FAST POWER CONVERTERS AND RAPID DIGITAL DESIGN BY GRANT PITEL B.S., Cornell University, 2003 M.S., University of Illinois at Urbana-Champaign, 2005 DISSERTATION Submitted in partial fulfillment of the requirements for the degree of Doctor of Philosophy in Electrical and Computer Engineering in the Graduate College of the University of Illinois at Urbana-Champaign, 2008 Urbana, Illinois Doctoral Committee: Professor Philip T. Krein, Chair Associate Professor Patrick Lyle Chapman Professor P. R. Kumar Professor Peter W. Sauer ABSTRACT Switching mode power supplies (SMPS) have a diverse history of analysis techniques. Discrete controls introduce new techniques and software design steps that add value through more features, advanced control algorithms, and reduced time-to-market. These advantages can improve voltage regulation at the point of load in micro power systems and can better organize massive projects in macro power systems via model based design. Voltage regulator modules (VRM) are micro power systems that supply clean lowvoltage high-current power to microprocessor loads. Minimum-time control algorithms and active topological changes are proposed to reduce VRM parameter sensitivity—an alternative to more sophisticated linear control algorithms and enlarged passive components. Minimum-time control has an intuitive solution based on geometric surfaces. Curved surfaces built from model parameters can achieve ―b est‖ theoretical control performance. When applications have unknown or poor parameter knowledge they can implement system identification algorithms. Performance surpasses curved surface control limits when converter topology actively changes. Augmented converters with programmable conduction change their topology in a way that can completely eliminate voltage transients. Model-based design has revolutionized workflows in macro-scale engineering projects. Digital control facilitates bottom-up workflows where hardware, software, and design teams can work independently. These new workflows are tested for sending power into the utility grid on the Grainger Center modular inverter. ii To my mother iii ACKNOWLEDGMENTS I want to thank the Grainger Center whose generous support has allowed me to pursue research with long-term impact. Their contributions to the University of Illinois’extensive library collection and the resources made available through the Grainger Center for Electric Machinery and Electromechanics have enriched my graduate education. The National Science Foundation (NSF ECS 06-21643) is another generous program that has funded my research. I want to express thanks to Professor Krein who gave me the opportunity to study under him. He has devoted personal attention to both his undergraduate and graduate students, as demonstrated through his well structured lectures and his regular student advisory meetings. He has patiently mentored me for five years both technically and professionally, and instilled the importance of quality research and writing—two virtues I hope to maintain always. I have largely Joyce to thank for helping me execute that last virtue. Joyce committed countless hours of individual attention to hone my writing skills. A feat no elementary school, high school, or college teacher was willing to perform. Thank you Joyce. Graduate school has been a taxing process; I want to acknowledge Sheryl for her moral support. Having a more patient companion go through the same process helped me finish what I started. You accepted me for who I am—idiosyncrasies and all. I promise, once we get our degrees we will go on our first vacation where I leave my work behind. Mom and Dad, I want to thank you for giving me the resources I needed to succeed: a nurturing home, a college education, and some needed discipline. iv The Power and Energy Systems group provided a unique opportunity to work with and learn from other students within same specialization. In particular, I want to thank Jonathan for giving me his advice on hardware design, Wayne for helping me through my first control classes, and Brett and Nick for their willingness to share their engineering experiences with me. I want to especially thank all those who worked on the modular inverter. It was a valuable piece of equipment that saved me a lot of time. Also, I want to thank my friends, Brian, Rodney, Trishan, Matt, Zeb, Jason, Marco, Zack, Joe, Tim, Angel, Linda, and Kate. It was difficult being away from family and friends; your hospitality at BBQs and attendance at Power Hours helped Sheryl and me to feel at home. Finally, I want to thank all my professors whose lessons taught me the necessary background for writing this dissertation: Prof. Delchamps for teaching all my fundamental DSP classes, Prof. Land and Dan Block for teaching me embedded programming, Prof. Chapman for teaching my power electronics and machines classes, Prof. Overbye and Gross for teaching me power systems, and Profs. Kumar, Sauer and Spong for their lessons on advanced control and system analysis. v TABLE OF CONTENTS 1 INTRODUCTION......................................................................................................1 2 POWER ELECTRONICS MODELING.................................................................6 2.1 Voltage Source Buck Converter Model .......................................................... 