Determination of Optimized Parameters for the Flexible Operation of a Biomass-fueled, Microscale Externally Fired Gas Turbine (efgt)

Biomass as a source of renewable energy is a promising solution for current problems in energy supply. Olive waste is considered as an interesting option, especially for Mediterranean countries. Within this paper, a microscale externally fired gas turbine (EFGT) technology is presented as a decentralized power plant, within the range of 15 kW th , based on olive residues. It was modeled by Aspen Plus 8.6 software to provide a sufficient technical study for such a plant. Optimized parameters for pressure ratio and turbine air-mass flow have been mapped for several loads to provide information for process control. For all cases, mechanical output, efficiency curves, and back-work ratio have been calculated. Using this information, typical plant sizes and an example of power production are discussed. Additionally, achievable energy production from olive waste is estimated on the basis of this data. The results of this study show that such a plant has an electrical efficiency of 5%–17%. This variation is due to the examination being performed under several combustion temperatures, actual load, heat exchanger temperatures, and heat transfer efficiency. A cost estimation of the discussed system showed an estimated capital cost of 33,800 to 65,300 € for a 15 kW th system.


Introduction
Using biomass as an energy source is considered to be one of the main options to supply renewable power and heat, thus reducing carbon dioxide emissions as well as consumption of imported fuels.Especially, the use of agricultural residues and other wastes from food industry is a good option to provide bioenergy with low additional carbon dioxide emissions.Biomass is a perfect investment, especially when hybridized with other unstable sources like wind and solar energy [1].From several types of biomass, we chose olive residues for this research due to the abundant availability in Mediterranean countries.
Olive-processing residues are considered as a promising source of biomass due to the energy utilization property shown based on its characteristics [2].For 2015/2016, the worldwide production is 2,742,500 tons, produced mainly by Mediterranean countries (approximately 97%) [3,4].Olive oil-extracting technologies are mainly traditional pressing and the centrifugation method with either two-or three-phase schemes [1,5].Solid residues (rich in water) are approximately 40% from pressing, and 30%-50% and 60%-70% for three and two phases, respectively [6,7].Each olive tree can produce an average of 10-30 kg/year of pruning residues; these are mostly burned in the field with a small portion used for animals feeding [5].
The produced water contains organic acids, lipids, alcohols, and phytotoxic materials that are dangerous for the environment; however, its organic matter and nutrients make it valuable for fertilizing soil [8].Roughly, solid dry residues can be estimated at 25% of the mass of the processed olive [9], thus it can be estimated that 685,625 tons is available worldwide for 2015/2016, with 97% in Mediterranean countries.
The chemical composition of olive waste generally differs from one sample to another because it depends on several factors like olive mill processing pressure and temperature, but also olive type, soil, and growing conditions.When the process is handled in normal conditions, the fat percentage is between 8% and 16%; the nucleus presence is approximately 40%, which is rich in minerals like calcium and copper, and has a high percentage (up to 40%) of fibers [10].The variability in the chemical composition of olive waste for two prototype samples, a Spanish and a Jordanian sample, is shown in Table 1.However, the effect of sample composition on electrical efficiency and plant operation will be investigated in a future study.For the present study, the Aspen modeling calculations were performed with the Jordanian sample.A noticeable difference is clear in fixed carbon and ash contents, in addition to the relatively high values for higher heating value (HHV).The most common thermochemical energy conversion processes used to convert solid biomass combined heat and power are direct combustion, pyrolysis, and gasification of biomass [12].To achieve electricity from a combustion process, it is necessary to select a suitable power plant technology that meets biomass distribution due and countries' conditions.For these reasons, small power plants are more practical than large ones, especially when concerned with developing distributed generation concepts.
Typical combined heat and power technologies in the range below 1 MW el are Stirling engines, steam engines, microgas turbines, gas engines (combined with gasification), or fuel cells.For solid fuels, the most suitable systems are based on combustion in combination with Stirling and steam engines, or with organic Rankine cycle (ORC) turbine technology [13].Another suitable system is the so-called externally fired gas turbine (EFGT) as shown in Figure 1, while gasification processes could also be used, as discussed in other research such as that conducted by Link et al. [14].Being able to process a wide variety of fuels, including those with suboptimal combustion properties, EFGT is considered to be a promising option for small-to medium-scale plant sizes [15,16].The literature shows that technical and economic studies have been done for plants in the range of 30-100 kWel, mainly for microscale.Typically, the discussion is about the use of EFGT in heat recovery, dealing with high-temperature heat exchangers, and thermal analysis for either biomass direct combustion or gasification [15][16][17][18][19][20][21][22].Such technology has some advantages over the other systems; for example, greater flexibility in fuel type and lower cleaning and maintenance costs when compared with internal combustion gas turbines [23,24].Additionally, there is no need for water as a medium or for cooling in the condenser, which can be an advantage in arid regions [19].There is no liquid working medium, as in steam turbines or engines; therefore, the startup, shutdown, and transient period of EFGT systems are mainly limited by the combustion process itself since the turbine has a relatively fast response [25,26].Systems based on gasification (e.g., in combination with gas engines or fuel cells), as discussed in the past [27,28], are not considered within this study.This is because such existing systems are mostly designed for woody fuels and there are still unresolved questions regarding gas cleaning of the gas produced from agricultural residues like olive waste.Additionally, a comparison between EFGT and a gasification-based gas turbine system has been published for a 30 kWel plant fueled by olive tree leaves and prunings [29].
