# A Reconfigurable Buck, Boost, and Buck-Boost Converter: Unified Model and Robust Controller

Authors: Martín Antonio Rodríguez Licea; Francisco Javier Perez Pinal; Alejandro Israel Barranco Gutiérrez; Carlos Alonso Herrera Ramírez; Jose Cruz Nuñez Perez
Journal: Mathematical Problems in Engineering
 (2018)

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## Abstract

The need for reconfigurable, high power density, and low-cost configurations of DC-DC power electronic converters (PEC) in areas such as the transport electrification and the use of renewable energy has spread out the requirement to incorporate in a single circuit several topologies, which generally result in an increment of complexity about the modeling, control, and stability analyses. In this paper, a reconfigurable topology is presented which can be applied in alterative/changing power conversion scenarios and consists of a reconfigurable Buck, Boost, and Buck-Boost DC-DC converter (RBBC). A unified averaged model of the RBBC is obtained, a robust controller is designed through a polytopic representation, and a Lyapunov based switched stability analysis of the closed-loop system is presented. The reported RBBC provides a wide range of voltage operation, theoretically from-∞ to ∞ volts with a single power source. Robust stability, even under arbitrarily fast (bounded) parameter variations and reconfiguration changes, is reported including numerical and experimental results. The main advantages of the converter and the robust controller proposed are simple design, robustness against abrupt changes in the parameters, and low cost.


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## Body

## 1. Introduction

It is widely known that the main goal of power electronic converters (PEC) is to convert energy from one stage to another in the most efficient way [1–5]. Early stages of Power Electronics in the “Modern Era” were devoted to the development of devices, accurate modeling of topologies, advances of reliable architectures, and design of high-performance control laws [6–8]. Later, researchers work was to improve technology from devices and overall converters efficiency [9]. In recent years, the researching goals in the development of PEC are system cost reduction, new interconnection technologies for ultrahigh power density systems, wide temperature operation range, smart power conversion, simple power management, and high level of integration [10].In particular, examples of integrated PEC can be found in a wide range of different applications. For instance, in [11] an exhaustive review of converters configuration, power quality behavior, design guidelines, and overall selection was performed. In [12] an adaptive, proportional-integral (PI) controller was proposed for a power factor correction converter; a comparison between two conventional PI structures and adaptive one was performed. An interesting 12-polygonal space vector modulation technique in a matrix converter for direct torque control was proposed in [13]. An application to induction motors with variable speed was given achieving a significant reduction in torque ripple, noise, and vibration, shown by numerical simulations and extensive experimental tests. Evaluation and comparison of several multicarrier pulse width modulation (PWM) methods applied to solar powered multilevel inverters were reported in [14]. It was stated that switching losses, total harmonic distortion (THD), and electromagnetic interference (EMI) generated depend on the PWM method used.Actually, the integration of various PEC in a single circuitry (reconfigurable PEC or RPEC) is preferred because it has several advantages such as low cost, portability, modularity, an increment of power density, and a wide operation region [15–28]. However, this increment of versatility rises the modeling and control complexity. In order to overcome this concern, some advance control methodologies that work in operation regions rather than single operation points have been proposed by researchers, for instance, by intelligent [29–37], pulse adjustment [38], and hybrid controllers [39].Few studies have investigated the development of RPEC and even of integrated PEC considering them as a class of polytopic switched system (PSS) [40]. Particularly, a PSS is a class of hybrid system constituted of a set of piecewise polytopic systems that commute owing to a discrete event. Those systems have the advantages that the switching principle can be stated by design rules; as a result, the PSS representation allows designing robust controllers with quantitative bounds of parameter variation, and the stability even among switching events is ensured, for example, by a common Lyapunov function. The controllers based on PSS can have high flexibility and adaptability in a large set of operating conditions like current or voltage ripple, changes on power load or voltage source, and continuous, discontinuous, or critical operation mode, among others.In this paper a reconfigurable Buck, Boost, and Buck-Boost DC-DC converter (RBBC), unified/generalized-averaged PSS model of the RBBC, a robust voltage-mode controller, and a Lyapunov stability proof in closed-loop are proposed in order to advance our knowledge of integrated PEC and RPEC from a PSS perspective. This RPEC was developed to provide a unique, low-cost, and stable solution to several problems arising in Electric Vehicles and smart grid scenarios. For example, in an Electric Vehicle, a single solution to driving the power from the battery to the main motor is desirable in a wide range of speed forward direction and in low speed reverse direction while several parameters are dynamic. The model, controller, and stability proof presented can be used for any combination of the aforementioned converters, even in an on-the-fly reconfigurable scheme. Numerical data for a demonstrative Proportional-Derivative (PD) controller, implemented in an experimental testbed, are presented.This paper is organized as follows. The unified Buck, Boost DC-DC converter (UBBC) and the methodology for the modeling are described in Section2. An insight into components selection is described in Section 3. The proposed control and robust stability analysis of the output voltage in closed-loop are given in Section 4. Section 5 shows numerical simulations. Practical results of the proposed converter during start-up and steady state and between converter transitions using an experimental testbed are shown in Section 6. A final discussion is given in Section 7 and conclusions and final remarks are given in the last section.


