speed
prime movers, it is important to consider the rotating moments of inertia when simulating
pumping parameters. These moments of inertia refer to those associated with the
counterweights, cranks, gear reducer, walking beam, horsehead, and the motor. All of these
individual moments of inertia are seen to lower the torque, PPRL, and PRHP and increase
the MPRL. This is because as the torque on the gear reducer increases during pumping, the
prime mover decreases speed. This then causes the crank and counterweight inertia to
release energy which in turn, lowers the torque the gear reducer can supply. The inertia of
the walking beam and horsehead, conversely, adds torque to the gear reducer, however,
this effect is quite small. As the prime mover slows down with the high torque, the polished
rod load slows down as well (Svinos, 2008). This reduction in speed leads to lower dynamic
forces which leads to a lower PPRL, PRHP and a higher MPRL. It is known from previous
results that as the viscosity increases, an increased load will also be seen. Fig. 44 is the plot
between the PRHP and Efficiency: (It should be noted that the Polished Rod Horsepower
is the same for all three pumping units as described in API-RP 11L)
53. 44
Figure 44: Polished Rod Horsepower (HP) vs Efficiency
6.2 Discussions
This study is an attempt to further expand the API-RP 11L process to include the
application of viscous oil and the effect viscosity has on the pumping characteristics the
process helps to predict. The approach involved four stages: the digitization of the API-RP
11L plots to develop equations for each pumping parameter which served as inputs to the
second stage β the simulator developed, the development of the frictional pressure losses
gradient equation, and lastly, determining the effect of viscosity on several pumping
characteristics with the use of the simulator and pressure gradient equation.
Each stage of the project presented numerous challenges in both the design and
optimization. The first objective of the project was the digitization of the API-RP 11L plots,
which proved to be quite the task as the solver data analysis tool in Excel is quite involved.
The technique is based upon setting an objective cell equal to a certain value, or
maximizing or minimizing it by changing certain variable cells. In the case of this work,
the variable cells are the coefficients of each digitization equation based on the plots in
Figures 10-19. To subject the objective cell to the appropriate delineation of optimization,
constraints must be added. These included subjecting specific cells to maintain their values,
most of which being the most important values. These were primarily the first and last
points or points of deviation in each plot. This was the most time-consuming part, as the
constraints had to be optimized to ensure the best fit plot for the work conducted. This stage
also was the backbone of the project as the primary results were based off of the digitization
process.
54. 45
The next stage of the project was implementing the API-RP 11L procedure along with the
equations generated from the digitization into a computer simulator. This simulator enables
the operator to predict certain pump characteristics without the use of tables and figures
found in literature. The simulator is set up so the user can input all of the pertinent data
(production rate, specific gravity, pump depth, stroke speed and length, etc...) and the
simulator will present all of the API dimensionless groups along with the associated loads,
torques, and horsepowers needed in all three pumping units (conventional, air balanced,
and Mark II) to model any pumping system. The accuracy of the simulator was validated
from SPE 20152, as seen from Figs. 21-25 in the results section.
The third stage of the project was solving the equation for the frictional pressure losses
gradient. This included going through the general form of the momentum equation with
many assumptions (described in chapter 5) in order to find an equation for the gradient
dependent on the viscosity, holding the velocities constant. The derivation and
simplification of certain integrals proved to be the challenge, especially when calculating
the flow rate based upon the velocity profile.
In deriving the final pressure gradient equation, there were numerous steps taken. First, the
theoretical equation of the pressure drop in annular flow of Newtonian fluids was
considered. The velocity of the rod was not considered in this step in order to validate the
results of the derivation agreed to that in literature. Then after the work correlated to that
in literature, the velocity of the rod was added in order to get the final equation. The result
included an equation that stated if the average flow velocity and the velocity of the rod
were held constant along with the radii, the viscosity could be varied in order to calculate
the pressure drop gradient. This gradient could then be multiplied by the total length to
achieve the additional pressure friction would induce based on the viscosity that must be
added to the loads calculated in the simulator. This equation was used quite extensively in
the last stage of the project.