Typical electrical efficiencies for systems like ORC and EFGT are in the range of 10%-20%.Although higher efficiencies of 25% for EFGT have been reported [30], for the relevant size within this study, we expect an electrical efficiency below 20% [13,15,22,30].Actually, there is no exact definition for EFGT classes with respect to the plant size, so we defined microscale, based on other researches, as being up to 200 kWel [31][32][33][34].An overview of existing research on EFGT is given in Table 2.  Being able to process a wide variety of fuels, including those with suboptimal combustion properties, EFGT is considered to be a promising option for small-to medium-scale plant sizes [15,16].The literature shows that technical and economic studies have been done for plants in the range of 30-100 kW el , mainly for microscale.Typically, the discussion is about the use of EFGT in heat recovery, dealing with high-temperature heat exchangers, and thermal analysis for either biomass direct combustion or gasification [15][16][17][18][19][20][21][22].Such technology has some advantages over the other systems; for example, greater flexibility in fuel type and lower cleaning and maintenance costs when compared with internal combustion gas turbines [23,24].Additionally, there is no need for water as a medium or for cooling in the condenser, which can be an advantage in arid regions [19].There is no liquid working medium, as in steam turbines or engines; therefore, the startup, shutdown, and transient period of EFGT systems are mainly limited by the combustion process itself since the turbine has a relatively fast response [25,26].Systems based on gasification (e.g., in combination with gas engines or fuel cells), as discussed in the past [27,28], are not considered within this study.This is because such existing systems are mostly designed for woody fuels and there are still unresolved questions regarding gas cleaning of the gas produced from agricultural residues like olive waste.Additionally, a comparison between EFGT and a gasification-based gas turbine system has been published for a 30 kW el plant fueled by olive tree leaves and prunings [29].
Typical electrical efficiencies for systems like ORC and EFGT are in the range of 10%-20%.Although higher efficiencies of 25% for EFGT have been reported [30], for the relevant size within this study, we expect an electrical efficiency below 20% [13,15,22,30].Actually, there is no exact definition for EFGT classes with respect to the plant size, so we defined microscale, based on other researches, as being up to 200 kW el [31][32][33][34].An overview of existing research on EFGT is given in Table 2.For analyzing the thermal operation of the gas turbine, Joule-Thomson or (as in other references) Brayton cycles are the best and ideal selections for calculating the efficiency of the gas turbine [40], since the working fluid (air) is compressed and then expanded by the operation of the gas turbine after heat addition from the combustion process.
Turbines are generally defined as rotating machines dependent on the flow of liquid or gas materials at a certain pressure and temperature, resulting in rotation of a connected shaft with an electrical generator.The ideal thermal efficiency by the means of temperature or pressure is given by Equation (1) (see also [41]): The heat exchanger (HE) is a key component in an EFGT biofuel-based plant due to the high combustion temperature (combined with elevated pressure) and the aggressive behavior of the flow gases that cause oxidation, surface corrosion, and erosion [42].There are several classifications and types for the heat exchanger depending on the specific application.In this research, shell-and-tube HE was selected (as in [22,23]), since shell-and-tube type is the most suitable due to its ability to operate in high-temperature conditions, the design can withstand fouling caused by combustion, and its thermal stress reluctance [38].
In a recent study on EFGT technology based on woody biomass [43], the resultant electrical cost was found to be 0.33 euro/kWh at a utilization factor of 0.8 (7000 h/year) with an assumed power output of 60 kW el .Another study was performed on the thermoeconomics of an EFGT cycle with two firing schemes-natural gas and biomass-with the plant designed to provide 100 kW el with the possibility of adjusting percentages of energy sources (natural gas (NG) and biomass) from 0% to 100%.The capital cost was determined to be 471,000 euros with operating costs (including biomass supply, ash discharge, and maintenance) of 69,750 euro/year when the biomass quota is 100% [21].
In [44], an economic analysis of advanced and EFGT cycles was made by estimating the capital, operating, and maintenance specific costs.The specific capital cost of a power plant of 1 MW el size was calculated to be 540 £ (ca.733.5 euro) per kW el .
While previous research on power production with EFGT technology concentrated on higher nominal power, as shown in Table 2, the following study aims to evaluate the use of a very small system (15 kW th ) and provide suitable parameters for the operation of such a system.The expected efficiency values and parameter mappings for nominal operation are presented.
At the beginning of the Methodology section, the design of the proposed system is described, followed by the models for the combustion process and the thermodynamic cycle.In the Results and Discussion section, suitable parameters for an EFGT of this small size are specified for olive waste as an exemplary biomass.Finally, a cost estimation of the proposed system is given.

