low-grade coal and biomass co-combustion on fluidized bed: exergy analysis
TRANSCRIPT
Low-grade coal and biomass co-combustion
on fluidized bed: exergy analysis
Carmen Martına, Miguel A. Villamanana, Cesar R. Chamorroa,Juan Oterob, Andres Cabanillasb, Jose J. Segoviaa,*
aLaboratory of Thermodynamic and Calibration TERMOCAL, Department of Energy,
School of Engineering, University of Valladolid, E-47011 Valladolid, SpainbDepartment of Fossil Fuels, Research Centre for Energy,
Environment and Technology Ciemat, E-28040 Madrid, Spain
Received 31 July 2003
Abstract
The purpose of this work is to prove the technical feasibility of the bubbling fluidized bed co-combustion,
using biomass and low-grade coal mixtures and applying the exergy method. The pilot plant modelled is an
atmospheric bubbling fluidized bed combustion chamber with a nominal capacity of 1 MWth. We have applied
the mass balance, the energy balance and the exergy balance to the plant in nine experiments, which have been
performed at different operation conditions. The exergy analysis includes the calculation of the exergy
destruction and the exergetic efficiency of the plant for these experiments. An estimation of the irreversibility
cost is also evaluated.
q 2005 Elsevier Ltd. All rights reserved.
1. Introduction
Low coal rank or coal waste and biomass co-combustion in coal fired power plants is a good technique
that contributes to the reduction of greenhouse gases. It is also a solution to the waste disposal problem.
Co-firing biomass with coal has the capability to reduce both NOx and SOx levels from coal fired power
plants. It also reduces CO2 emissions, and soil and water pollution [1].
Energy 31 (2006) 330–344
www.elsevier.com/locate/energy0360-5442/$ - see front matter q 2005 Elsevier Ltd. All rights reserved.
doi:10.1016/j.energy.2005.01.008
* Corresponding author. Tel./fax: C34 983 423 420.
Nomenclature
BL black lignite
cp specific heat capacity (J/kg K)
ctotal total cost per exergy flow input (V/year per kW)
Ctotal total cost (V/year)
Ca/S calcium/sulphur molar ratio
d.b. dry base_E exergy flow (MJ/h)_Ech chemical exergy flow (MJ/h)_Eph physical exergy flow (MJ/h)
Efconv carbon conversion (%)
Efret sulphur retention (%)
GD granulometrical distribution
H enthalpy
HHV higher heating value (kJ/kg)_I exergy destruction rate or irreversibility rate
k unit exergy cost
LHV lower heating value (kJ/kg)
mf fuel mass flow (kg/h)
P pine chips
p0 environment pressure
PA proximate analysis
Qloss heat loss to the environment (MJ/h)
Quseful heat rejected to the water (MJ/h)
RC refuse coal
Tbed bed temperature
T0 environment temperature (K)
UA ultimate analysis
vf fluidization velocity (m/s)
W work
x working hours
z cost of coal
DG0f standard molar Gibbs function of formation (J/mol)
30 standard molar chemical exergy (J/mol)
30el standard molar chemical exergy of an element (J/mol)
3ph specific physical exergy (J/kg)
h thermal or energetic efficiency
j exergetic or rational efficiency
C. Martın et al. / Energy 31 (2006) 330–344 331
In this context, the project deals with semi-industrial scale studies on the co-firing of different coal
wastes or low rank Spanish coal with biomass, in order to promote the clean, efficient use of these
resources. The biomass used in this study is made of pine chips, i.e. wood waste from forestry and wood
processing of the region where the pilot plant is located.
C. Martın et al. / Energy 31 (2006) 330–344332
This work is related to a previous one [2,3] which was involved in an EU-project ‘Combined
Combustion of Biomass/Sewage Sludge and Coals of High and Low Rank in Different Systems of Semi-
industrial and Industrial Scale’ the main results of which were summarized by Hein and Bemtgen [4].
