Open Access
This article is

- freely available
- re-usable

*Energies*
**2012**,
*5*(9),
3573-3585;
doi:10.3390/en5093573

Article

Performance Analysis and Optimization of a Solar Powered Stirling Engine with Heat Transfer Considerations

^{1}

Department of Aeronautics and Astronautics, National Cheng Kung University, No.1, University Road, Tainan City 70101, Taiwan

^{2}

Department of Electrical Engineering, National Chin-Yi University of Technology, No. 57, Sec. 2, Zhongshan Rd., Taiping Dist., Taichung City 41170, Taiwan

^{*}

Author to whom correspondence should be addressed.

Received: 23 July 2012; in revised form: 13 August 2012 / Accepted: 4 September 2012 / Published: 17 September 2012

## Abstract

**:**

This paper investigates the optimization of the performance of a solar powered Stirling engine based on finite-time thermodynamics. Heat transference in the heat exchangers between a concentrating solar collector and the Stirling engine is studied. The irreversibility of a Stirling engine is considered with the heat transfer following Newton's law. The power generated by a Stirling engine is used as an objective function for maximum power output design with the concentrating solar collector temperature and the engine thermal efficiency as the optimization parameters. The maximum output power of engine and its corresponding system parameters are determined using a genetic algorithm.

Keywords:

heat transfer; irreversibility; optimization; maximum power output; genetic algorithms; Stirling engine## 1. Introduction

Classical thermodynamics, a field that concerns thermal equilibrium problems, involves the performance indices of a time-invariant system. These include, for example, efficiency, delivered power, and similar factors, for a quasi-static thermodynamic process. As an extension and generalization of classical thermodynamics, the finite-time thermodynamics, which takes time into account, can be used to describe the dynamics of energy and entropy flow in a non-equilibrium system. Taking into consideration time-invariant quantities, such as power, refrigeration rate, power density, entropy production rate, and others, finite-time thermodynamics is effectively adopted to optimize the performance of practical systems. It has been successfully utilized in a wide range of disciplines, an important of which is the optimization of practical performance of thermodynamic cycles, such as the Carnot cycle, the Otto cycle, the Diesel cycle, the Brayton cycle, the Stirling cycle, and others.

In 1957, Novikov [1] was the first pioneer in the field of finite-time thermodynamics, and Curzon and Ahlborn [2] proposed a more adequate thermal efficiency analysis for practical thermal processes, where the upper bound on the thermal efficiency was modified accordingly by considering the loss due to thermal resistance. Ondrechen et al. [3] performed a thermal analysis of a heat source of finite extent. In 1985, DeVos [4] extended the scope of finite-time thermodynamics using various heat transfer laws.

In 1991, Angulo-Brown [5] introduced an ecological optimization criterion as an objective function to optimize the performance of a heat engine, taking into account the maximum output power and the rate of production of entropy. [5] showed that the production rate of entropy is greatly reduced by costing part of output power, when the optimum thermal efficiency is approximated as the average of the respective efficiency suggested by Carnot and that suggested by Curzon and Ahlborn [2]. In 1991, Ibrahim et al. [6] considered irreversible parameters - the isentropic ratio of the isothermal processes and thus optimized the Carnot cycle by a more practical manner. Based on the assumption that the temperature of a gas varies linearly with the temperature of the surface of the wall of the cylinder that contains it, Klein [7] proposed the net output power and an optimized compression ratio for designing an engine with the greatest possible power output. Wu and Kiang [8] performed a finite heat transfer analysis to investigate the effects of a nonisentropic compression process, expansion process, turbine efficiency and compressor efficiency and a heat exchanger on the output power optimization. In 1993, Chen and Yan [9] evaluated the maximum output power with the consideration of the irreversible factors, which are heat leakage, finite heat transfer between the heat reservoir and the heat engine in the compression and expansion processes. In 1995, Ait-Ali [10] considered the range of operating temperatures to optimize the output power of an endoreversible Carnot engine. Angulo-Brown et al. [11] used the Clausius inequality to modify the parameters as well as a linear time-temperature relationship, and took into account the power loss, to obtain analytic solutions for both the output power and the thermal efficiency. In 1998, Chen et al. [12] noted that in an Atkinson cycle, the thermal efficiency at the point of maximum power density is always better than that at the point of maximum power. Chen et al. [13] also investigated the effect of heat transfer on an Otto cycle. In 1999, [14] proposed a generalized Otto cycle and quantified the degree of irreversibility in a study of performance optimization in various heat transfer modes. Lin et al. [15] also represented an effective method for improving heat engine performance in practical operation for a dual combustion cycle using the finite-time thermodynamics approach. In 2004, Hou [16] examined the effect of heat transfer on a dual combustion cycle. Zhou et al. [17] studied the effect of a generalized heat transfer law on the optimization of power output of a generalized Carnot engine with internal and external irreversibility. In 2007, Hou [18] proved that the expansion ratio in an Atkinson cycle exceeds the compressive ratio in an Otto cycle. In 2009, Lu et al. [19] applied the energy equilibrium equation for a collecting plate to optimize a solar power generating system, in which the efficiency of the light collection unit of the solar concentrator was optimized at such operating temperature corresponding to the working fluid temperature.