System Design
For the study, an EFGT has been designed on the basis of Figure 1.This includes a direct biomass combustion system, a turbine, a compressor for turbine air, and a high-temperature heat exchanger.
Considering plant size, a 15 kW th EFGT cycle is suggested in order to illustrate the idea of decentralized power generation from olive waste for the modeling part.Noting that, it is also applicable for other biomass resources, including mixtures, which could be provided internationally since the moving parts (especially the turbine) are separated from the flue gas stream by the heat exchanger.

Combustion Model
Referring to the schematic diagram in Figure 1, the complete process of the EFGT cycle is based on biomass pellets.The burning process is performed at a 15 kW th burner where the stoichiometric combustion equation (based on the composition of Jordanian sample 2 from Table 1) is calculated by Equation ( 2): For energy and mass balance calculations, the flow sheet software Aspen Plus has been used.In Aspen Plus, olive residues are considered as a nonconventional component.The combustion reaction is performed by using two reactors RYield and RGibbs as in Figure 2. RYield reactor is commonly used when the stoichiometric reaction is not known (i.e., no need to clarify the stoichiometric reaction and its kinetics).RGibbs reactor performs the chemical equilibrium by minimizing the Gibbs free-energy, and the heat-transfer balance is done by connecting a heat stream between both reactors in order to maintain the energy balance.Since olive residues are considered as a nonconventional component, RGibbs reactor is not suitable for energy calculations.As a solution, the RYield reactor is placed before RGibbs to convert olive residues to constituent elements [45].SSPLIT is used to separate ash from the total flow.The residues' component yields (mass basis) are shown in Table 3 for RYield reactor.
Energies 2016, 9, 856 5 of 15 Considering plant size, a 15 kWth EFGT cycle is suggested in order to illustrate the idea of decentralized power generation from olive waste for the modeling part.Noting that, it is also applicable for other biomass resources, including mixtures, which could be provided internationally since the moving parts (especially the turbine) are separated from the flue gas stream by the heat exchanger.

Combustion Model
Referring to the schematic diagram in Figure 1, the complete process of the EFGT cycle is based on biomass pellets.The burning process is performed at a 15 kWth burner where the stoichiometric combustion equation (based on the composition of Jordanian sample 2 from Table 1) is calculated by Equation ( 2 For energy and mass balance calculations, the flow sheet software Aspen Plus has been used.In Aspen Plus, olive residues are considered as a nonconventional component.The combustion reaction is performed by using two reactors RYield and RGibbs as in Figure 2. RYield reactor is commonly used when the stoichiometric reaction is not known (i.e., no need to clarify the stoichiometric reaction and its kinetics).RGibbs reactor performs the chemical equilibrium by minimizing the Gibbs free-energy, and the heat-transfer balance is done by connecting a heat stream between both reactors in order to maintain the energy balance.Since olive residues are considered as a nonconventional component, RGibbs reactor is not suitable for energy calculations.As a solution, the RYield reactor is placed before RGibbs to convert olive residues to constituent elements [45].SSPLIT is used to separate ash from the total flow.The residues' component yields (mass basis) are shown in Table 3 for RYield reactor.The flow gas components are performed by specifying the expected products in RGibbs reactor; the components are C (pure solid), CO 2 , N2, H 2 O, O 2 , H 2 , CO, and SO 2 .For both reactors the pressure is 1 bar.