The use of waste coal, with low heating value and high ash content, mixed with biomass is interesting
because of the complementary properties of the two fuels. Opposed to the typical characteristics of poor
coal, biomass has a low ash content and a high volatile content that is favourable, both from the technical
and environmental point of view, to a clean combustion of the coals that are being taken into
consideration. The goal of the project is to prove at semi-industrial scale the technical feasibility of the
fluidized bed as a clean technology for the combustion and determine the influence of co-firing of coal
waste and biomass on the combustion process, the gaseous emissions, the flue gas cleaning process, the
fireside fouling of the boiler and its influence on the heat efficiency and the composition of solid residues.
Co-combustion of coal and biomass has been quite extensively studied [1–9]. As it was presented by
Sami et al. [7] in a complete review of literature on coal co-firing with biomass fuels, biomass and coal
blend combustion is a promising combustion technology; however, significant development work is
required before large-scale implementation can be realized.
The main purpose of this paper is to present and discuss the most significant results achieved in the
bubbling fluidized bed combustion plant using exergy analysis. [10]
We do not try to undertake a deep study of the combustion process because this has been carried out
by other authors [11–13]; we have applied the exergy balance to the experimental installation and
calculated the exergetic efficiency of the process to quantify exergy destruction and parameters of the
installation that could improve the efficiency of the process.
2. Experimental section
2.1. Pilot plant
The pilot plant studied is an atmospheric bubbling fluidized bed combustion chamber. It has a
nominal capacity of 1 MWth. Fig. 1 shows the flowsheet scheme of the plant. The combustor vessel is
divided into three parts for easier maintenance. The lower part is a common windbox and a distributor
plate with a 1 m2 total surface. The distributor plate is formed by a staggered 608 array of 522 nozzles
supplied from the common windbox. The middle part is a vessel with 1.14 m internal diameter and 1.2 m
height. It is lined with approximately 2-inch. thick refractory materials, which are protected with
an abrasion-resistant paint. The third part is a vessel of 2.8 m height. The last 0.6 m of this vessel has an
increase diameter to minimize the elutriation of materials to the cyclone.
The air is provided by two fans which produce air flows at 500 N m3/h (secondary air) and
1500 N m3/h (primary and tertiary air). It is introduced into the combustor at three levels: the primary air
below the distributor plate, the secondary at the fuels feeding same location, and the tertiary about above
the bed. The fuels are introduced into the bed by means of a screw conveyor feeder.
Heat extraction is made by means of three heat exchangers: two of them located in the bed area and
the third one at the top of the freeboard to cool the flue gas. In Fig. 2, there is a detail of the heat
exchanger’s geometry. Each heat exchanger has 34 vertical section and 34 semicircular section and the
tube has a diameter of 2.54 cm.
BIOMASS
1
2
COAL
1
2
1 2
LIMESTONE
9
6
3
10
10
98
7
5
13
4
11
TEMPERATURE
PRESSURE
FLOW
12
O2 NO2
CO SO2
CO2 NO
1 HOPPER 2 FEEDING SCREW 3 COMBUSTOR
4 MULTICYCLONE 5 PRIMARY AIR 6 SECONDARY AIR
7 TERTIARY AIR 8 EXTRACTOR 9 ASH
10 HEAT EXCHANGER11 CONTROL 12 GAS SAMPLE COLLECTOR13 SAMPLES COLLECTED
Fig. 1. Scheme of the atmospheric bubbling fluidized bed pilot plant.
C. Martın et al. / Energy 31 (2006) 330–344 333
The pilot plant has a Hartmam and Braun distributed process control system, Contronic 3P. More
details of the pilot plant have been published previously [14].
2.2. Analytical procedures
For each fuel (black lignite, refuse coal or pine chips), proximate, ultimate, granulometrical
distribution, bed and fly ashes, and higher heating value have been determined by conventional methods.
14.47 cm
4.37 cm
Fig. 2. A detail of heat exchanger’s geometry.
Table 1
Proximate analysis (PA), ultimate analysis (UA), granulometrical distribution (GD), higher heating values, HHV and chemical
exergy, Ech for the fuels in dry base (d.b.)
Sample Black lignite Refuse coal Pine chips
PA (%d.b.)
Fixed carbon 30.50 9.12 21.41
Volatile 41.29 11.25 75.56
Ashes 28.84 79.63 3.03
Moisture 8.27 1.87 12.75
UA (%d.b.)