The final stage of the project was numerically finding the effects of viscous oil on the
pumping characteristics predicted from the simulator. The results are seen not only from
Figs. 26-44 in the results section, but also in the plots seen in the Appendix. It can be seen
that based on all of the plots that there is quite a correlation between viscosity and the
associated loads and torque on the system as a whole. High viscosity fluids greatly increase
the magnitude of the polished rod loads and torque, both on the upstroke and downstroke
as well as overall. The effect is seen more so when calculating the torque than the polished
rod loads, but is still quite high in both parameters.
Of course, the standard gravity of oil or lighter oils can be produced with standard pump
designs, however pumping very heavy oil will call for major design changes when
designing a pump. Rod centralizers, paraffin scrapers and rod guides will need to be
employed as they not only help keep the rods and couplings away from the tubing to
decrease the wear, but also aid in the stabilization of the pump. Pump and rod wear occur
much more frequently for heavy oil applications. Viscous oil production will also call for
a heavier rod string for more support and that leads to a heavier counterbalance effect. As
55. 46
it can be seen, viscous oil production is much more costly and difficult than lighter oil
production.
56. 47
CHAPTER 7
CONCLUDING REMARKS
The goal of this work was to improve upon the API-RP 11L procedure as it is used only
for inviscid or low viscosity fluids. Also, to create a simulator where instead of using tables
and figures to calculate the parameters needed, equations are used.
The following conclusions can be drawn from the study:
β’ The digitization used in this study along with the computer simulator seem
to slightly underestimate the peak polished rod load and peak torque.
β’ Heavy oil has a major effect on rod loads and torque, but as seen in the plots
in the results section, the effect on the torque is much higher than is seen on
the rod loads due to the stress that is put on the gear reducer (>50% vs
~25%).
β’ For conventional units:
o 10% increase on PPRL from 0 β 4000 cp
o 25% increase on MPRL from 0 β 4000 cp
o 35% increase on the Peak Torque Upstroke from 0 β 4000 cp
o 40% decrease on the Peak Torque Downstroke from 0 β 4000 cp
o 55% increase on Peak Torque from 0 β 6000 cp
Based on these conclusions, this work shows the modeling of a pumping system becomes
far more complicated when dealing with a heavy oilfield. As stated before, heavy oil
reservoirs present a mountain of problems, from cementing and keeping the wellbore
integrity to very close pressure maintenance (Halliburton, 2009). Cost is also one of the
most, if not the most important factor in the decision to drill a heavy oil reservoir.
This research helps to quantify the effect of the viscous oil on the pump system based on
the momentum equation as well as give the operator an easier method to predict pump
loads and torque requirements. However, with the rod stretch seen downhole with the
production of heavy oil as well, there is still much to be understood regarding the effect of
viscosity not only on the surface equipment, but also downhole.
57. 48
CHAPTER 8
FUTURE WORK
The following are some recommendations for suggested areas of further research:
β’ Drill string Design / Buckling Applications
β’ Drag and Torque Applications for straight and inclined wellbores
β’ Finding the ideal stabilizer positions as well as the distance required
between them.
58. 49
REFERENCES
Black Gold Pump and Supply, Inc. Plungers: Monel. (2015). Signal Hill, California.
Heavy Oil Industry Challenges β Halliburton Solutions Summary. (2009). Houston,
Texas.
<http://www.halliburton.com/public/solutions/contents/Heavy_Oil/related_docs/
H06685.pdf>
Herzog, S., Neveu, C., Placek, D. (2005). The Benefits of Maximum Efficiency
Hydraulic Fluids. Noria Publication: Machinery Lubrication. Louisville,
Kentucky.
Hyne, Norman J. (2012). Nontechnical Guide to Petroleum Geology, Exploration,
Drilling & Production, 3rd
Edition. Tulsa, Oklahoma.
Jennings, J.W, SPE. (1989). Design of Sucker-Rod Pump Systems. Society of Petroleum
Engineers SPE 20152. Texas A&M University.
<https://www.onepetro.org/download/conference-paper/SPE-20152-
MS?id=conference-paper%2FSPE-20152-MS>
Juch, A.H, Watson, R.J, SPE. (1969). New Concepts in Sucker-Rod Pump Design.
Society of Petroleum Engineers SPE 2152. Shell de Venezuela, Ltd.
<https://www.onepetro.org/download/journal-paper/SPE-2172-PA?id=journal-
paper%2FSPE-2172-PA>
Kelly, Michael. (2000). Rod Pumping Overview β Class Notes. New Mexico Institute of
Mining and Technology.