Thermodynamic Cycle Model
Figure 2 shows the complete plant modeled by Aspen Plus 8.6.
To study the cycle behavior for different operational cases, it is necessary to have a reference case.The general parameters for the reference case are given in Table 4.Both compressor and turbine follow the isentropic operation, and the main parameters to set are pressure difference and efficiency.The temperature difference on heat exchanger terminals (HED, T CO -T HI ) will be mainly discussed a value of 20 K, while results for a difference of 100 K will also be included for comparison of cases with suboptimal heat exchanger operation (e.g., due to fouling).In literature, the values for this temperature difference are in the range of 10-150 K and 50-200 K (see Table 2) [29].It is important to notice that this study is on open-loop cycle, which means lower efficiency values are expected due to heat loss; in addition, 90% electrical generator efficiency is assumed for all calculations.The sensitivity property in Aspen is used for finding the net power output from the cycle, then assigning the pressure and air flow in the compressor where the maximum power is found.This procedure is used for parameter mapping for the maximum benefit from the plant in general, under different operational conditions.Modeling parameters are shown in Table 4.

Technical Evaluation
In comparison to the reference case with nominal operation conditions, the behavior of the cycle with variating pressures, temperatures, and mass flow parameters is evaluated in this section.Flow gas components in the exhaust streams hot stream input (HI) and hot stream output (HO) at an air-to-fuel ratio (AFR) of 20 are shown in Figure 3.After combustion, the hot flue gas (stream HI in Figure 2) has a temperature of about 1088 K.For the reference case, AFR was adapted to reach this temperature to avoid overheating of the heat exchanger.As a result, turbine inlet temperature (TIT) is limited, too.The effect of changing TIT, especially due to different flue gas temperatures, is discussed later in this study.
The results show that for the normal situation (taking parameters in Table 4), the compressor consumes around 3.2 kWm while the gas turbine delivers 4.9 kWm, resulting in 1.7 kWm generated from the whole process.The delivered power is related mainly to the pressure variation and combustion temperature.Figure 4 shows the net mechanical output power with respect to pressure variation at 0.017 / .The output power change with respect to mass flow through the compressor at p = 4 bar is given in Figure 5.After combustion, the hot flue gas (stream HI in Figure 2) has a temperature of about 1088 K.For the reference case, AFR was adapted to reach this temperature to avoid overheating of the heat exchanger.As a result, turbine inlet temperature (TIT) is limited, too.The effect of changing TIT, especially due to different flue gas temperatures, is discussed later in this study.
The results show that for the normal situation (taking parameters in Table 4), the compressor consumes around 3.2 kW m while the gas turbine delivers 4.9 kW m , resulting in 1.7 kW m generated from the whole process.The delivered power is related mainly to the pressure variation and combustion temperature.Figure 4 shows the net mechanical output power with respect to pressure variation at .m a = 0.017 kg/s .
The output power change with respect to mass flow through the compressor at p = 4 bar is given in Figure 5.
The results in Figure 4 show that the output power increases with increasing pressure until 4 bar, after which it starts to decay.This refers to high compressor consumption while the turbine starts to show a lower increase in power generation; in this case the maximum output when varying pressure is 1.7 kW m .This can be compared to Figure 5 where the maximum net power output is found at 0.017 kg/s turbine air-mass flow.
The electrical efficiency is affected by the combustion, and as a result, by the air stream temperature entering the turbine.As shown in Figure 6, lower temperature values result in lower efficiencies, noting that the variation for both efficiency and AFR is calculated for maximum power output at each turbine inlet temperature (T CO ).
Energies 2016, 9, 856 8 of 15 especially due to different flue gas temperatures, is discussed later in this study.
The results show that for the normal situation (taking parameters in Table 4), the compressor consumes around 3.2 kWm while the gas turbine delivers 4.9 kWm, resulting in 1.7 kWm generated from the whole process.The delivered power is related mainly to the pressure variation and combustion temperature.Figure 4 shows the net mechanical output power with respect to pressure variation at 0.017 / .The output power change with respect to mass flow through the compressor at p = 4 bar is given in Figure 5.The results in Figure 4 show that the output power increases with increasing pressure until 4 bar, after which it starts to decay.This refers to high compressor consumption while the turbine starts to show a lower increase in power generation; in this case the maximum output when varying pressure is 1.7 kWm.This can be compared to Figure 5 where the maximum net power output is found at 0.017 kg/s turbine air-mass flow.