Carbon 48.76 12.67 52.03
Hydrogen 2.20 1.26 5.97
Nitrogen 0.90 0.53 0.41
Sulphur 9.86 1.48 0.07
Oxygen 9.44 4.43 40.08
Chloride !0.02 !0.02 !0.02
GD (wt%)
Mesh screen mm Partial Acumm. Partial Acumm. Partial Acumm.
C63 0.00 0.00 0.00 0.00 0.00 0.00
K63 C32 0.00 0.00 0.00 0.00 0.00 0.00
K32 C16 0.00 0.00 0.00 0.00 3.76 3.76
K16 C8 0.00 0.00 0.00 0.00 20.52 24.28
K8 C4 0.42 0.42 0.00 0.00 26.65 50.93
K4 C2 20.90 21.32 0.20 0.20 23.19 74.12
K2 C1 26.85 48.17 17.59 17.78 12.64 86.75
K1 C0.5 16.95 65.13 22.21 39.99 5.72 92.48
K0.5 C0.25 15.64 80.77 23.15 63.14 3.56 96.03
K0.25 C0.125 9.94 90.72 16.25 79.39 1.84 97.87
K0.125 C0.063 5.40 96.12 9.70 89.09 1.28 99.16
K0.063 3.88 100.00 10.91 100.00 0.84 100.00
HHV (kJ/kg) (db) 20,421 3936 20,630
Ech(kJ/kg) (db) 22,010 4220 21,469
C. Martın et al. / Energy 31 (2006) 330–344334
The characteristics of the fuels employed in this study and their compositions are shown in Table 1.
Measurements of emissions were made continuously with a multicomponent infrared photometer,
Hartmam and Braun Uras 10P. It has five measuring channels: nitrogen oxide, nitrogen dioxide, sulphur
dioxide, carbon monoxide and carbon dioxide. The oxygen concentration was measured with a
zirconium oxide cell ETC 2000.
2.3. Combustion experiments
As fuels, two coals have been selected for study: black lignite and washing reject coal. The biomass
fuel for test runs was made of pine chips. This is the most common forest residue available in Spain,
often in mixtures with small amounts of other wood residues. It is also one of the most abundant residues
produced by Spanish wood industries.
We have analysed nine combustion experiments. The fuel used in them and their operation conditions
are shown in Table 2. The parameters that have been varied during experimentation are bed temperature,
Table 2
Operation conditions of the combustion experiments: number of the experiment, fuel used RC (refuse coal), P (pine chips), BL
(black lignite), percentage in weight of biomass, fuel mass flow (mF), bed temperature (Tbed), molar ratio of calcium and sulphur
(Ca/S) and fluidization velocity (vf)
Exp. Fuel %P mf (kg/h) Tbed (8C) Ca/S (mol) vf (m/s)
1 RCCP 58 294.3 850 5.99 0.63
2 RCCP 57 299.7 847 5.13 0.73
3 P 100 178.6 807 0.00 0.62
4 RCCP 57 272.7 805 2.66 0.62
5 BLCP 47 165.6 842 3.00 0.63
6 BLCP 47 165.6 840 2.99 0.71
7 BLCP 28 178.2 842 2.92 0.63
8 BLCP 28 178.2 850 2.92 0.73
9 BL 0 152.0 850 2.75 0.73
C. Martın et al. / Energy 31 (2006) 330–344 335
Ca/S molar ratio, biomass/coal ratio and fluidization velocity which have been achieved through the
modification of primary to tertiary air ratio.
3. Results
We have applied the mass balance, the energy balance and the exergy balance to the
atmospheric bubbling fluidized bed combustion chamber for the nine experiments referenced in
Table 2.
As inputs to the plant we consider the coal, the biomass, the limestone (which is added to avoid
sulphur oxides emissions) and the air. The outputs are the exhaust gases, the ash recovered in the cyclone
and in the bed and the heat transfer to the three heat exchangers. The difference between both represents
the heat loss to the environment.
The modelling of the experimental installation has been done using an EXCEL (MS) sheet where the
experimental data are introduced.
The uncertainties in the measured parameters are G2 8C for temperature; G0.1% (full-scale) for
pressure and G2% (full-scale) for mass flow.