The finite-time thermodynamics, as its name indicates, applies in many range of fields, whenever heat transfer occurs in a device or a system of finite extent or within a limited period. Under some suitable assumptions, this work proposes a constrained model to optimize the performance of a practical heat engines with irreversible thermodynamic process. In finite-time thermodynamics, the optimization of performance indices involves the optimization of an overall system on the assumption of irreversibility. Comparing with the classical thermodynamics, it is more adequate when applied to practical applications, and is useful in studies of the best use of energy.

This paper investigates the maximum power output design problem for a solar powered Stirling engine, where the thermal efficiency and solar collector temperature are considered as the design parameters. The heat transfer between the solar collector to the engine and the surroundings is studied such that the result can provide an adequate prediction for overall system thermal efficiency in practice.

## 2. Maximum Power Analysis of Stirling Engine with Solar Collector

The thermal model for a Stirling engine with solar collector which mainly consists of a spherical reflector and an absorber that acts as a heat source is shown in Figure 1 [20]. A collector, which is connected to an expansion chamber of the heat engine, is directly heated, and the heat is released to the ambient by radiation and natural convection as the surface temperature of the collector is increased.

Considering the heat loss on the collector surface and from the law of conservation of energy, it yields:

$$\omega {I}_{sun}{A}_{c}-{h}_{n}({T}_{w}-{T}_{s}){A}_{c}-\epsilon \sigma ({T}_{w}^{4}-{T}_{s}^{4}){A}_{c}={q}_{in}$$

The heat absorption efficiency on the collector surface is defined as:

$${\eta}_{collector}\equiv \frac{{q}_{in}}{{I}_{sun}\times {A}_{c}}$$

In this model, heat is transferred to the expansion chamber, where a high conductive coefficient and extremely thin surface of the collector is applied such that the temperature on the interior surface of the expansion chamber is almost equal to that in the collector. The working fluid is considered as the ideal gas and the heat transfer process follows Newton’s linear heat transfer law. In each cycle, Q
and the heat released by the Stirling engine to the ambient is given by:
where t

_{in}is the heat absorbed by the working fluid, and Q_{out}is the heat released to the ambient. The temperature of the corrector is denoted as T_{w}and the ambient temperature is denoted as T_{s}. The heat from the collector to the Stirling engine satisfies:
Q

_{in}= α_{2}(T_{w}− T_{3})t_{34}= h_{f}A_{c}(T_{w}− T_{3})t_{34}
Q

_{out}= α_{1}(T_{1}− T_{s})t_{12}_{12}and t_{34}are the times required for engine heat rejection and engine heat accumulation, respectively. T_{1}and T_{3}are the temperature of the working fluid in the isothermal heat rejection and addition process, respectively.In the isothermal and endothermic process, the entropy terms in the thermodynamic relation yield:

$$TdS=T{\left(\frac{dP}{dT}\right)}_{v}dV$$

The ideal gas equation is:

PV = nRT

Substituting Equation (6) into Equation (5) yields:

$$TdS=\frac{nRT}{V}dV$$

Integrating Equation (7) over states 3 and 4 yields:

$$\underset{3}{\overset{4}{\int}}TdS=\underset{3}{\overset{4}{\int}}\frac{nRT}{V}dV$$

Entropy is defined as:

$$S\equiv {\left(\frac{\delta Q}{T}\right)}_{\mathrm{int},rev}$$

Substituting Equation (9) into Equation (8) yields:

$${Q}_{34}={Q}_{in}=nR{T}_{3}\mathrm{ln}\frac{{V}_{4}}{{V}_{3}}$$

In each cycle, the incremental entropy in the working fluid inside a Stirling engine is given by:

$$\Delta S={\displaystyle \oint \frac{\delta Q}{T}}+{S}_{gen}$$

Since entropy behaves analogously to heat, it is independent of the integration path itself. Therefore, the net change in entropy between the initial and final states of a complete cycle is identically zero:

$$\Delta S={\displaystyle \oint \frac{\delta Q}{T}}+{S}_{gen}=\frac{{Q}_{in}}{{T}_{3}}-\frac{{Q}_{out}}{{T}_{1}}+{S}_{gen}=0$$

From the Second Law of thermodynamics:

$${S}_{gen}\ge 0$$

The Clausius inequality yields:

$$\oint \frac{\delta Q}{T}}\le 0$$

From Equations (12) to (14):

$$\frac{{Q}_{in}}{{T}_{3}}-\frac{{Q}_{out}}{{T}_{1}}\le 0$$

Now, let:
where ϕ is an irreversible property of a Stirling engine, such as thermal resistance, friction, heat loss. Consistent with the second law of thermodynamics, such irreversible factors, which cannot be ignored, bring about an increase in entropy in each cycle. Given an identical amount of heat transfer Q

$$\frac{{Q}_{in}}{{T}_{3}}=\frac{{Q}_{out}}{\varphi {T}_{1}},\text{}\varphi \ge 1$$

_{in}, for an endoreversible heat engine ϕ > 1, Q_{out}is expressed as:
$$\frac{{Q}_{in}}{{T}_{3}}-\frac{{Q}_{out}^{rev}}{{T}_{1}}=0$$

Relating Equation (16) to (17) yields:

$${Q}_{out}=\varphi \times {Q}_{out}^{rev}$$

In a Stirling engine, the heat that is released to low-temperature thermal storage (cold chamber) in a reversible isothermal process is:

$${Q}_{out}^{rev}=nR{T}_{1}\mathrm{ln}\frac{{V}_{1}}{{V}_{2}}$$

Back-substituting Equation (19) into Equation (18) yields:

$${Q}_{out}=\varphi nR{T}_{1}\mathrm{ln}\frac{{V}_{1}}{{V}_{2}}$$

Let compressive ratio r

_{v}be defined as:
$${r}_{v}\equiv \frac{{V}_{4}}{{V}_{3}}=\frac{{V}_{1}}{{V}_{2}}$$

Equating Equation (3) with Equation (10) and substituting Equation (21) into Equation (3) yields:

h

_{f}A_{c}(T_{w}− T_{3})t_{34}= nRT_{3}lnr_{v}The endothermic time of the heat engine is given by:

$${t}_{34}=\frac{nR{T}_{3}\mathrm{ln}{r}_{v}}{{h}_{f}{A}_{c}\left({T}_{w}-{T}_{3}\right)}$$

Equating Equation (4) with Equation (20) and substituting Equation (21) into Equation (4) yields:

α(T

_{1}− T_{s})t_{12}= ϕnRT_{1}ln r_{v}The time for which the heat engine is exothermic is:

$${t}_{12}=\frac{\varphi nR{T}_{1}\mathrm{ln}{r}_{v}}{{\alpha}_{1}\left({T}_{1}-{T}_{s}\right)}$$

Suppose that in the heat regenerating process, the temperature of the working fluid, T
where K