The electrical efficiency is affected by the combustion, and as a result, by the air stream temperature entering the turbine.As shown in Figure 6, lower temperature values result in lower efficiencies, noting that the variation for both efficiency and AFR is calculated for maximum power output at each turbine inlet temperature (TCO).The results in Figure 4 show that the output power increases with increasing pressure until 4 bar, after which it starts to decay.This refers to high compressor consumption while the turbine starts to show a lower increase in power generation; in this case the maximum output when varying pressure is 1.7 kWm.This can be compared to Figure 5 where the maximum net power output is found at 0.017 kg/s turbine air-mass flow.
The electrical efficiency is affected by the combustion, and as a result, by the air stream temperature entering the turbine.As shown in Figure 6, lower temperature values result in lower efficiencies, noting that the variation for both efficiency and AFR is calculated for maximum power output at each turbine inlet temperature (TCO).The resulting graphs for the reference case are generated by variating one variable (p or ) at a combustion temperature of 1088 K. Figure 7 shows the output power with respect to combustion temperature for both 100% and 50% fuel consumption and at two values for HED (heat exchanger temperature difference: TCO-THI) Whereas the lower value of 20 K represents good operation, the higher value of 100 K is considered to be incomplete heat exchange (e.g., due to fouling).It is clear  The resulting graphs for the reference case are generated by variating one variable (p or . m a ) at a combustion temperature of 1088 K. Figure 7 shows the output power with respect to combustion temperature for both 100% and 50% fuel consumption and at two values for HED (heat exchanger temperature difference: T CO -T HI ) Whereas the lower value of 20 K represents good operation, the higher value of 100 K is considered to be incomplete heat exchange (e.g., due to fouling).It is clear that higher electrical output values are reachable when increasing the temperature of combustion for both cases.For the case of 100% fuel feed, the net output electrical power is around 0.5 kW el at flue gas temperature of approximately 700 K and HED of 20 K, at the same time; this value does not exceed 0.4 kW el at 100 K HED.The increase in the electrical power output seems to be fast until 1300 K, after which it slows down with closing behavior for both 20 and 100 K HED.The same explanation is applicable to 50% fuel-feed diagrams but with lower values: nearly 0.25 kW el as a starting point for 20 K HED and 0.2 kW el for 100 K HED.The electrical output power can reach 2.5 and 1 kW el at 1750 K for both 100% and 50% of fuel feed, respectively.However, the limitations in temperature values for HE and turbine should be taken into consideration.The HED has a slight effect on power output for higher temperature values, while HED effect starts to increase for lower combustion temperatures.
Energies 2016, 9, 856 9 of 15 exceed 0.4 kWel at 100 K HED.The increase in the electrical power output seems to be fast until 1300 K, after which it slows down with closing behavior for both 20 and 100 K HED.The same explanation is applicable to 50% fuel-feed diagrams but with lower values: nearly 0.25 kWel as a starting point for 20 K HED and 0.2 kWel for 100 K HED.The electrical output power can reach 2.5 and 1 kWel at 1750 K for both 100% and 50% of fuel feed, respectively.However, the limitations in temperature values for HE and turbine should be taken into consideration.The HED has a slight effect on power output for higher temperature values, while HED effect starts to increase for lower combustion temperatures.The sensitivity tool in Aspen was used in an optimization process.At each flue gas temperature (or turbine inlet temperature at 20 or 100 K HED), was varied within the range from 0.001 to 0.03 kg/s with steps of 0.001 kg/s, and at each step p is also changed within the range from 1.4 to 8 bar (abs) with steps of 0.3 bar, taking the maximum net output power from the cycle and then registering both p and , and so on, until about 1850 K flue gas temperature.The electrical output power shown in Figure 7 is at the maximum point for flue gas temperature.This is achieved by optimizing both p and , as explained above, and mapping both parameters in order to get the maximum power point as a function of flue gas temperature (see Figure 8).The sensitivity tool in Aspen was used in an optimization process.At each flue gas temperature (or turbine inlet temperature at 20 or 100 K HED), .m a was varied within the range from 0.001 to 0.03 kg/s with steps of 0.001 kg/s, and at each step p is also changed within the range from 1.4 to 8 bar (abs) with steps of 0.3 bar, taking the maximum net output power from the cycle and then registering both p and .m a , and so on, until about 1850 K flue gas temperature.The electrical output power shown in Figure 7 is at the maximum point for flue gas temperature.This is achieved by optimizing both p and .m a , as explained above, and mapping both parameters in order to get the maximum power point as a function of flue gas temperature (see Figure 8).
In Figure 8, the mapping diagram for both pressure and turbine air-mass flow shows the optimum values for both parameters at each turbine inlet temperature.It is shown that at low TIT values, it is necessary to keep low pressure and high .m a ; this is explained by the compressor power consumption, which depends on pressure value.Optimum pressure values for both 100% and 50% of nominal power are strongly dependent on turbine inlet temperature, while only a small correlation to nominal power and HED has been found.
As can be expected, optimized turbine air-mass flow shows different results.For the case of 50% fuel feeding, the optimized value is reduced nearly linearly.Considering changes in heat exchanger efficiency, it is increased to compensate for lower heat transfer.