Lea, J.F., Rowlan, Lynn. (2014). Guidelines & Recommended Practices: Selection of
Artificial Lift Systems for Deliquifying Gas Wells. Artificial Lift Research and
Development Council. Austin, Texas.
Li, J., Han, M., Han, X. (2012). A New Pump Application in Heavy Oil Recovery.
Design Innovation Papers. China University of Petroleum.
<http://fluidsengineering.asmedigitalcollection.asme.org/article.aspx?articleid=14
40796>
Lufkin Conventional & Reverse Mark Pumping Units Operatorβs Manual A-82. (2013).
Lufkin, Texas.
Lufkin Air Balanced Pumping Units Operatorβs Manual A-82. (2013). Lufkin, Texas.
Lufkin Mark II Pumping Units Operatorβs Manual A-82. (2013). Lufkin, Texas.
59. 50
Rohatgi, Ankit. (2015). WebPlotDigitizer User Manual, Version 3.9. Austin, Texas.
<http://arohatgi.info/WebPlotDigitizer/userManual.pdf>
Rudnick, Leslie. (2013). Synthetics, Mineral Oils and Bio-Based Lubricants, 2nd
Edition.
Chemical Industries. Philadelphia, Pennsylvania.
Svinos, J.G, Treiberg, Terry. (2008). XROD-V: Advanced Modern Design and
Simulation of Rod Pumping Systems for Vertical Wells, 3rd
Edition. La Habra,
California.
<http://www.doverals.com/File%20Library/Theta/Manual%20and%20Brochure/
manual-xrod.pdf>
Takacs, Gabor. (2015). Sucker Rod Pumping Handbook: Production Engineering
Fundamentals and Long-Stroke Rod Pumping. Hungary.
60. 51
APPENDIX
Figure 45: Air Balanced Units: Viscosity Effect on Polished Rod Loads at 5000 ft
Figure 46: Mark II Units: Viscosity Effect on Polished Rod Loads at 5000 ft
10.449% increase
24.605% increase
10.731% increase
26.822% increase
61. 52
Figure 47: Air Balanced Units: Effect of Viscosity and Length on PPRL
Figure 48: Air Balanced Units: Effect of Viscosity and Length on MPRL
62. 53
Figure 49: Air Balanced Units: % Increase of PPRL at 5000 ft due to Viscosity
Figure 50: Air Balanced Units: % Increase of MPRL at 5000 ft due to Viscosity
63. 54
Figure 51: Mark II Units: Effect of Viscosity and Length on PPRL
Figure 52: Mark II Units: Effect of Viscosity and Length on MPRL
64. 55
Figure 53: Mark II Units: % Increase of PPRL at 5000 ft due to Viscosity
Figure 54: Mark II Units: % Increase of MPRL at 5000 ft due to Viscosity
65. 56
Figure 55: Conventional Units: Effect of Viscosity and Length on Peak Torque
(Upstroke)
Figure 56: Conventional Units: Effect of Viscosity and Length on Peak Torque
(Downstroke)
66. 57
Figure 57: Air Balanced Units: Effect of Viscosity and Length on Peak Torque
(Upstroke)
Figure 58: Air Balanced Units: Effect of Viscosity and Length on Peak Torque
(Downstroke)
67. 58
Figure 59: Mark II Units: Effect of Viscosity and Length on Peak Torque (Upstroke)
Figure 60: Mark II Units: Effect of Viscosity and Length on Peak Torque (Downstroke)
68. 59
Figure 61: Air Balanced Units: Effect of Viscosity and Length on Peak Torque
Figure 62: Air Balanced Units: % Increase of Peak Torque at 5000 ft due to Viscosity
69. 60
Figure 63: Mark II Units: Effect of Viscosity and Length on Peak Torque
Figure 64: Mark II Units: % Increase of Peak Torque at 5000 ft due to Viscosity
70. 61
Figure 65: Air Balanced Units: Effect of Efficiency and Viscosity on PPRL
Figure 66: Air Balanced Units: Effect of Efficiency and Viscosity on MPRL
71. 62
Figure 67: Mark II Units: Effect of Efficiency and Viscosity on PPRL
Figure 68: Mark II Units: Effect of Efficiency and Viscosity on MPRL
76. Applications of Viscous Oil in a Rod Sucker Pump System
By Utkarsh Bhargava
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