_{fluid}, varies linearly with time:
$$\frac{d{T}_{fluid}}{dt}=\pm {K}_{1}$$

_{1}> 0, which is the average rate of change of temperature, and is independent of time but dependent on the material of the heat regenerator, is called the heat regenerative time coefficient: a positive or negative sign shows that the temperature increases or decreases with time, respectively.The duration of the heat regenerative process from state 2 to state 3 is:

$${t}_{23}=\frac{\left({T}_{3}-{T}_{2}\right)}{{K}_{1}}$$

Similarly, that of the heat regenerative process from state 4 to state 1 is:

$${t}_{41}=\frac{\left({T}_{4}-{T}_{1}\right)}{{K}_{1}}$$

Accordingly, time for a complete Stirling cycle is represented as:

t

_{c}= t_{12}+ t_{23}+ t_{34}+ t_{41}Substituting Equations (23), (25), (27) and (28) into Equation (29) yields:

$${t}_{c}=\frac{\varphi nR{T}_{1}\mathrm{ln}{r}_{v}}{{\alpha}_{1}\left({T}_{1}-{T}_{s}\right)}+\frac{\left({T}_{3}-{T}_{2}\right)}{{K}_{1}}+\frac{nR{T}_{3}\mathrm{ln}{r}_{v}}{{h}_{f}{A}_{c}\left({T}_{w}-{T}_{3}\right)}+\frac{\left({T}_{4}-{T}_{1}\right)}{{K}_{1}}$$

In each cycle, the effective energy in a collector is:

Q

_{in}= q_{in}× t_{c}Substituting Equations (10), (21) and (30) into Equation (31) yields the total amount of heat applied to a Stirling engine in each cycle, which is:

$${q}_{in}=\frac{{h}_{f}}{\frac{1}{{A}_{c}({T}_{w}-{T}_{3})}+\frac{{h}_{f}\varphi {T}_{1}}{{\alpha}_{1}{T}_{3}\left({T}_{1}-{T}_{s}\right)}+\frac{2{h}_{f}({T}_{3}-{T}_{1})}{nR{T}_{3}\mathrm{ln}{r}_{v}{K}_{1}}}$$

The thermal efficiency of a heat engine is defined as:

$${\eta}_{Strling}\equiv \frac{{P}_{stirling}}{{Q}_{in}}=\frac{{Q}_{in}-{Q}_{out}}{{Q}_{in}}=1-\frac{{T}_{1}}{{T}_{3}}\varphi $$

Substituting $\delta =\sqrt{\frac{{h}_{f}}{{\alpha}_{1}}}$ and $K=\sqrt{\frac{2{h}_{f}}{nR{K}_{1}}}$ into Equation (32) yields:

$${q}_{in}=\frac{{h}_{f}}{\frac{1}{{A}_{c}({T}_{w}-{T}_{3})}+\frac{{\delta}^{2}(1-{\eta}_{Stirling})}{\left[\frac{(1-{\eta}_{Stirling}){T}_{3}}{\varphi}-{T}_{s}\right]}+\frac{K}{\mathrm{ln}{r}_{v}}\left[1-\frac{(1-{\eta}_{Stirling})}{\varphi}\right]}.$$

The heat that is released to the ambient in a Stirling cycle is given by:

$${q}_{out}=\frac{{Q}_{out}}{{t}_{c}}$$

Substituting Equations (20), (30) and (33) into Equation (35) yield:

$${q}_{in}=\frac{{h}_{f}(1-{\eta}_{Stirling})}{\frac{1}{{A}_{c}({T}_{w}-{T}_{3})}+\frac{{\delta}^{2}(1-{\eta}_{Stirling})}{\left[\frac{(1-{\eta}_{Stirling}){T}_{3}}{\varphi}-{T}_{s}\right]}+\frac{K}{\mathrm{ln}{r}_{v}}\left[1-\frac{(1-{\eta}_{Stirling})}{\varphi}\right]}$$

The output power that is provided by a Stirling engine in a Stirling cycle is:

P

_{Stirling}= η_{Stirling}× q_{in}From the collector temperature and the thermal efficiency, the amount of heat that is applied to the collector is determined using Equation (11); then, Equation (34) is solved for the endothermic temperature of the heat engine, which is expressed in a quadratic form as:
where:

$${T}_{3}=\frac{-b\pm \sqrt{{b}^{2}-4ac}}{2a}=f({T}_{w},{\eta}_{Stirling})$$

$$a=\frac{s{A}_{c}(1-{\eta}_{Stirling})}{\varphi}$$

$$b=\frac{(1-{\eta}_{Stirling})}{\varphi}-{\delta}^{2}{A}_{c}(1-{\eta}_{Stirling})-\frac{s{A}_{c}{T}_{w}(1-{\eta}_{Stirling})}{\varphi}-s{A}_{c}{T}_{s}$$

c = −T

_{s}+ A_{c}δ^{2}(1 − η_{Stiring})T_{w}+ sA_{c}T_{w}T_{s}In the above three parameters, the parameter

**s**is defined as:
$$s=\frac{{h}_{f}}{{q}_{in}}-\frac{K}{\mathrm{ln}{r}_{v}}\left[1-\frac{(1-{\eta}_{Stirling})}{\varphi}\right]$$

From Equation (33), the rejection temperature of the heat engine is:

$${T}_{1}=\frac{(1-{\eta}_{Stirling}){T}_{3}}{\varphi}$$

Given the collector temperature, the heat transferred from the collector to the heat engine is determined. Partial differentiation of Equation (34) with respect to endothermic temperature yields the optimized endothermic temperature:

$$\frac{\partial {q}_{in}}{\partial {T}_{3}}=0$$

$${T}_{3.opt}=\frac{\sqrt{\varphi}\delta {T}_{w}(1-{\eta}_{Stirling})+\varphi {T}_{s}}{(1-{\eta}_{Stirling})(1+\sqrt{\varphi}\delta )}$$

Back-substituting Equation (41) into Equation (34) yields the amount of heat applied at the optimal endothermic temperature:

$${q}_{in,opt}=\frac{{h}_{f}}{\frac{1}{{A}_{c}({T}_{w}-{T}_{3,opt})}+\frac{{\delta}^{2}(1-{\eta}_{Stirling})}{\left[\frac{(1-{\eta}_{Stirling}){T}_{3,opt}}{\varphi}-{T}_{s}\right]}+\frac{K}{\mathrm{ln}{r}_{v}}\left[1-\frac{(1-{\eta}_{Stirling})}{\varphi}\right]}.$$

## 3. Results and Discussion

For a given solar intensity, the relation between the thermal efficiency of a Stirling engine and the collector temperature are studied in this section. Thermal efficiency of an engine can be improved by either increasingg T

_{3}of the isothermal heat addition process, or reducing T_{1}of the isothermal heat rejection process. In general, the heat rejection temperature will not fall below the ambient temperature, so the intended thermal efficiency can only be improved by elevating T_{3}. Since the collector receives limited energy for a given solar intensity and it loses heat to the surroundings by both radiation and convection, a temperature upper bound will exist for the collector as well as the T_{3}of the thermal process. Also, the temperature difference between them will determine the heat been accumulated by the engine from the collector. In this study, a solar powered Stirling engine with the solar intensity = 4000 W/m^{2}is considered with system parameters listed in Table 1.Equation (1) is used to determine the heat loss from the collector to the surroundings which can be used to determine a reasonable heat available for the engine. Figure 2 reveals the heat loss by the collector with respect to collector temperature. When the collector temperature exceeds 698 K, the heat loss from the collector exceeds the amount of solar power can possibly been accumulated.