kg/s with steps of 0.001 kg/s, and at each step p is also changed within the range from 1.4 to 8 bar (abs) with steps of 0.3 bar, taking the maximum net output power from the cycle and then registering both p and , and so on, until about 1850 K flue gas temperature.The electrical output power shown in Figure 7 is at the maximum point for flue gas temperature.This is achieved by optimizing both p and , as explained above, and mapping both parameters in order to get the maximum power point as a function of flue gas temperature (see Figure 8).In Figure 8, the mapping diagram for both pressure and turbine air-mass flow shows the optimum values for both parameters at each turbine inlet temperature.It is shown that at low TIT values, it is necessary to keep low pressure and high ; this is explained by the compressor power consumption, which depends on pressure value.Optimum pressure values for both 100% and 50% of nominal power are strongly dependent on turbine inlet temperature, while only a small correlation to nominal power and HED has been found.
As can be expected, optimized turbine air-mass flow shows different results.For the case of 50% fuel feeding, the optimized value is reduced nearly linearly.Considering changes in heat exchanger efficiency, it is increased to compensate for lower heat transfer.
The importance of mapping presented in Figure 8 is related to the plant controlling for load variations, whatever the biomass used.Thus, THI is the relative temperature value that needs to be measured in order to assign both p and .It should be noted that sensitivity analysis in Aspen produces small changes in HED to reach numerical stability and to conserve mass and energy balances.
Electrical efficiency is highly affected by the TIT as shown in Figure 9.While for 1060 K it reaches 10% at 4 bars, it is significantly lower at TIT of 938 K and 988 K.It should also be noted that optimal pressure changes with TIT.The importance of mapping presented in Figure 8 is related to the plant controlling for load variations, whatever the biomass used.Thus, T HI is the relative temperature value that needs to be measured in order to assign both p and .m a .It should be noted that sensitivity analysis in Aspen produces small changes in HED to reach numerical stability and to conserve mass and energy balances.
Electrical efficiency is highly affected by the TIT as shown in Figure 9.While for 1060 K it reaches 10% at 4 bars, it is significantly lower at TIT of 938 K and 988 K.It should also be noted that optimal pressure changes with TIT.To have an overview on the rotational speed of a suggested radial flow turbocharger, a micro size turbocharger with a blade radius of 0.03 m is assumed to be installed.Assuming no exit swirl at the turbine output; the specific work w can be calculated according to Equation (3) (see [46]): (3) where U2 and V2 are the blade and axial flow speeds respectively.Once finding the specific work (dividing turbine power by ), the blade speed is calculated from Equation (3), then the rotational speed is found by converting the linear velocity to an angular one.The speed variation in rpm with inlet turbine temperature is shown in Figure 10.This is an expected value for such turbocharger size; a value of 72,000 rpm is reached for larger sizes, as in [23].The back-work ratio (BWR) (that is, the ratio between power consumed by the compressor and mechanical power produced by the turbine), as seen in Figure 11, decreases with higher temperature values entering the turbine, thus leading to more efficient operation.To have an overview on the rotational speed of a suggested radial flow turbocharger, a micro size turbocharger with a blade radius of 0.03 m is assumed to be installed.Assuming no exit swirl at the turbine output; the specific work w can be calculated according to Equation (3) (see [46]): where U 2 and V 2 are the blade and axial flow speeds respectively.Once finding the specific work (dividing turbine power by .m a ), the blade speed is calculated from Equation (3), then the rotational speed is found by converting the linear velocity to an angular one.The speed variation in rpm with inlet turbine temperature is shown in Figure 10.To have an overview on the rotational speed of a suggested radial flow turbocharger, a micro size turbocharger with a blade radius of 0.03 m is assumed to be installed.Assuming no exit swirl at the turbine output; the specific work w can be calculated according to Equation (3) (see [46]): (3) where U2 and V2 are the blade and axial flow speeds respectively.Once finding the specific work (dividing turbine power by ), the blade speed is calculated from Equation (3), then the rotational speed is found by converting the linear velocity to an angular one.The speed variation in rpm with inlet turbine temperature is shown in Figure 10.This is an expected value for such turbocharger size; a value of 72,000 rpm is reached for larger sizes, as in [23].The back-work ratio (BWR) (that is, the ratio between power consumed by the compressor and mechanical power produced by the turbine), as seen in Figure 11, decreases with higher temperature values entering the turbine, thus leading to more efficient operation.This is an expected value for such turbocharger size; a value of 72,000 rpm is reached for larger sizes, as in [23].The back-work ratio (BWR) (that is, the ratio between power consumed by the compressor and mechanical power produced by the turbine), as seen in Figure 11, decreases with higher temperature values entering the turbine, thus leading to more efficient operation.