3.1. Mass balance
Results of the mass balance are summarized in Table 3. This contains the composition of the exhaust
gas (dry base) per kJ input to the installation and normalized at 6% oxygen, these units allow a better
analysis of the emissions. In the last two columns, the efficiencies of carbon conversion (Efconv) and
sulphur retention (Efret) are shown.
Satisfactory combustion results have been achieved for black lignite and all mixtures coalCbiomass
studied, as shown in Table 3. All the experiments have achieved a carbon conversion related to the
residual heat value in the ash ranging 97.6–99.8%.
The addition of biomass to high sulphur black coal produces a decrease of SO2 emissions in
correspondence to the proportion of biomass, and, hence, the amount of sulphur, added. The increase of
Table 3
Flue gas composition expressed in dry base (mg/MJ) and 6% oxygen (mg/N m3)
Exp. Flue gas composition Efficiency
CO2 (%) Dry base (mg/MJ) 6% O2 (mg/N m3) Efconv (%) Efret (%)
SO2 CO NOx SO2 CO NOx
1 11.5 334 188 134 821 461 329 97.6 72.3
2 15.0 205 148 190 491 354 454 98.1 86.5
3 15.4 21 105 56 55 275 146 99.3 78.1
4 15.7 236 83 107 605 212 275 98.9 84.5
5 17.0 621 112 34 1864 337 101 98.7 91.0
6 16.9 538 130 39 1542 373 112 99.5 92.0
7 16.8 626 134 34 1898 406 104 98.4 92.8
8 17.7 687 113 33 1973 325 96 99.8 92.4
9 16.8 675 159 36 1963 461 105 99.4 94.1
Efconv, Efficiency of carbon conversion (%) and Efret, efficiency of sulphur retention (%).
C. Martın et al. / Energy 31 (2006) 330–344336
fluidization velocity seems to cause a light reduction of SO2 emissions, both for refuse coal and black
lignite mixtures with biomass, increasing the sulphur retention rate. In mixtures of refuse coal and
biomass, the increase of molar Ca/S ratio, from about 2.5 to 5 did not cause any significant effect on the
sulphur retention rate which could be in connection with low sulphur content in fuel mixtures.
With all feed materials and mixtures, it was possible to reduce residual carbon content in bed ash to
!0.6%.
The NOx content in the combustion emissions remained at low levels in all cases. A slight increase in
the case of tip coal and biomass was observed. This fact is in connection to the higher content of nitrogen
in ash-free refuse coal when compared to ash-free black lignite.
3.2. Energy balance
The energy balance for a control region undergoing a steady-state reacting process may be written as
X_Q C
X_W Z
XP
_noutðHf CDHÞout K
XR
_ninðHf CDHÞin (1)
where the enthalpy of a compound is composed of Hf , associateD with the formation of the compound
from its elements at standard conditions, and DH, associated with a change of state at constant
composition. The equation can be rearranged to readX_Q C
X_W Z
XP
_noutHfout K
XR
_ninHfin C
XP
_noutDHout KX
R
_ninDHin (2)
The enthalpy flow reactants to the control region have the contributions of the fuels, the
limestone and the air. In addition to the combustion reactions, the reactions related to the
dissociation of the limestone and the formation of calcium sulphate must be taken into account, as
C. Martın et al. / Energy 31 (2006) 330–344 337
they are expressed below:
CaCO3/CaO CCO2
CaO CSO2 C1=2O2/CaSO4
The dissociation of CaCO3 is endothermic but formation of CaSO4 is exothermic through the
mass balance known. The net effect of limestone addition is that a part of the energy produced by
the combustion of the fuel is consumed to avoid the presence of SO2 in the flue gas.
As we have considered that the pressure and the temperature of the input matter flows are at standard
conditions, the term DHin for the reactants is zero. On the other hand, the enthalpy of combustion is the
lower heating value of the fuel with the minus sign.