## 2. Modeling

In this section, the schematic and the operating modes of the RBBC are presented; later a polytopic representation of the RBBC is obtained. Such polytopic representation is used to demonstrate the closed-loop stability of the RBBC, despite parametric uncertainty.In order to explain the functioning of the aforementioned RBBC consider the circuit shown in Figure1. The proposed RBBC has a single power source E. By managing a switching strategy, the power flow from the source E to the load R is possible with some desired polarization. Three operation modes are allowed, and each one of them is selected by a proper switching activation and by a pulse width modulation (PWM) MOSFET activation:(1)
S1, S2 closed, S3, M2 open, and PWM switching on M1, Buck(2)
M1, S2 closed, S1, S3 open, and PWM switching on M2, Boost(3)
M2, S3 closed, S1, S2 open, and PWM switching on M1, Buck-Boost.Figure 1
Proposed RBBC.A nonpolarized capacitorC is used and the load R uses a wide voltage vR range with reversible flow current demand iR.Consider Mode 1; the equivalent circuit idealized as the well-known noninverting Buck converter is shown in Figure2. S1 is PWM-switched, and an alternating voltage E is supplied to the RLC branch at high frequency when a voltage 0<vR≤E is needed.Figure 2
Mode 1 of the proposed RBBC.The MOSFET M1 is modeled as a variable resistanceR1(t) (Figure 3) with smooth transitions from very high to very low resistance and vice versa.Figure 3
Idealized Mode 1 of the proposed RBBC.In such idealization, the voltage supplied to theRLC branch can be taken as the average Vi(t) of a smooth time function (Figure 4):(1)Vit=Euˇt,where(2)0≤uˇt≤1is the PWM duty cycle. Equations that describe the dynamic behavior are(3)LdiLdt=uˇE-vR,(4)CdvRdt=iL-vRR.Note that system (3)-(4) coincides with the well-known averaged model of the Buck converter (see [41]). Substitution of (3) in (4) allows obtaining(5)v¨R=uˇELC-vRLC-v˙RRCand the equivalent representation in state space with x=[vR,v˙R]T=[x1,x2]T is(6)x˙=Ax+Buˇ,where [·]T denotes the transpose matrix operation, and (7)A=01-1LC-1RC,B=0ELC.Figure 4
Idealized Mode I schematic.Consider Mode 2; the equivalent circuit can be idealized as the well-known noninverting Boost converter shown in Figure5. M2 is PWM-switched and an alternating voltage E is supplied to the RLC branch at high frequency when a voltage vR>E is needed. Analogous modeling procedure allows obtaining the same state space representation (6) where u(t) represents the one-minus-duty-cycle inverse of the PWM signal; this is,(8)11-u^=ut>1 with u^ as the duty-cycle percentage.Figure 5
Mode 2 of the proposed RBBC.In a similar way, Mode 3 shows the well-known inverting Buck-Boost converter shown in the Figure6. M1 is PWM-switched and an alternating voltage E is supplied to the RLC branch at high frequency when a voltage vR<0 is needed. Analogous modeling procedure allows obtaining the same state space representation (6) where u(t) now represents(9)u~u~-1=ut<0 with u~ as the duty-cycle percentage.Figure 6
Mode 3 of the proposed RBBC.By considering smooth transitions (allowing discharge ofL) between modes, the resulting linear RBBC model is given by(10)x˙=Ax+Bu,where (11)A=01-1LC-1RC,B=0ELC,and the active mode depends on the value of u: (i)
Mode 1:0≤u≤1.(ii)
Mode 2:u>1.(iii)
Mode 3:u<0.Note that the theoretical output voltagevR in this configuration can reach any value from -∞ to ∞; however, it is well-known that in practice the voltage of Boost and Buck-Boost converters is limited due to nonideal components and also it is for the RBBC.Consider the following voltage PD control law:(12)u=k1x1+k2x2,where k1 and k2 are the proportional and derivative gains, respectively. Note that a PI or PID controller can be used instead. The closed-loop system is represented then as(13)x˙=ARx,where (14)AR=01Ek1LC-1LCEk2LC-1RC.In the following analysis, model (13) is addressed as nominal, because in this work the overall model’s parameters are considered time-varying values. Using parametric ranges of uncertainty, a polytopic description is obtained as follows: consider that L(t)∈[L_,L¯], ∀t; that is, the inductance L(·) varies in a known range from a maximum L¯ to a minimum L_ which is inclusive. Similarly R(t)∈[R_,R¯] and C(t)∈[C_,C¯]. Then, a Linear Parameter Variant (LPV) system representation of (13) is(15)x˙=ARtx=ARθtx,where θi_≤θi(t)≤θi¯∀i∈{1,2,3,4}; that is, the matrix AR(t) is polytopic in the following sense:(16)ARt=ARθ∣∑i=14Aiθit=ARt,where (1≥θi(t)≥0∧∑i=14θi(t)=1)∀t and θ∈R4 or equivalently(17)ARθ=θ101a21_a22_+θ201a21_a22¯+θ301a21¯a22_+θ401a21¯a22¯,where a21_ and a22_ represent the minimum values of the matrix entries for all t; in a similar way, a21¯ and a22¯ represent the maximum possible values of the matrix entries for all t. That is,(18)a21_=E_k1-1L¯C¯,a21¯=E¯k1-1L_C_,a22_=E_k2L¯C¯-1R_C_,a22¯=E¯k2L_C_-1R¯C¯.