8 2.2 Boost Converter Modeling ............................................................................ 12 2.3 Voltage Source Inverter Modeling................................................................ 14 3 FAST POWER CONVERTERS VIA CONTROL ...............................................17 3.1 Review of Line Switching Surfaces .............................................................. 22 3.2 Review on Curved Switching Surfaces......................................................... 24 3.3 N-Switch Edge Trajectories .......................................................................... 29 3.4 Minimum-Time Disturbance Recovery ........................................................ 32 3.4.1 Multiple line surface generation .......................................................... 37 3.4.2 Raster-surface generation .................................................................... 44 3.4.3 Sensitivity and transient analysis ......................................................... 54 3.5 Parameter Observers ..................................................................................... 61 3.5.1 A priori and posteriori knowledge ....................................................... 62 3.5.2 Nonparametric versus parametric models ........................................... 63 3.5.3 Candidate power converter model ....................................................... 66 3.5.4 Discrete-time model ............................................................................ 67 3.5.5 Review of recursive least square algorithm ......................................... 68 3.5.6 System identification performance metrics ......................................... 70 3.5.7 Simulated results.................................................................................. 72 3.5.8 Hardware experiment .......................................................................... 75 4 FAST POWER CONVERTERS ............................................................................81 4.1 System Performance ..................................................................................... 82 4.2 Unknown Load Disturbances........................................................................ 86 4.3 Known Load Disturbances ............................................................................ 88 4.4 Conclusions ................................................................................................... 90 5 RAPID PROTOTYPES USING MODEL-BASED DESIGN ..............................92 5.1 Single-Phase Grid Connected Control .......................................................... 95 5.2 Direct Digital Synthesis ................................................................................ 97 5.3 All Digital Phase-Lock Loop ........................................................................ 99 5.4 Software in the Loop Experiment ............................................................... 102 5.5 Rapid Control Prototypes and System Products ......................................... 104 6 CONCLUSIONS AND FUTURE WORK ...........................................................110 REFERENCES .............................................................................................................. 112 APPENDIX A MATHCAD SYMBOLIC MODEL DERIVATIONS ................... 121 A.1 Constant-Resistance Buck Converter ......................................................... 121 A.2 Constant-Current Buck Converter .............................................................. 126 vi A.3 A.4 Boost Converter .......................................................................................... 129 Voltage Source Inverter .............................................................................. 133 APPENDIX B SIMULINK CONTROL BLOCKS ................................................. 139 B.1 Voltage Mode Control (No Error Integrator).............................................. 139 B.2 One Cycle Control (No Error Integrator).................................................... 139 B.3 Peak Current Mode Control (No Error Integrator) ..................................... 139 B.4 Minimum Time Control (No Error Integrator) ........................................... 140 APPENDIX C SURFACE GENERATION ............................................................. 141 C.1 Rotated Line Surface Generation ................................................................ 