For the products, the contributions are the flue gas and bed and cyclone ashes. We have taken into
account the temperature dependence of the heat capacity for the different components. The presence of
CaCO3, CaO, CaSO4, and CaS in the ash has been considered, so that the energy balance for the plant
can be written as:
X_Q þ
X_W ¼
Xfuel
_miðKLHVÞi þ _nCaCO3, H
fCaO þ H
fCO2
KHfCaCO3
� �
þ _nCaO, HfCaSO4
þ HfCaO KH
fSO2
� �þ
Xash
miðLHVÞash
þX
flue;gas
_mi
ðTout
T0
cpiðTÞdT þX
ash;bed
_mi
ðTout
T0
cpiðTÞdT
þX
ash;cyclone
_mi
ðTout
T0
cpiðTÞdT
(3)
The work input to the fans can be neglected:X
_W z0 (4)
Concerning the heat flow, the purpose of the installation is to recover heat to the water but there is also
a heat loss to the environment, so that both heat flows are negativeX
_Q Z _Quseful C _Qloss (5)
The heat transfer from the chamber to the water is calculated by measuring the flow matter and the
input and the output temperatures of the water for the three heat exchangers:
_Quseful ZKX3
iZ1
_miðhout;i Khin;iÞ (6)
In Table 4, we have summarized the more relevant results of the energy balance for the nine
experiments studied. The absolute value of useful heat flow transfers to the water (Quseful) (Eq. (6)); the
energy of the inputs to the chamber (Input) defined by
Table 4
Results of the energy balance: Heat transfer from the chamber to the water (Quseful), the energy of the input to the chamber
(Input), the energy output from the chamber (Output), the heat loss to the environment (Qloss) and the thermal efficiency of the
combustion chamber (h).
Exp. Quseful (MJ/h) Input (MJ/h) Output (MJ/h) Qloss (MJ/h) h (%)
1 1587.1 3256.5 2397.4 859.1 48.7
2 1596.4 3247.5 2428.8 818.7 49.2
3 1532.2 2907.2 2117.2 790.0 52.7
4 1563.2 2933.5 2208.0 725.5 53.3
5 1500.8 2762.8 2093.3 669.5 54.3
6 1524.2 2832.1 2131.3 700.8 53.8
7 1470.5 3080.0 2152.9 927.1 47.7
8 1603.6 3052.0 2332.9 719.1 52.5
9 1390.8 2524.6 1914.2 610.5 55.1
C. Martın et al. / Energy 31 (2006) 330–344338
Input ¼Xfuel
_miðKLHVÞi � _nCaCO3, H
fCaO þ H
fCO2
KHfCaCO3
� �
þ _nCaO, HfCaSO4
þ HfCaO KH
fSO2
� �(7)
The energy of the outputs from the chamber (output) defined by
Output ZXash
miðLHVÞash CX
flue;gas
_mi
ðTout
T0
cpiðTÞdT CX
ash;bed
_mi
ðTout
T0
cpiðTÞdT
CX
ash;cyclone
_mi
ðTout
T0
cpiðTÞdT KQuseful (8)
where the heat loss to the environment (Qloss) is the difference between both and; the efficiency of the
combustion chamber (h) is calculated as the ratio between the absolute value of the heat transfer to the
water (Quseful) and the energy input to the chamber (input).
In Fig. 3, the energy balance is represented graphically as the distribution of the input energy (%).
It may be noticed that in the mixtures formed by refuse coalCbiomass (experiments 1, 2 and 4), the
energy input from biomass is not lesser than 86%.
The results show that the energetic efficiency of the process is some 50%, ranging from 47.7% for
experiment 7 to 55.1% for experiment 9, which is the highest efficiency achieved.
On the other hand, the heat loss to the environment represents 25% of the energy input, where 20% of
the outlet energy is found in the combustion gas.
3.3. Exergy balance
Finally, the experimental data of the pilot plant has been analysed using the exergy method which is
the main purpose of the present work.
The exergy balance for a control region undergoing a steady-state process may be written as
Fig. 3. Percentage distribution of input energy for the nine experiments studied.
C. Martın et al. / Energy 31 (2006) 330–344 339
_I Z _Einput K _Eoutput ZX
IN
_Ei KXOUT
_Ei (9)
where the exergy flow to or from the control region is associated with the inflow or outflow of matter,
heat transfer and work transfer. The difference between the two, the loss of exergy rate, is also called
exergy destruction rate or irreversibility rate (I).