System Parameters | Values |
---|---|

Solar intensity | I_{sun} = 4000 W/m^{2} |

The upper bound of thermal efficiency | 0.57 |

The temperature of collector | 450–698 K |

The coefficient of convection in the expansion chamber | h_{f} = 90 W/(m^{2}·K) |

The coefficient of natural convection | h_{n} = 5 W/(m^{2}·K) |

The product of heat transfer coefficient and heat transfer area between cold-end chamber to the surroundings | α_{1} = 50 W/K |

Surface radiation emission rate | ε = 0.12 |

Boltzmann constant | σ = 5.67 × 10^{−8} W/(m^{2}·K^{4}) |

Collector wall absorption rate | ω = 0.9 |

Degree of irreversible factor in heat engine | ϕ = 1 |

Ambient temperature | T_{s} = 293 K |

Collector area | A_{c} = 1 m^{2} |

Figure 3 plots the output power as a function of the collector temperature at thermal efficiencies of 0.1, 0.3 and 0.5. Figure 4 illustrates available heat for the engine for different isothermal heat addition process temperature T

_{3}. The maximum power available according to the optimal hot-end temperature determined by Equation (41) is also indicated in Figure 4. Accordingly, the output power generated by the engine is shown in Figure 5. Figure 3, Figure 4 and Figure 5 reveal that a higher T_{3}will result higher thermal efficiency; however, it will also reduce the heat power been accumulated from the collector. Therefore, the maximum power output of the engine requires a trade-off between thermal efficiency and isothermal heat addition process temperature of the thermal process. Figure 6 and Figure 7 illustrate the maximum output power of the engine with respect to thermal efficiency and collector temperature, respectively. They show that the solar powered Stirling engine will generate maximum power at a thermal efficiency of between 0.3 and 0.4 and a collector temperature of between 550 K and 600 K.System Parameters | Values |
---|---|

Solar intensity (P_{solar}) | 4000 W/m^{2} |

Collector wall absorption rate | 0.9 |

Power accumulated by collector | 3600 W/m^{2} |

Collector temperature | 560.4 K |

Radiation heat loss | 621 W/m^{2} |

Convection heat loss | 1337 W/m^{2} |

Collector efficiency | 0.41 |

The input power of heat engine | 1642 W |

Thermal efficiency | 0.363 |

The temperature of the working fluid in the isothermal heat addition process (T_{3}) | 517.4 K |

The temperature of the working fluid in the isothermal heat rejection process (T_{1}) | 329.7 K |

The output heat of heat engine | 1047 W |

The power generated by the heat engine (P_{Stirling}) | 596 W |

The total power loss of the system | 3404 W/m^{2} |

Overall system thermal efficiency (P_{Stirling}/P_{solar}) | 0.149 |

Finally, the optimum design parameters are determined using a genetic algorithm. The maximum output power of a Stirling engine and the corresponding parameters are determined using the Matlab Toolbox Genetic Algorithm Toolbox, with the output power as an objective function, and the thermal efficiency and the collector temperature as optimized parameters. As shown in Table 2, the simulation yields a maximum output power of 596 W at a thermal efficiency of 0.363 and a collector temperature of 560.4 K, which also confirms the expecting result from Figure 6 and Figure 7.

## 4. Conclusions

This work adopts finite-time thermodynamics to optimize the performance of a solar powered Stirling engine. The genetic algorithm is used to reveal the maximum output power of a Stirling engine by determining the thermal efficiency, the collector temperature, and their corresponding values of the optimized parameters. The results of the simulation herein described can be directly applied to optimize the design of a practical solar powered Stirling engine. The proposed work investigates the maximum power output of a Stirling engine under the solar concentrated heat of 4000 W/m

^{2}. According to the optimal design, it reveals that maximum power can be generated if the engine is designed with efficiency 0.363 and temperature of collector is kept to be about 560.4 K, which can be achieved using a temperature regulating control loop.## Acknowledgments

Part of this research is financial supported by the National Science Council, Taiwan, under Grant No. NSC 100-2221-E-006-104-MY2.