141 C.2 Minimum-Time Surface Generation ........................................................... 142 C.3 Surface Approximation ............................................................................... 143 C.4 Raster Surface Search Algorithm................................................................ 145 C.5 Simulink Blocks: Main Block ..................................................................... 147 C.6 Simulink Blocks: Physical Power Converter Target .................................. 147 C.7 Simulink Code Blocks: Experiment Timers ............................................... 148 APPENDIX D SYSTEM IDENTIFICATION......................................................... 149 D.1 Continuous-Time Transfer Function Coefficients ...................................... 149 D.2 RLS Derivation with Sensor Scaling .......................................................... 151 D.3 Embedded RLS Function ............................................................................ 153 APPENDIX E GRID CONNECTED VSI ................................................................ 155 E.1 Open-Loop Control Derivations ................................................................. 155 E.2 SIL Root Block Diagram ............................................................................ 156 E.3 All Digital Phase Lock Loop ...................................................................... 157 E.4 Digital Controlled Oscillator....................................................................... 158 E.5 SIL—Inverter Startup Waveforms .............................................................. 159 E.6 SIL—Inverter Steady-State Waveform....................................................... 160 E.7 SIL—ADPLL Startup Waveforms ............................................................. 161 E.8 Hardware Grid Connected Inverter Block .................................................. 161 AUTHOR’S BIOGRAPHY .......................................................................................... 162 vii 1 INTRODUCTION Switching mode power supplies (SMPSs) are found in applications requiring small volume and weight, and efficient energy conversion. These traits have helped SMPSs establish presence in most areas of science. Their design requires multidisciplinary experience in circuits, thermodynamics, mechanics, electromagnetics, and system and control theory. As a result, SMPSs use a diverse and often jumbled collection of frequency and time-domain analyses, each with its own merits in electrical and mechanical systems. Digital control adds to the jumble with similar, but less intuitive domains. Frequency-domain analysis discerns steady-state stability using phase and gain margins, and performance using bandwidth and resonance. These metrics work well in passive circuits for frequency content systems (e.g., voice, data, and radio [periodic signals]). Time-domain analysis through differential equations, i.e., state-space representation, lends itself readily to numerical simulations and real-world performance metrics such as rise time, under- and overshoots, and slew rate. These metrics help describe systems with large-signal content (e.g., motors, cars, and planes [trajectory motion]). Although SMPSs are circuits, their switching and transient behavior is conveniently modeled in the time-domain. Time-domain is emphasized in this work. It is a powerful predesign tool, quantifies dynamic performance, and contains more rigorous stability and sensitivity tools. The digital-domain has sample-time and complex frequency-domain equivalents for the previously mentioned continuous-time/frequency analyses. Its strength lies not in its ability to mimic analog domains but in its ability to reformulate design problems. For 1 example, consider a bench-top power supply with binary i/o signals (current limit, voltage limit, faults, optical encoded knobs, etc). Simple interfaces built from discrete components and logic devices are one way to solve the problem, but complicated interfaces are best left to semantic programming languages. Using software functions to handle hardware problems greatly increases the designer toolset. Modern motion control functions are organized into five groups: communication, auxiliary functions, data acquisition and processing, power circuit interface, and system logic and control algorithms [1]. The first two groups are strong motivators in featurerich designs. The last three directly affect output performance. The same groupings are adopted in this work to describe programmable SMPS functions. Commercial ICs rely heavily on communication protocols such as SPI, I2C, and SMBUS, and on system-level protocols such as CAN. Auxiliary functions handle processes not directly involved in plant control, such as monitoring, display, user input, and