The exergy associated to the flow of matter has two contributions the physical exergy (Eph) and the
chemical exergy (Ech) so that:
_Ei Z _Eph C _Ech (10)
The application of the exergy balance to the atmospheric bubbling fluidized bed combustion chamber
has been carried out as explained below. The exergy flow input to the combustion plant is
_Einput ZX
i
_Efuel;i C _Elimestone C _Eair (11)
where the physical exergy for these three streams is zero because it is considered that they enter into the
plant at environmental state (p0Z101.325 kPa, T0Z298.15 K).
The chemical exergy of the compounds has been calculated accurately [15,16] and the standard
chemical exergy of the fuel ðE0chÞ can be written as
E0ch Z DG0
f CX
nelE0ch;el (12)
where DG0f is the standard molar Gibbs function of formation, nel is the number of moles of the elements
in the compound under consideration and E0ch;el is the standard chemical exergy of the constituent
elements. These data were taken from Szargut [16] and are summarized in Table 5. In the calculation of
the Gibbs function, the entropy values are needed and they were estimated using the procedure described
in the literature [17]. The value obtained for the chemical exergy of the fuel is close to its higher heating
value, as it can be seen in Table 1.
For the chemical exergy of limestone, we have considered the useful work which can be obtained
from the reactions referred above in the energy balance, and the chemical exergy of the compounds were
taken from literature [16] and are summarized in Table 5.
Table 5
Values of the standard chemical exergy of different substances used in the calculations of the exergy balance (T0Z298.15 K;
p0Z101.325 kPa)
Fuel E0ch
a (kJ/mol) Flue gas E0ch
a (kJ/mol) Ash E0ch
a (kJ/mol)
C(s) 410.26 CO2 19.87 CaCO3 1.0
O2(g) 3.97 H2O(l) 1.1 CaO 110.2
H2(g) 236.09 H2O(g) 9.7 CaSO4 8.2
N2(g) 0.72 SO2 314.0
S(s) 609.6 CO 275.10
NO2 55.3
NO 88.9
a Taken from Ref. [16].
C. Martın et al. / Energy 31 (2006) 330–344340
The exergy flow output from the combustion plant is:
_Eoutput Z _Euseful C _Eflue;gas C _Eash;bed C _Eash;cyclone (13)
where Euseful is the exergy of the heat flow transfer from the chamber to the water and it is calculated as:
_Euseful Z _Quseful 1 KT0=Tbed
� �(14)
We have used the bed temperature instead of the water temperature because the purpose of the plant is
not to produce steam water, only dissipated the heat rejected and quantified it in order to study the effects
of different fuels and fluidization conditions in the performance of the plant so that the irreversibility due
to heat transfer from fluidized bed to water is not included in the calculations.
The physical exergy of the streams has been calculated for the flue gases and for the ashes in the bed
and in the cyclone neglecting the effect of pressure drop. The thermal component of specific physical
exergy of the stream is
Eph Z
ðT1
T0
cpðTÞdT K
ðT1
T0
cpðTÞðT0=TÞdT (15)
where cp is the specific heat capacity, T0 is the environmental temperature and T1 is the temperature of
the stream considered. The values of the standard chemical exergy for the components of the ashes and
the flue gas were taken from the literature [16] and are summarized in Table 5.
To complete the exergy analysis of the plant, the exergetic efficiency or rational efficiency (j) is
calculated
j Z _Euseful= _Einput (16)
where both terms have been defined in Eqs. (11) and (14).
Table 6 summarizes the results of the exergy balance for the nine experiments studied: the exergy of
the inputs (Ein); the exergy of the outputs (Eout) of the chamber as defined in Eqs. (11) and (13),
respectively; the total exergy destruction or irreversibility rate (I) (Eq. (9)), the value of the exergy of the
heat flow transferred to the water (Euseful) (Eq. (14)), and the exergetic efficiency (j) (Eq. (16)).
The table also presents the values of the exergy of the flue gas and the exergy of the ashes and the
contributions of the physical exergy and chemical exergy to both streams are given separately.