## 3. Component Selection

The converter components selection depends on application specifications as maximum voltage or current ripple, input voltage, and load current among others. In this work, an insight into their selection is presented and depends on the maximum inductor current ripple, switching frequency, source voltage, and output voltage [9]. Three inductor values are obtained, one for each mode, and the highest one is selected as the minimum inductance value required for a ripple specification; that is, the worst-case scenario is used to obtain a single inductor value:(19)L_=1fswΔILmaxvO,1Λ1,EΛ2,EΛ3,where (20)Λ1=1-vO,1E.Λ2=1-EvO,2,Λ3=vO,3vO,2-Efsw is the switching frequency, vO,1 is a nominal output voltage value in Mode 1, vO,2 is a nominal maximum output voltage value, vO,3<0 is a nominal minimum output voltage value, and ΔIL is the maximum desired current ripple. Using the same method, saturation and maximum supported current of the inductor can be selected.Semiconductor manufacturers recommend using low ESR capacitors to minimize the ripple on the output voltage, and the minimum value ofC is selected from the maximum of three values; that is, a worst-case C capacitance value is selected:(21)C_=iR,maxfswΔVRmaxΛ1,Λ2,Λ3,where iR,max is the peak load current demand and ΔVR is the desired load voltage maximum ripple.


## 4. Stability Analysis

The control objective is to design a controller for the RBBC, such that stability of the trajectories of system (15) is ensured for parametric variation within specified design ranges.Without loss of generality, the origin is considered the equilibrium point; note that a variable change calculated from an operating point can be performed in order to achieve it. Stability of a polytopic system can be ensured by the following result.Proposition 1 (see [42]).
Quadratic stability of system (15) is equivalent to the existence of P∈R4×4 symmetric, positive definite matrix satisfying(22)PAR,i+AR,iTP≺0,∀i=1⋯4,where AR,i denotes the ith vertex and ≺0 denotes a negative definite matrix.In other words, it is enough to prove that all of the systems built with each vertex (in the following, vertex is used to identify the system built with theith vertex) are stable using a common Lyapunov function (CLF) to ensure that the polytopic system is quadratically stable even under arbitrarily fast parameter variation. Consider the CLF candidate:(23)V=xTPx=xTc20012x=c2x12+12x22 with c>0. The time derivative along the trajectories of each vertex has the form(24)V˙=c+Ek1LC-1LCx1x2+Ek2LC-1RCx22,V˙<0, if (25)c+Ek1LC-1LC=0,Ek2LC-1RC<0and from the previous equality, with k1<0, (26)c=1LC-Ek1LC>0which reduces to(27)k1<1E.From the inequality in (25) a second condition over k2 is obtained:(28)k2<LE.Since closed-loop involves a negative feedback for any vertex (k1<0, k2<0), it is easy to determine that AR,i is Hurwitz for all i, and the stability under arbitrarily fast parameter variations (within bounded ranges) is ensured.