diagnostics. Data acquisition and processing samples signals. System-logic and control algorithms govern output. Power circuit interface generates switching signals. Data acquisition is a specific research interest as it is the only listed digital function that interacts with mixed signals. Here a/d converters transform the plant into a sampled data system [2]. The traditional rule of thumb for linear systems is to sample 10 or more times faster than the plant frequency. The rule applies to power electronics when the switching frequency is 10 or more times faster than the averaged model frequency. This rate depends primarily on its energy storage elements. Low-power converters have small energy storage and thus need fast samplers and processors to keep loop speed near the averaged system dynamics—one reason it has taken nearly three decades for industry to 2 adopt fully digital control loops in micro power systems. This dissertation investigates nonlinear converter model performance, where the switching/control loop criterion does not apply. Control-loop speed depends on processor architecture, clock rate, instruction sets, memory, and bus width. The most common embedded architectures, ranked by increased processor performance, are microcontroller units (MCU), digital signal processors (DSP), and programmable logic devices (PLD) [3]. Programmable architecture cost and functionality, along with the five function groups previously listed, help define how digitally controlled power electronics evolved. The first generation of digitally controlled power electronics (1960-70) contained communication, auxiliary functions, and power circuit interfaces that supervised analog control loops [4] in processes called direct digital control [5] and direct digital synthesis [6]. Here, logic devices stored sampled switching functions [7] that could reduce harmonics sent onto the utility grid [8]. The second generation used data acquisition and processing to emulate the analog control loop in the digital domain [9]. Here control loop speeds could handle averaged dynamics, and engineers had design tools that were essentially the same as the analog design tools. The third generation has system logic and control algorithms that fully utilize processor capabilities. Here, control executes computationally intensive nonlinear control and observer algorithms, and engineers have sophisticated software-aided design tools for algorithm testing. Similar classifications were devised for power electronics control [10], where generations were distinguished by sampling/switching speed. This dissertation organizes the classifications according to the five function groups and engineering design tools. 3 Third-generation designers have tools with new coding and test methods. These address the need to improve workflows in macro power system projects, reduce development time, and test thoroughly and systematically. Software abstractions such as very high-level programming (VHLL), rapid control prototypes (RCP) [11], and software/hardware in the loop (SIL/HIL) testing make large-scale problems manageable for engineering teams. Success with these tools has been shown for dc distribution on electric ships [12], controls of automobiles [13], and electric locomotives [14]. Finally, third-generation digital control must add value over the previous generations. The value propositions in the power supply industry—― more features,‖ ― better performance,‖ and ―r educed time to market‖—are evident in the micro power systems sector for low-voltage regulation over a wide range of loads, temperatures, and set points. Voltage regulator modules (VRM ) are ubiquitous in commercial products. This dissertation researches minimum-time disturbance recovery, system identification, and active topology change for low-voltage regulators. It also investigates new design/test procedures, SIL and RCP, using a voltage-source inverter (VSI) that connects to the ac system. The dissertation is organized as follows. Chapter 2 covers power electronics model performance as defined by its circuit parameters. Models are essential components adopted in third-generation control algorithms. In Chapter 3, simple dc-dc converter models serve as predictors in fast performance controllers and as storage mechanisms in system identification algorithms. Minimum-time control via numerical trajectory paths— the fastest a fixed topology converter can react to any control or system disturbances—is introduced. Numerical solutions stored as curved surfaces are tested in hardware 4 experiments. Minimum-time results indicate that parameter knowledge affects how well a controller can react to disturbances. Identification algorithms can handle situations with poor knowledge. A power converter can achieve performance beyond minimum-time only if its topology or parameters change, as demonstrated in Chapter 4, through a concept called converter augmentation. Chapter 5 shows how macro power systems can be designed either top down or bottom up, like computer software, as is exemplified on the Grainger Center modular inverter. 