Cost Estimation
As discussed, literature on EFGT cycle economics have not handled EFGT ranges of 15 kWth (around 1.5-3 kWel).By using economical capital scaling [47], capital costs can be calculated from different installations while considering scaling effects as in Equation ( 4): (4) where C is the capital cost of a plant of a capacity M, , are the base capital cost and capacity (consider [21]), and s is the dimensionless scale factor (0.6 ≤ s ≤ 0.8).Due to the low number of installed systems for externally fired gas turbines, the scaling factor cannot be estimated at a higher precision, currently.Thus, the estimated capital cost of a 15 kWth power plant with about 1.6 kWel net output (including generator efficiency) is estimated to be 33800-65300 Euro, considering the reference data from [21].

Conclusions
Combined heat and power (CHP) technology based on biomass in general is a promising way to reduce fuel import dependency, improve the electrical grid as a distributed generation technology, and reduce carbon dioxide emissions.Using biomass as a fuel has advantages compared to solar and wind power, since its availability is not dependent on weather conditions.Solid olive waste can be stored as briquettes or as pellets, so power can be produced on demand.Also, the wastes are already available at centralized places (olive mills) which reduce transport costs and emissions.Usage of adequate technology (e.g., EFGT) makes it possible to have higher fuel flexibility, which provides more options (e.g., under changing agricultural situations).
For the current study, an EFGT with a nominal thermal power of 15 kW has been investigated to map optimized pressure and turbine air-mass flow for several conditions.The plant electrical efficiency is in the expected range based on the literature.The results show that plant efficiency between 5% and 17% is realizable, taking into consideration that the nominal state is around 10%, which depends on temperature limits for the setups.Noting that, efficiency could be improved when using a more efficient compressor and gas turbine, in addition to the potential of waste heat recovery.Application of the CHP concept is possible for domestic heating; as a result, the heating from olive residues is applicable beyond electrical generation applications.
Turbine inlet temperature is a dominant factor in the electrical efficiency, so higher temperature values in combustion flue gas could provide a more efficient operation.To this point, it is important

Cost Estimation
As discussed, literature on EFGT cycle economics have not handled EFGT ranges of 15 kW th (around 1.5-3 kW el ).By using economical capital scaling [47], capital costs can be calculated from different installations while considering scaling effects as in Equation ( 4): where C is the capital cost of a plant of a capacity M, C 0 , M 0 are the base capital cost and capacity (consider [21]), and s is the dimensionless scale factor (0.6 ≤ s ≤ 0.8).Due to the low number of installed systems for externally fired gas turbines, the scaling factor cannot be estimated at a higher precision, currently.Thus, the estimated capital cost of a 15 kW th power plant with about 1.6 kW el net output (including generator efficiency) is estimated to be 33,800-65,300 Euro, considering the reference data from [21].