## 5. Simulations

In this section, representative simulations of the RBBC are presented. Simulations are performed in PSIM with a switching frequency of 10 kHz and an integration time of 1μs. Power source voltage of 10 V is used and the maximum duty cycle is established in 85% for M2 and M3; nominal values of components are R=50 Ω, L=10 μH, and C=100 μF with variation ranges for controller design of ±20%, inductor parasitic resistance of 0.01 Ω, MOSFET diode threshold voltage of 0.65 V, MOSFET on resistance of 0.2 Ω, MOSFET diode resistance of 0.1 Ω, and SCR are used as switches with voltage drop, holding current and latching current of 0.1 V and 0.1 A, respectively. In order to show robustness, changes of R from 40 Ω to 60 Ω (squared function) are alternated at 20 Hz. In Figure 7 a comparison of the output voltage vR versus a sinusoidal reference is presented; note that the output voltage follows the reference with a fast response. The different colors represent the different operating modes: intersection of Vr with the blue color represents the Boost configuration (Mode 2), intersection of Vr with the purple color represents the Buck configuration (Mode 1), and intersection of Vr with the yellow color represents the Buck-Boost configuration (Mode 3). In this simulation hard switching between modes is used intentionally (without dead time or synchronization) in order to show the robustness of the controller. Note also that controller gains can be programmed differently for each mode in order to improve a particular desired response.Figure 7
Sine reference response.In order to show the benefits of the proposed control strategy, in Figure8 a representative comparison of the dynamical behavior of the converter during parameter abrupt changes in the load resistance and in the setpoint is presented, between the proposed robust controller and a sliding mode controller. While in sliding mode a high overshoot is presented during setpoint changes; with the proposed controller this overshoot can be avoided by proper gain selection and even can be tuned intuitively; in sliding mode avoiding overshoots may imply the use of additional circuitry.Figure 8
Sliding mode versus robust PD comparison for an abrupt load change.


## 6. Experimental Results

In this section some of the relevant experimental results obtained by the implementation of the RBBC are presented.Figure9 shows the implemented circuit. A simple double pole double throw is used for the switches. The robust control law and PWM generator are implemented in a cheap PIC16 with analog to digital converter and PWM generator. Trigger outputs are optically isolated from the converter and a voltage source (E) of 25 V is used. Different load capacities are used and the controller gains fulfill the Section 4 conditions.Figure 9
Experimental work bench.In Figure10 the circuit output voltage is presented in red; load current is calculated by the voltage in 0.5 Ω shown in yellow. For a regulated voltage (setpoint) of 12 V, an abrupt change in load shows a higher current step calculated in 0.4 A and with a minimal voltage variation minor to 0.1 V.Figure 10
Buck mode parameter change response in closed-loop.In Figure11 the circuit output voltage is presented in red; due to high voltage, a load resistance of a higher value is used (2 kΩ) for a regulated voltage (setpoint) of 70 V; an abrupt change in load shows a higher current step calculated in 0.22 A and with a minimal voltage variation.Figure 11
Boost mode parameter change response in closed-loop.


## 7. Discussion

The simulations and experimental data shown in the previous sections allow confirming that the proposed reconfigurable topology has benefit for a wide range of applications, such as vehicular one since the reversible power flow is possible with a simple reconfiguration. A new unified modeling technique is proposed and allows the use of a wide range of control techniques, even those that do not consider the switching reconfiguration characteristic of the RBBC; that is, the unified model is valid for a Buck, Boost, and Buck-Boost converter or a reconfigurable combination. The simulations and experimental data shown in the previous sections allow validating the analytic results for modeling, controller design, and stability.While other control techniques, as sliding mode, are beneficial for implementations, where the high overshoot, no-adjustment, and settling time are not a critic issue, the proposed control strategy allows performing a fine tuning, even for the nonexpert. That is, sliding mode and other control techniques have large benefits; however, they are very sensitive to large changes in the parameters. In contrast, the presented control strategy stabilizes the voltage output even when abrupt changes on the parameters occur, as long as they vary within the design bounds. Even more, since voltage feedback is used the implementation cost is very low.


## 8. Conclusions

In this work, a new reconfigurable converter (RBBC) is presented. The reconfigurable converter has three operating modes/configurations, Buck, Boost, and Buck-Boost that are possible with only two MOSFETs which implies that the implementation cost is very low. In this reconfigurable converter, the output voltage can vary within a wide range from negative to high positive values (Boost) and the reconfiguration can be done on the fly. In view of the above, the presented reconfigurable converter can be used in a wide range of applications, for example, in electric propulsion/traction applications where forward and reverse direction are required.A dynamical model for the reconfigurable converter is obtained in a unified sense for the Buck, Boost, and Buck-Boost configurations. That is, the dynamical model structure is the same and the control inputu defines the smooth reconfiguration and the output level. Thus, the reconfigurable converter and the dynamical model can be used with a wide range of different control techniques. Even more, the model can be used for single configurations or a combination of them, for example, a reconfigurable Buck and Boost converter (without the Buck-Boost).Moreover, in this work the methodology for the design of a robust controller for the reconfigurable converter is presented. The closed-loop stability is demonstrated by using a polytopic model and a common Lyapunov function and provides several advantages as simplicity, low implementation cost by voltage feedback, and adjustable gains. Comparative results are provided in order to illustrate the dynamical behavior against changes in parameters as capacitance, inductance, load resistance, and input voltage, with respect to a sliding mode controller.



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*Source: 6251787-2018-03-05.xml*