5 2 POWER ELECTRONICS MODELING Modeling is an important step toward understanding SMPS control and system limitations. Models serve as an ideal environment to compare theoretical with hardware results, act as SIL for developing and testing complicated control algorithms, and store plant knowledge in third-generation digital controllers. This section gives an overview of system types, defines variables, and introduces the three power-converter models used throughout the dissertation. A general dynamical circuit model depends on a parameter vector, 𝜆, composed of passive circuit components, 𝑅; energy store elements, 𝐿 and 𝐶; and power sources, 𝐸 and 𝐼. A circuit can have a controlled input vector, 𝑢. Its output depends on its internal state vector, 𝑥, that contains currents, 𝑖𝐿 , through 𝐿, and voltages, 𝑣𝐶 , across 𝐶. The circuit dynamics are governed by the differential vector equation, 𝑥 = 𝑓(𝑡, 𝑥, 𝑢, 𝜆). (1) This equation can model nonlinear circuits. Approximations and constraints can make the equation practical for switching-circuit modeling and simulations. The first approximation assumes that all elements in 𝜆 are constants. The approximation makes the model an autonomous system composed of basic ideal circuit elements. The second approximation assumes the system has ideal 𝑁 switches that can configure 2𝑁 linear circuit network combinations. The third lets control configure these combinations with an switch index, 𝑖. These three approximations comprise an autonomous piecewise linear (PWL) system, 𝑓(𝑥, 𝜆, 𝑖) = 𝐴𝑖 𝜆 𝑥 + 𝐵𝑖 𝜆 , 6 (2) convenient for power electronics time-domain simulation. Here, 𝐴𝑖 (𝜆) and 𝐵𝑖 𝜆 are parameter-dependant matrices for any switch index. Switching describes the transition between different 𝑖. Numerically integrating (2), or summing its state-space solution, (3), over every switch period, simulates voltage and current state trajectories [15] and is the foundation for trajectory-based control [16, 17]. 𝑥(𝑡, 𝑥0 , 𝜆, 𝑖) = 𝑒 𝐴𝑖 (𝜆)𝑡 𝑥0 + 𝑡 0 𝑒 𝐴𝑖 (𝜆)(𝑡−τ) 𝐵𝑖 (𝜆)𝑑𝜏. (3) Piecewise solutions can model nonlinear power electronics phenomena such as limit cycles (a.k.a., ripple), but do not fit the linear system framework. PWL equations integrate with time steps shorter than the switching period—leading to slow simulations. When the switched system satisfies certain switching/parameter criteria, averaging can approximate state trajectories [18, 19]. Averaging (sometimes called the small-ripple approximation [20]) is rooted in singular perturbation theory whose results are generalized in the time domain using the Krylov-Bogoliubov-Miltropolsky method and in the frequency domain using multifrequency averaging methods [21, 22]. Averaging was popularized in power electronics with a less general technique called state-space averaging (SSA) [23], which removes ripple entirely. SSA combines matrices 𝐴𝑖 and 𝐵𝑖 into averaged matrices 𝐴𝑎𝑣𝑔 and 𝐵𝑎𝑣𝑔 using duty cycle control. The SSA buck, boost, and inverter models, presented in Sections 2.1-2.3, fit the bilinear equation 𝑥 = 𝐴𝑎𝑣𝑔 𝜆 𝑥 + 𝑢 𝐵𝑎𝑣𝑔 𝜆 𝑥 + 𝛾 𝜆 +𝛿 𝜆 , (4) where vectors 𝛾 and 𝛿 contain the model power sources [24]. The next three sections present symbolic SMPS models with the following format. First, a circuit schematic shows the topology and defines its parameters; second, a piecewise model (2) is shown; third, a bilinear (4), and lastly, a steady-state equation 7 describing the range of static equilibriums (a.k.a., a load line) are presented. The models were derived using Mathcad™; the code is listed in Appendix A. 2.1 Voltage Source Buck Converter Model The constant resistance load (CR) buck converter model shown in Fig. 1 has a voltage source 𝐸1 , ideal switches 𝑞1 and 𝑞2 , inductor 𝐿1 , with equivalent series resistance 𝑅𝐿1 , capacitor 𝐶1 with equivalent series resistance 𝑅𝐶1 , and load 𝑅1 . It has a PWL model (2), where 𝐴0 = − 1 𝑅𝐿1 +𝑅1 𝑅𝐶1 𝐿1 1 𝑅+𝑅𝐶1 𝑅1 𝐶1 1 − 𝐿1 − 𝑅1 +𝑅𝐶1 1− 1 𝐶1 𝑅𝐶1 𝑅1 +𝑅𝐶1 1 , 𝑅1 +𝑅𝐶1 𝐴1 = 𝐴0 , 𝐵0 = 𝑥= 0 , 0 𝑖𝐿 𝑣𝐶 and 𝐵1 = 𝐸1 𝐿1 0 . Fig. 1 Constant-resistance buck converter schematic 𝐴0 and 𝐵0 are the state matrices when 𝑞1 is open and 𝑞2 closed, and 𝐴1 and 𝐵1 are the matrices when 𝑞1 is closed and 𝑞2 open. Its SSA model is (4), where 8 − 𝐴𝑎𝑣𝑔 = 1 𝑅1 𝑅𝐿1 + 𝑅1 𝑅𝐶1 + 𝑅𝐿1 𝑅𝐶1 𝐿1 𝑅1 + 𝑅𝐶1 1 𝑅1 𝐶1 𝑅1 + 𝑅𝐶1 Bavg = 1 𝑅1 𝐿1 𝑅1 + 𝑅𝐶1 , 1 1 − 𝐶1 𝑅1 + 𝑅𝐶1 − 0 0 , 0 0 𝐸 𝛾= 𝐿 , 0 𝛿= 0 , 0 and 𝑢 = 𝑑. Duty cycle 𝑑 is the duration during which 𝑞1 is closed. The SSA buck model has a continuum of infinite switching frequency equilibrium points, 𝐸1 𝑥𝑒 (𝜆, 𝑢) = 𝑅1 +𝑅𝐿1 𝐸1 𝑅1 𝑅+𝑅𝐿1 𝑢 𝑢 , (5) defined over the duty cycle range, (0,1). The linear time invariant (LTI) model applies directly to linear-system and control-theory