Table 6
Results of the exergy balance for nine experiments studied
Exergy flow
(MJ/h)
Experiment number
1 2 3 4 5 6 7 8 9
Ein 3789.9 3784.4 3381.8 3425.2 3182.3 3240 3509.5 3486.5 2895.8
Eout 1660.8 1718.3 1498.3 1562.9 1545.9 1570.9 1584.7 1751.3 1493.2
I 2129.1 2066.1 1883.5 1862.3 1636.4 1669.1 1924.8 1735.2 1402.6
I/Ein (%) 56.2 54.6 55.7 54.4 51.4 51.5 54.8 49.8 48.4
Euseful 1165.8 1171.5 1109.3 1130.9 1099.5 1116.0 1077.3 1177.9 1021.6
jZEuseful/Ein (%) 30.8 31.0 32.8 33.0 34.6 34.4 30.7 33.8 35.3
Euseful/Eout (%) 70.2 68.2 74.0 72.4 71.1 71.0 68.0 67.3 68.4
Eflue gas 465.4 516.9 386.9 413.4 356.9 384.2 404.1 457.4 326.0
Eflue gas/Ein (%) 12.3 13.7 11.4 12.1 11.2 11.9 11.5 13.1 11.3
Ech flue gas 215.3 259.6 199.6 212.9 183.2 191.9 206.6 220.0 182.2
Eph flue gas 250.1 257.4 187.3 200.5 173.6 192.3 197.5 237.4 143.8
Eash 29.6 29.9 2.1 18.6 89.6 70.7 103.3 115.9 145.6
Eash/Ein (%) 0.8 0.8 0.1 0.5 2.8 2.2 2.9 3.3 5.0
Ech ash 20.9 22.1 1.8 13.5 68.1 51.9 76.2 84.9 110.8
Eph ash 8.7 7.8 0.4 5.1 21.5 18.8 27.1 31.0 34.8
C. Martın et al. / Energy 31 (2006) 330–344 341
For a better understanding of these results, those values are referred to the exergy input as a
percentage and they are represented graphically in Fig. 4.
The results obtained for the experiments studied show that a percentage ranging from 48.4
(experiment 9) to 56.2% (experiment 1) of the exergy input to the pilot plant is destroyed due to the
irreversibility of the process, they arise from the combustion process, the reactions of dissociation of the
limestone and also due to thermal interaction (Qloss) with the environment. Not all the exergy output is
useful exergy, an amount ranging from 67.3 (experiment 8) to 74.0% (experiment 3) of the exergy output
is transferred to the water (Euseful); the other exergy output to the plant is meanly the exergy of the flue
gas, ranging from 21.8% for experiment 9 to 30.1% for experiment 2. The exergy of the ash is only
significant in the mixtures containing black lignite, for example, in experiment 9 fed pure black lignite
reaches 9.7% of the exergy output.
Fig. 4. Percentage distribution of input exergy for the nine experiments.
C. Martın et al. / Energy 31 (2006) 330–344342
The exergy losses in the flue gas and in the ash are taken into account in the definition of the exergetic
efficiency. It ranges from 30.8% for experiment 1 to 35.3% for experiment 9 which means that 70% of
the exergy input to the plant is destroyed or lost as shown in Fig. 4.
To decrease the exergy losses, the exit temperature of the exhaust gas may be reduced adding heat
exchangers into the plant. This allows recovering physical exergy of the combustion gas but not the
chemical exergy, which represents some 6% of the input of exergy. Also a better insulation of the plant
could reduce the heat loss to the environment which represents 12% of the input of exergy.
In order to apply the exergy method to optimise the plant we have analysed how the exergetic
efficiency depends on the operation parameters.
The comparison between experiments 1 and 2 or experiments 5 and 6 indicates that the fluidization
velocity does not affect the exergetic efficiency.
On the other hand, the experiments studied show that an increase in the Ca/S ratio produces a decrease
in the rational efficiency and the sulphur retention is not improved, so that high ratios are not convenient
from an environmental and an exergetic point of view.
The bed temperature directly affects the performance of the plant because of the definition of useful
exergy (Eq. (14)). Attending to the exergy analysis, the exergetic efficiency increases for higher bed
temperatures, although this conclusion is not clear in the experimental results because there are other
factors which operate simultaneously.