## References

- Novikov, I.I. The efficiency of atomic power stations. J. Nucl. Energy II
**1958**, 7, 125–128. [Google Scholar] - Curzon, F.L.; Ahlborn, B. Efficiency of a Carnot engine at maximum power output. Am. J. Phys.
**1975**, 43, 22–24. [Google Scholar] [CrossRef] - Ondrechen, M.J.; Rubin, M.H.; Band, Y.B. The generalized Carnot cycle-A working fluid operating in finite time between finite heat source and sinks. J. Chem. Phys.
**1983**, 78, 4721–4727. [Google Scholar] [CrossRef] - De Vos, A. Efficiency of some heat engines at maximum power conditions. Am. J. Phys.
**1985**, 53, 570–573. [Google Scholar] [CrossRef] - Angulo, B.F. An ecological optimization criterion for finite time heat engines. J. Appl. Phys.
**1991**, 69, 7465–7469. [Google Scholar] [CrossRef] - Ibrahim, O.M.; Klein, S.A.; Mitchell, J.W. Optimum heat power cycles for specified boundary conditions. J. Eng. Gas Turb. Power
**1991**, 113, 514–521. [Google Scholar] [CrossRef] - Klein, S.A. An explanation for observed compression ratios in internal combustion engines. J. Eng. Gas Turb. Power
**1991**, 113, 511–513. [Google Scholar] [CrossRef] - Wu, C.; Kiang, R.L. Power performance of a nonisentropic Brayton cycle. J. Eng. Gas Turb. Power
**1991**, 113, 501–504. [Google Scholar] [CrossRef] - Chen, J.C.; Yan, Z.J. Optimal performance of endoreversible cycles for another linear heat transfer law. J. Phys. D Appl. Phys.
**1993**, 26, 1581–1586. [Google Scholar] [CrossRef] - Ait, A.M. Maximum power and thermal efficiency of an irreversible power cycle. J. Appl. Phys.
**1995**, 78, 4313–4318. [Google Scholar] [CrossRef] - Angulo, B.F.; Rocha Martinez, J.A.; Navarrete Gonzalez, T.D. A non-endoreversible Otto cycle model: Improving power output and efficiency. J. Phys. D Appl. Phys.
**1996**, 29, 80–83. [Google Scholar] [CrossRef] - Chen, L.G.; Lin, J.X.; Sun, F.R.; Wu, C.I. Efficiency of an Atkinson engine at maximum power density. Energy Convers. Manag.
**1998**, 39, 337–341. [Google Scholar] [CrossRef] - Chen, L.G.; Wu, C.; Sun, F.R.; Cao, S. Heat transfer effects on the net work output and efficiency characteristics for an air-standard Otto cycle. Energy Convers. Manag.
**1998**, 39, 643–648. [Google Scholar] [CrossRef] - Chen, L.G.; Sun, F.R.; Wu, C. Effect of heat transfer law on the performance of a generalized irreversible Carnot engine. J. Phys. D Appl. Phys.
**1999**, 32, 99–105. [Google Scholar] [CrossRef] - Lin, J.X.; Chen, L.G.; Wu, C.; Sun, F.R. Finite time thermodynamic performance of a dual cycle. Int. J. Energy Res.
**1999**, 23, 765–772. [Google Scholar] [CrossRef] - Hou, S.S. Heat transfer effects on the performance of an air standard dual cycle. Energy Convers. Manag.
**2004**, 45, 3003–3015. [Google Scholar] [CrossRef] - Zhou, S.; Chen, L.; Sun, F.; Wu, C. Optimal performance of a generalized irreversible Carnot engine. Appl. Energy
**2005**, 81, 376–387. [Google Scholar] [CrossRef] - Hou, S.S. Comparison of performances of air standard Atkinson and Otto cycles with heat transfer considerations. Energy Convers. Manag.
**2007**, 48, 1683–1690. [Google Scholar] [CrossRef] - Lu, J.; Ding, J.; Yang, J. Optimal performance for solar thermal power system. Energy Power Eng.
**2009**, 1, 110–115. [Google Scholar] [CrossRef] - Bejan, A. Advanced Engineering Thermodynamics; Wiley-Interscience: New York, NY, USA, 1997. [Google Scholar]

© 2012 by the authors; licensee MDPI, Basel, Switzerland. This article is an open access article distributed under the terms and conditions of the Creative Commons Attribution license (http://creativecommons.org/licenses/by/3.0/).