frameworks, a property used extensively in Section 3.5. The constant current load (CC) buck converter, shown in Fig. 2, has constantcurrent output 𝐼0 . The approximation is popular for small-signal modeling. It simplifies analysis and accurately approximates constant-resistance dynamics, but cannot accurately approximate its large-signal equilibria, as will be shown mathematically. The CC buck converter produces a PWL model (2), where 9 𝐴0 = − 1 𝑅𝐿1 + 𝑅𝐶1 𝐿1 1 − 1 𝐿1 0 𝐶1 , 𝐴1 = 𝐴0 , 𝐼0 𝑅𝐶1 𝐵0 = 𝐿1 𝐼0 – , 𝐶1 and 𝐸1 + 𝐼0 𝑅𝐶1 𝐿1 𝐵1 = 𝐼0 – 𝐶1 The SSA produces the bilinear differential equation (4), where 𝐴𝑎𝑣𝑔 = − 1 𝐿1 𝑅𝐿1 + 𝑅𝐶1 1 𝛾= 0 0 𝐸1 𝐿1 0 0 , 0 , and 𝐼𝑜 𝑅𝐿1 𝛿= 1 𝐿1 0 𝐶1 𝐵𝑎𝑣𝑔 = − 𝐿1 𝐼0 – , 𝐶1 Fig. 2 Constant-current buck converter schematic 10 , The SSA model has a continuum of infinite switching equilibria, 𝑥𝑒 (𝜆, 𝑢) = 𝐼0 , 𝐸1 𝑢 − 𝐼0 𝑅𝐿1 (6) defined over the range of 𝑢. The SSA buck converter models accurately approximate fast-switching PWL models when 𝑞1 and 𝑞2 are bidirectional-conducting bidirectional-blocking (as with synchronous buck converters), or 𝑞2 is forward-conducting reverse-blocking with 𝑖𝐿 𝑡 > 0 (as with continuous conduction mode (CCM) buck converters containing freewheeling diodes). The CC and CR buck converter models were verified by simulating CCM startup for a PWL model superimposed on its SSA approximation, as shown in Fig. 3 and Fig. 4, respectively. More complicated SMPS modeling can become a tedious and time-consuming endeavor. Modern simulation packages have somewhat alleviated modeling effort (e.g., Piecewise Linear Electrical Circuit Simulator [PLECS]) with functions that can extract indexed state matrices from graphical circuit schematics. Unfortunately, these functions lump components and evaluate them as numeric matrices. Symbolic matrices provide Fig. 3 PWL / SSA CR buck converter comparison (𝑅𝐿1 = 10 mΩ, 𝑅𝐶1 = 10 mΩ, 𝐸1 = 5 V, 𝑅1 = 1 Ω, 𝐿1 = 5 mH, 𝐶1 = 100 μF, and 𝑢 = 0.2) 11 Fig. 4 PWL/SSA CC Buck converter comparison (𝑅𝐿1 = 10 mΩ, 𝑅𝐶1 = 12 mΩ, 𝐸1 = 10 V, 𝐼𝑜 = 4.167 A, 𝐿1 = 0.8 mH, 𝐶1 = 1.29 mF, and 𝑢 = 0.313) valuable insight into how components affect system performance. This dissertation presents symbolic equations whenever possible. The symbolic derivations for CR and CC buck converter models are given in Appendices A.1 and A.2, respectively. 2.2 Boost Converter Modeling The boost converter model, shown in Fig. 5, has the same component variables as defined in Section 2.1. This topology produces the PWL model (2), where 𝐴0 = − 𝑅𝐿1 𝐿1 1 𝐶1 𝐴1 = − − − 𝑅𝐿1 − , 𝑅1 𝐶1 0 𝐿1 0 1 𝐿1 1 1 𝑅1 𝐶1 𝐸1 𝐵0 = 𝐿1 0 and 𝐵1 = 𝐵0 . 12 , Fig. 5 Boost converter schematic The SSA for the model produces the bilinear differential equation (4), where 𝐴𝑎𝑣𝑔 = 𝐵𝑎𝑣𝑔 = − 𝑅𝐿1 0 𝐿1 1 0 𝑅1 𝐶1 1 0 − 𝛾= 𝛿= , 𝐿1 𝑅1 0 𝑅1 𝐶1 , 0 , 0 𝐸1 𝐿1 0 , and 𝑢 =𝑑−1 Duty cycle 𝑑 is the duration in which 𝑞1 is closed. The SSA model approximates the PWL model under the same conditions specified for the CR and CR buck converters described in Section 2.1. 𝐸1 𝑥𝑒 (𝜆, 𝑢) = 𝑅1 𝑢 2 +𝑅𝐿1 𝐸1 𝑅1 𝑢 𝑅1 𝑢 2 +𝑅𝐿1 (7) Numerical integration easily simulates bilinear circuit models. The models were verified by simulating the PWL and SSA model for a CCM startup condition, as shown in Fig. 6. Linearization reduces the bilinear model to fit the linear control framework. Such a 13 reduction is useful for systematically defining linear feedback gains [25]. The process discards large-signal behavior and approximates local dynamic behavior about 𝑥𝑒 . The symbolic derivations for previous equations are shown in Appendix A.3 = Fig. 6 PWL/SSA boost converter comparison (𝑅𝐿1 = 10 mΩ, 𝑅𝐶1 = 0 mΩ, 𝐸1 = 5 V, 𝑅1 = 1 Ω, 𝐿1 = 5 mH, 𝐶1 = 100 μF, and 𝑢 = 0.2) 2.3 Voltage Source Inverter Modeling The voltage source inverter (VSI) model, shown in Fig. 7, has the same components and variables as defined in Section 2.1. This topology produces the PWL model (2), where 𝐴0 = − 𝑅𝐿1 − 𝐿1 1 − 𝐶1 − 𝐴1 = 𝐴2 = 𝑅𝐿1 𝐿1 𝑅1 𝐶1 1 𝐿1 1 𝐿1 1 − 𝐶1 𝐵0 = , 1 − 𝑅1 𝐶1 𝑅𝐿1 − , 0 0 − 1 𝐿1 1 𝐸1 𝐿1 0 𝑅1 𝐶1 , 14 , and 𝐵2 = 𝐵1 = 𝐵0 . Here, 𝑖 = 0 when 𝑞1 and 𝑞2 are closed and 𝑞3 and 𝑞4 are open; 𝑖 = 1 when 𝑞1 and 𝑞2 are closed and 𝑞3 and 𝑞4 are open; and 𝑖 = 2 when 𝑞1 and 𝑞2 are closed and 𝑞3 and 𝑞4 are open. The circuit is classified as a switch matrix [26], which creates multiple power converters based on index combinations. A system with 𝑖 = 0,2 is a two-level VSI inverter. A system with 𝑖 = {0,1,2} is a three-level VSI. A system with 𝐸1 (𝑡) = 170sin (120𝜋𝑡) is a grid-connected VSI inverter. The three-level VSI produces the bilinear differential equation (4), where 𝐴𝑎𝑣𝑔 = − 𝑅𝐿1 0 𝐿1 1 0 𝑅1 𝐶1 0 𝐵𝑎𝑣𝑔 = − 𝑅1 1 𝐿1 0 𝑅1 𝐶1 𝛾= , , 0 , 0 and 𝛿= 𝐸1 𝐿1 0 . The input, 𝑢 = 𝑑 − 1, is the 𝑞2 duty cycle with values −1,1 , as was modeled in [27]. The SSA approximates the PWL model when devices switch quickly. The SSA model has a continuum of infinite switching equilibrium points, 𝐸1 𝑥𝑒 (𝜆, 𝑢) = 𝑅1 𝑢 2 +𝑅𝐿1 𝐸1 𝑅1 𝑢 𝑅1 𝑢 2 +𝑅𝐿1 15 (8) The bilinear VSI model was tested by simulating startup for a VSI that boosts grid voltage. 