On the other hand, an advantage of combustion process at low temperatures, as occurs in these
experiments, is to avoid NOx emissions. This is one of the reasons to consider fluidized bed combustion
as a clean technology for coal.
3.4. Exergy costing
The analysis of the combustion chamber performance has been completed with the estimation of the
total cost of the exergy destruction (Ctotal) in V/year, for each experiment. We have calculated, for each
experiment, the cost of the fuel necessary to produce a useful exergy equal to the destructed exergy, in
the same conditions. It can be expressed as
Ctotal Z _Ixkz (17)
where x is the working hours of the plant; k is the unitary cost of exergy or the inverse of the exergetic
efficiency and z is the cost of coal. The values of total cost for the nine experiments, summarized in
Table 7, have been estimated assuming that the plant operates 7500 h/year and that the cost of coal is
0.664 ¢ V/thermia of higher heating value (1 thermiaZ0.8598 kW h), considering a 4550 kcal/kg
average higher heating coal and of 30.23 V/t coal national price [18].
To directly compare the results obtained in the irreversibility cost, the values of the total cost (Ctotal)
have been divided by the exergy flow input to the installation for the nine experiments (ctotal) and they
are summarized in Table 7.
A first conclusion is that the cost depends on the type of fuel used, the combustion of mixtures
containing pine chips and refuse coal is more expensive than the combustion of mixtures containing pine
chips and black lignite.
Table 7
Economical study: total irreversibility cost (Ctotal) and total irreversibility cost per input exergy (ctotal)
Exp. Ein (kW) I (kW) k j (%) Ctotal (V/year) ctotal (V/year per kW)
1 1053 591 3.25 30.8 82,243 21.7
2 1051 574 3.23 31.0 79,386 21.0
3 939 519 3.05 32.8 67,779 19.7
4 951 512 3.03 33.0 66,426 19.1
5 884 458 2.89 34.6 56,675 17.8
6 900 463 2.90 34.4 57,492 17.7
7 975 534 3.26 30.7 74,539 21.2
8 968 482 2.96 33.8 61,089 17.5
9 804 390 2.83 35.3 47,258 16.3
C. Martın et al. / Energy 31 (2006) 330–344 343
Only experiment 7 behaves in a different way, it is probably due to a bad performance of the
experiment because of values obtained for the efficiency. The other three experiments using black lignite
and pine give similar results.
On the contrary, in mixtures of refuse coal and pine chips, there is a clear relationship between
exergetic efficiency and cost. Comparing experiments 2 and 4, an increase of 31–33% (6.5%) in
the exergetic efficiency reduces the cost of 21–19.1 V/year per kW, which represents a decrease of 9%,
which is quite significant.
4. Conclusion
In this paper, we have applied the exergy analysis to nine experimental results of an atmospheric
bubbling fluidized bed combustion chamber. This plant has been used to study the behaviour of the
combustion of mixtures formed by waste coal and biomass. To calculate the energy and exergy balances,
the pressure and temperature of the different streams that enter or leave the plant, the bed temperature have
been measured and also the compositions of flue gas and ashes have been analysed for the mass balance.
The irreversibility and the exergetic efficiency have been quantified for the nine experiments, it ranges
from 31 to 35%. The exergy balance shows that the performance of the plant could be improved by
decreasing the exit temperature of the flue gas and with a better isolation of the combustor chamber.
Concerning the operation conditions, the fluidization velocity does not influence the exergetic
efficiency whereas an increase in the Ca/S ratio produces a decrease in the rational efficiency but the
sulphur retention is not improved continuously, so that, there is an optimum ratio.
It should be underlined that we have found no works concerning the application of the exergy method
to experimental data from biomass and coal co-firing for comparison in the literature.
Acknowledgements
Support for this work came from the Direccion General de Ensenanza Superior e Investigacion
Cientıfica Program FEDER. Spanish Ministery of Education, Project 1FD97-2221-C02-02 and Project
EET2001-4573-C04-03.
C. Martın et al. / Energy 31 (2006) 330–344344
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