Conclusions
Combined heat and power (CHP) technology based on biomass in general is a promising way to reduce fuel import dependency, improve the electrical grid as a distributed generation technology, and reduce carbon dioxide emissions.Using biomass as a fuel has advantages compared to solar and wind power, since its availability is not dependent on weather conditions.Solid olive waste can be stored as briquettes or as pellets, so power can be produced on demand.Also, the wastes are already available at centralized places (olive mills) which reduce transport costs and emissions.Usage of adequate technology (e.g., EFGT) makes it possible to have higher fuel flexibility, which provides more options (e.g., under changing agricultural situations).
For the current study, an EFGT with a nominal thermal power of 15 kW has been investigated to map optimized pressure and turbine air-mass flow for several conditions.The plant electrical efficiency is in the expected range based on the literature.The results show that plant efficiency between 5% and 17% is realizable, taking into consideration that the nominal state is around 10%, which depends on temperature limits for the setups.Noting that, efficiency could be improved when using a more efficient compressor and gas turbine, in addition to the potential of waste heat recovery.Application of the CHP concept is possible for domestic heating; as a result, the heating from olive residues is applicable beyond electrical generation applications.
Turbine inlet temperature is a dominant factor in the electrical efficiency, so higher temperature values in combustion flue gas could provide a more efficient operation.To this point, it is important to develop high-temperature standing material for a pressurized heat exchanger and turbine, which is also required to get the maximum benefit.
It is also shown that the plant tends to be less efficient at low input power percentages when the back-work ratio is more than 70%, while moving to higher flue gas temperatures leads to higher efficiency.
Further research is currently running to describe a detailed technical operation including practical findings, controls, transient behavior, and results of testing further biomass types on a real combustion system combined with a hardware-in-the-loop (HIL) system.

Figure 2 .
Figure 2. Combustion model in Aspen plus.

Figure 2 .
Figure 2. Combustion model in Aspen plus.

Figure 4 .
Figure 4. Compressor, turbine, and net output power as a function of pressure.

Figure 4 .
Figure 4. Compressor, turbine, and net output power as a function of pressure.

Figure 5 . 15 Figure 5 .
Figure 5. Compressor, turbine, and net output power as a function of turbine air mass flow.

Figure 6 .
Figure 6.Electrical efficiency and air-to-fuel ratio (AFR) with respect to the turbine inlet temperature at 100% of fuel consumption and 20 K heat exchanger temperature difference (HED).

Figure 6 .
Figure 6.Electrical efficiency and air-to-fuel ratio (AFR) with respect to the turbine inlet temperature at 100% of fuel consumption and 20 K heat exchanger temperature difference (HED).

Figure 7 .
Figure 7. Net output power variation with the turbine inlet temperature for four cases.

Figure 7 .
Figure 7. Net output power variation with the turbine inlet temperature for four cases.

Figure 8 .
Figure 8. Pressure and air mass flow where the maximum mechanical output power could be achieved at (a) 20 and (b) 100 K HED for 50% and 100% of nominal power.

Figure 8 .
Figure 8. Pressure and air mass flow where the maximum mechanical output power could be achieved at (a) 20 and (b) 100 K HED for 50% and 100% of nominal power.

Figure 9 .
Figure 9. Electrical efficiency as a function of pressure at selected turbine inlet temperature (TIT) at 20 K HED.

Figure 10 .
Figure 10.Rotational speed with inlet temperature at 100% fuel feed and 20 K HED.

Figure 9 .
Figure 9. Electrical efficiency as a function of pressure at selected turbine inlet temperature (TIT) at 20 K HED.

Energies 2016, 9 , 856 11 of 15 Figure 9 .
Figure 9. Electrical efficiency as a function of pressure at selected turbine inlet temperature (TIT) at 20 K HED.

Figure 10 .
Figure 10.Rotational speed with inlet temperature at 100% fuel feed and 20 K HED.

Figure 10 .
Figure 10.Rotational speed with inlet temperature at 100% fuel feed and 20 K HED.

Figure 11 .
Figure 11.Back-work ratio (BWR) at different turbine inlet temperatures at 100% fuel feeding and 20 K HED.

Table 2 .
Overview on previous studies on biomass-fueled EFGT.

Table 2 .
Overview on previous studies on biomass-fueled EFGT.

Table 4 .
Reference case simulation parameters.

Table 5
shows the pressure and temperature values, taking into consideration the pressure drop on HE terminals.