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Wu, "Direct PWM synchronization using an all digital phase-locked loop for high power grid-interfacing converters," in IEEE Applied Power Electronics Conference, Anaheim, CA, 2007, pp. 901-906. 120 121 APPENDIX A MATHCAD SYMBOLIC MODEL DERIVATIONS A.1 Constant-Resistance Buck Converter NON-IDEAL AVERAGED A BUCK CONVERTER WITH CONSTANT RESISTANCE LOAD Full Model Active switch on substitute ,13 Vc + R esr · iL = ----R+ Resr --> 12 = simplify Vc- R· iL R + Resr state equations: R· Resr" Vc - R· iL dYe vc-R·iL dt C 2 · ( R + Resr ) dYe - dt dve expand,vc , iL ----+ - = dt 1 R 1 1 C R+ Resr C R+ Resr = -. - - - . iL - - . - - - , Yc 122 i Active switch off substitute ,13 vC+Resr"iL = ----R + Resr --> 12 = simplify dve - dt dve - dt dve dt 1 1 C2 C2 = - . ic = 1 = -. ( iL - 1 .12 = - . C2 Vc + R esr · iL) R + Resr C2 vc-R·iL C2 · (i L - 13) 1 ( = - . iL C2 substitute,I2 dve expand,vc , iL ----+ ( R + Resr ) cit = = ve + R,~, . iL) ----R + R,~, Vc - R· iL R + Resr dve ----+ dt = Vc - R· iL C 2 · (R + Resr) dve - dt 123 1 R C R+ Resr = -. - - - . 1 1 C R+ Resr iL - - . - - - . Vc R . Rdcr + R . Resr + Rdcr . Resr L . (R: L· (R + Resr) R C. (R R,~,) l ~ R,~,) J BavgCE,L, d) :~ Mavg(B(E,L) ,d) Bavg is BavgCE, L, d) simplify The L TI buck model is dx avg -- = dt Aavg . x avg + Bavg' u where u = d The input duty to state transfer function H(s) is H(s) = yes) = c . (s . 1- Af 1 B U(s) The input duty to voltage output transfer function is R . Rdcr + R . Resr - Rdcr' Resr L. (R - R",) R simplify Hvc(T"R,r:,R,Rdcp Rcsps) Icollect,s F, . R ----)0 - - - - - - - - - - - - - . : . : . . . . . : . : . . . . - - - - - - - - - - - - - ( ) , ( ) C . L . R + C . L· Resr . ~,t + L + C . R· Reier + C . R· Resr + C . Rdcr' Resr . S + R + Rdcr Ii ~T" R, r:, n, Rdcp Rcsps) :- - - - : - - - . , - - - - - - - - , - - - - - - - - - - - - , - - - - - ; - - - . , - C.L.(1 + R"'). s2+ (.1:.R + C.Rd _C.R + C· RduR .R~,) .s+ (1 + RJUj' R R cr eST santlty check Hvc(L,R,C,E,Rdcr,Re~r's) substitute,Re,r =0 E·R ---+ - - - - - - - - - - - - - R + Rocr + L . s + C . R . Rdcr . S - C . L . R . ,,,2 124 same result as Ideal buck The input duty to inductor current output transfer function is ,. (R: RoJ]'. [~: R . Rdcr + R . Resr + Rdcr . Resr L· (R + Resr) R HiL(L.R.C.E . Rd" . R,~,.s) simplify I 11 C. (R + R,~,) ] E + s . (C. E· R + C . E· R,~,) --> - - - - - - - - - - - - - - - - ' - - - - - - - - - = - ' - - - - - - - - - - - - - co ect,s 2 (C . L . R + C . L . Resr) . S + (L + C . R . Rdcr + C . R . Resr + C . Rdcr . Resr) . S + R + Rdcr E + s . (C. E· R + C . E· Resr) ~L.R.C.E.Rd".R,~,"s):~ - - - - - - - - - - - - - - - - ' - - - - - - - - = ' - - - - - - - - - - - 2 (C . L . R + C . L . Resr) . S + (L + C . R . Rdcr + C . R . Resr + C . Rdcr . Resr) . S + R + Rdcr santity check E+C·E·R·s HiL(L.R.C.E.Rd,,"R,~,"s) substitute.R,~, = 0 --> - - - - - - - - - - - - - - - - - - 2 same result as ideal buck R+ Rdcr + L . s + C . R· R dcr · + C . L . R· s S time (ms) BuckMdlCOmpare2. mdl PLECS Circuit Circuit Scope2 Vs'R1 L 1' C1 ' (R1 +rC1 )s2+(L 1 +C1 ' R 1' rL 1 +C1 ' R1 ' rC1 +C1 ' rL 1' rC1 )s+(R1 +rL 1) DJty2'¥CTF Steady state solution (Geometric Load Line) lim Hvc(L,R,C,E,RdcpResps) simplify -----+ s --> 0 E· R· signum(R + RdcpO). E·R - - - ifR+Rdcr*O R + Rdcr We can quickly calculate the equalibrium by X' = A . xe + B =0 Xo = -(B + A- 1) xe(E,L,R,C,Resr,Rdcr,d) := 125 00 if R + Rdcr = 0 ~I [ j R+ x~E,L,R, C ,R,""Rdcr,d) simplify ---> iL = - - R + R dcr Rdcr v c = VCR.r and the inductor current has to be Vc E · R ·d R+ If the desired output voltage is R dcr then E·R E·d simplify RI :~ 2 126 V CRef ---> - - R A.2 Constant-Current Buck Converter NON-IDEAL AVERAGED A BUCK CONVERTER WITH CONSTANT RESISTANCE LOAD Full Model 10 Active switch closed 10 substitute ,13 ~=~-~ diL .. IslIllphfy ] =10 ~~=~-~ ] ] cit =L· YL =L{E] ] - (ve + 12 ·R esr + 1].Rdcr )] ] diL ] = -{EI dt L] [ve + (iL - IO)"Resr+ iL"R dcr] =L{E] ] [ve + (iL - 10)·Resr + iL·R dcr] diL expand,iL,vC ----+ dt diL E] + 10·Resr ] = -{EI + IO·R esr - (Rdcr + Resr)"iL - vC] = + eli L] L] dVe] ]] -dt =-e]. i e =-.1 2 =-·(iL e] e] r:~ l t [-±.(Rdcr + Resr) dvej - ] cit -i. 0 ve E] =-L] - -L] 10·Resr Rdcr·i L Res(iL + --- - --- - --L] L] L] ] --.(R dcr + Resr)"iL L ] -·vC L ] 13) =-·(iL e] (IL 1 (I 10) E] + ·lve) + _ _ - x - A].x + B] -10 l e ~~.Resr 1 ) 1 ~ Active switch open I] L, RL1 12 10 I] =iL 12 diL =iL - ] 13 13 =10 ] cit =L· YL =L{O ] diL ] cit =L{O ] diL ] ] (ve + 12 ·R esr + 1].Rdcr )] =L{O ] [ve + (iL - 10)·Resr + iL·Rdcr] [ve + (iL - 10)·Resr + iL·R dcr] expand,iL,ve ~ diL 10·Resr ve Rdcr·i L ] ] cit =-L-- - L - - L - - ] ] 10·Resr ] ] -.~(IO·R ) - (Rd + R ).i L - ve] = - - + --.(R d + R ).i L - -·ve Ll L esr cr esr Ll L cr esr L -dt = 127 Res(iL -L-] rdt 1_- l dvc cit j __ 1 -10 Resr diLI [-I'L,(Rdcr + Resr) - 'L I] (iL l ' ) + 2. 0 Vc C I~ (Io' l STATE SPACE AVERAGE FOR CONSTANT - x - AI, x+ B I ~ RESISTA~Ir.I:: I nAn o I :~E I ,L I 'C I ,Resr,IO):= ["Tl LI -10 o The LTI buck model is dx -dtavg - =Aavg 'xavg + B avg ,u where u =d f2(EI ,L I 'C I ,RespRdcr,IO,d ,xo,X I) := Aavg(LI ' C I 'Resr'Rdcr'lo'd){:~ J+ Bavg(EI ,L I ' CI ,Resr, IO ,d) IO,Resr + EI ,d - Rdcr' xO - Res r'xO 128 xI Solve equalibrium substitute,xl = IO"Resr + Erd - Rdcr"XO - Resr" xO I 10 - 10 - Xo - - - - = 0 solve, xo C1 ----,io C1 10 PWLSPACCLBuck.mdl IfUll """""~ Puls e Generat or ~ () > :I/~~ . o 10 20 30 Xo -->~-- simplifY 40 50 time (m s) 129 ~ Constant r-r-n ~ r-r-n ~ =0 A.3 Boost Converter NON IDEAL STATE SPACE AVERAGE when q1 = 0 ic=C·v'c , _ 1 . VC-C"lC ic Vc =iL - R FI when q1 = 1 ., _ 1 lL-L'"VL ic = C· ViC , _ 1 . Vc ·le C .i'L Vc ic=-R V'c = -~. (:) FI 130 fL 0 ) . (iL J Vs =( -i Vc + L v'c = (0 __ 1 ). (iLJ R· C Vc The stage space average matrices are ,[-~ d~ll M,", (A2(L,R,C,'L),d) 'impluy ~ d- 1 substitute u = d -1 1 --- --C M,"i B 2(E,L),d) 'impluy -+ c· R [~J BILINEAR FORM Consider the bilinear representation of a network with synchronous switches [IOJ, [11 J: d drx=f(x)+ug(x)+h'=Ax+u(Bx+y)+~ (1) where A and B are square constant matrices, and y and ~ are vectors representing constant power sources. We usulilly represent the vector fields f(x), g(x), and h as Bilinear sliding motion from Ramiraz (E t2(R,L,C,]i,fT.,Ye,1T.'U) simplify ---+ I l L vc+R.iL· u 131 SIMULATED RESULTS FOR NON-IDEAL BOOST BoostMdICompare_OpenLoop.zip iL (y ell ow - P\AL, purp le SPA) 100 50 1 ' \ 0 0 0.05 O~(yellc!:5P"A'L PJOrple SPA~25 03 0.3 5 40 0 ~-~--~-'--~--~-~_ _~_~ ~O ~p -~ ----~ ---~ ----~ ----:----~ --0 S L1J syste m1 %intialize variables %see BoostDesign.xmcd for values % power inductor C l ~ 66 0 e -6; filter capacitor % source voltage E ~ 125 ; ; 0. 05 01 0.15 0 0.05 01 0.15 02 0. 25 03 0. 35 , 02 0. 25 03 J 05 11=0.0 10 ; Vd ~ 25 0 0 0 Time desired output % load switching frequency Rl ~ 1 0; f s w ~30000; rLl ~O.O; D ~O. 5 0 1 ; Vb ~ 25 0; L SOlv e 'i L----+ __=E-,--_ 0= Isimplify L Vc R . u 2 + fL = R· u· iL E substitute,i L = - - - - E· R· u _ R· u 2 + fL----+ Vc = ____ 2 R u + fL simplify o CI :~ 0.129 The equalibrium in terms of u is Ll :~ 0.126 RI :~ I EI :~ 2.5 rLl:~ 0.044 ul x,,(RI,Ll , C I ,E I ,rLl ,ul ) l1oal,3 --> 132 :~ 0.2 29.8) ( 5.95 N I:~ 10000 0. 35 to solve in terms of vC (i.e. geometric form ) E2 0R - 4 0fL 0v e E+ ve = E oR ou J 2 R 2 2 El 0Rl - 4 0fLl 0ve f( v c) := El + _---'-_ _ _R _ l_ __ 2 ve 2 ve 0 solve,u --+ 0 2 R u + fL 0 f(10) E2 0R - 4 0fL 0v e E+ substitute , u = 0.1 25 + 0.1 68i 2 J R = ----'!.------.::..:....--- 2 ve 2 0 2 ve --+ iL = -/-r==:=====::::::::~ E20R - 4orLove2 ] R o E+ 0 simplify [ J II 2· Vc 2 l vCI :~ 5 The equalibrium in terms of vC is --> (130) 5.0 20 x,~ Rl, Ll, Cl, El ,ILl, vc) Example non-ideal load line R o 10 o ~~~-~--~ o 4 133 A.4 Voltage Source Inverter BOOSTING VOLTAGE SOURCE INVERTER WITH CIRCUIT DERIVATION R, EI ic=C·v'c I _ VC- 1 . C "l C ic = i L Vc -- R EI .i'L = Vs Vc + L (-L"fL 0 ) . (iL) v'c = (0 __ 1 ) .(i R· C ., _ 1 lL-L'"VL ic = C· ViC , _ 1 . Vc ·le C V'c = -~. (:) 134 L Vc ) EI ic=C·v'c , _ 1 VC- C . "l C EI diL ic = c· dve dve 1 . = - . Ie C ic 1 =-. (vs L Vc = -R 135 iL"rd SUMMARY positive current into plus side of capacitor charging inductor with lows ide switches l (lL) l . dx dt = A. x + B = (lL) Vc c::: = positive current into minus side of capacitor L 1 C . C::: dx dt = A. x + B = Vc = charging inductor with highs ide switches L o 136 STATE SPACE AVERAGE WITH DUTY CONTROL Suppose we are given two systems X' =Ao· x + Bo and x' = Aj . x + B j Than the average matrix is and the system average is if we let u = D - 1 and u is between 1 and -1 then 137 that alternate with duty cycle D simulation file: VSICompare_RevF.zip run lritvars to load syste m ard control parameters IVoltage Source Inverter Model Comparisonl run 5im r:l ot (Sco peData ) to piC( Vv 'NO " Gain Iv0--> Averaged Sys tem v.; " '" ,------,. " ~ vC Circuil 1 ~ .1 "I" Co rt rol Contro ll er 2 ~ 00 vS Vs q f .... ,,, ,,, q" q qn IV5': Vv PLECS Circuil ,c I Sign al General lY 138 Circuil2 iL~ ,c D ~ EQUALIBRIUM ANALYSIS solve iL in equalibrium 0=(1 0) [AAV.(LoRoCorLou) 0 0 C~) + BAV.(vsoL)] solveoiL --> Vs -r: Vc 0 solve vC in equalibrium R . vC . u 2 - R . v S . U + fL· v C CoR rL 0 R.vCou2_R.vSOU+fL"VC R·u·ys 0= - - - - - - - - - - - solve,vc ----+ - - - C· R· fL R. u 2 + fL iL = Vs-U·Vc substitute,vc fL = R·u·vs 2 R .u + fL Vc R .u + = ---------R D2 - 2 RoD + R + rL 0 = --'-2 Rovso(D-l) ----+ Vc 2 R u + rL Vs ----+ iL Rouovs = iL Vs = 2 ----+ iL R u + rL fL 0 V des = R· 139 Vs =-----'----R D2 - 2 RoD + R + rL R·u·vs 2 U substitute ,fL + fL 0 0 0 = 0 ----+ 0 Vs V des = -; solve, U Vs ----+ V des