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Concept Analysis of an Electrical Fuel CellIntegration in Modern Aircraft
A Lucken1, T. Kut2, H. Langkowski1, S. Dickmann2, Senior Member IEEE and D. Schulz1, Member IEEE1Electrical Power Systems, Helmut Schmidt University, 22043 Hamburg, Germany
2Fundamentals of Electrical Engineering, Helmut Schmidt University, 22043 Hamburg, Germany
Abstract—The reduction of pollutant emissions and hence theincreasing of the eco efficiency of future aircraft is one ofthe major challenges for the aviation industry. Executing theMore Electric Aircraft concept can be one approach to achievethese high targets. One idea in this context is to substitutethe traditional Auxiliary Power Unit by a Multifunctional FuelCell System. It is necessary to transform the load-dependentfuel cell stack output voltage to the intended electrical onboardgrid voltage level. To increase the efficiency and reduce thesystem weight an optimized electrical integration is presented.Measurement results on a test bench confirm the theoreticalconcepts.
Index Terms—Fuel Cell Integration, More Electric Aircraft
I. INTRODUCTION
In the recent years, the international air transport has
increased more and more. The global aircaft fleet is expected
to double in the next years. Therefore, the trend is towards
higher efficiency for modern commercial aircraft. A significant
reason are the limited resources and therefore the increase of
the kerosene price, which leads to enforce the development of
weight optimized electrical architectures. An approach could
be the implementation of the More Eletric Aircraft (MEA)
concept. Within this concept, hydraulic and pneumatic systems
should be substituted by electrical ones, which lead to an
increase of the electrical power, see Figure 1 [1].
1
2
3
4
5
B767 B777 A380 B787 C Series
Next Gen.
(long range)
Next Gen.
(short range)
Conventionalaircraft
More ElectricAircraft
Elec
trica
l pow
er (k
W/s
eat)
Fig. 1: Increase of the electrical power demand [2].
The rising demand of the electrical energy leads to an
increase of the voltage level for power transmission on a
modern aircraft. Therefore, a High Voltage DC (HVDC) grid
(540 VDC or ±270 VDC) could be used [3]. One reason for
the decision of 270 VDC is the transformation of the traditional
three phases 115 VAC aircraft grids. A thyristor bridge rectifier
(B6) with a trigger delay angle of α = 0◦ could be used and
is described as follows [4]:
VDC =3 ·√3 ·√2
π· cos(α) ·VAC (1)
The HVDC has several positive effects compared to
conventional AC grid. The decrease of the cable diameter
due to the reduced current flow, while transmitting the same
amount of electrical power leads to weight savings. The
reduction of the dissipation power due to the higher voltage
level increase the system efficiency. Moreover, it is possible
to design a lightweight DC/DC converter due to the small
number of electronic components which leads to an average
high power density [5]. Figure 2 shows the increase power of
different conventional Auxiliary Power Unit (APU) systems
of the last 50 years. It is presented that the share of the
shaft power compared to the total power decreases while
the electrical power increases. Normally, the conventional
APU has to provide both, electrical energy and compressed
air. Modern aircraft have an electrical engine start and
an electrical environmental control system and substitute
the pneumatic ones, which reduce the share of the shaft power.
0
325
700
1050
1400
1963
1983
1988
1993
2007
2008
Pow
er (k
W)
Overall Power
Shaft PowerElectrical Power
year aircraft APU-type196319831988199320072008
B727A310A320B747A380B787
GTCP 85GTCP 331GTCP 131GTCP 600PW 980AAPS 5000
Fig. 2: Increasing APU power within the last 50 years [6], [7], [8],[9].
The trend to create an electrical engine start leads to the
approach to use a Multi Functional Fuel Cell System (MFFCS)
to increase the efficiency of a modern APU concept. The
MFFCS could replace the noisy and inefficient APU in the
tail of the aircraft. In addition, to the high efficiency it must
543978-1-4673-4430-2/13/$31.00 ©2013 IEEE
be ensured that the system weight of the MFFCS does not
exceeds the overall weight of the substituted components. The
required DC/DC converter, as well as the fuel cell stacks are
the heaviest single components. Therefore, a weight optimized
electrical integration is required. As a part of the project
cabin technology and multifunctional fuel cell systems, the
Institutes of Electrical Power Systems and the Fundamentals
of Electrical Engineering are dealing with a high efficiency
weight optimized power supply based on a multi functional
fuel cell system in cooperation with Airbus Operation GmbH.
A. The advantages of MFFCS
The reduction of emissions such as carbon dioxide (CO2)
gas, the water production and the noise level reduction are
important benefits. The Oxygen Depleted Air (ODA) can also
be used for fuel tank inerting and for fire suppression inside
the aircraft. Moreover, the ram air turbine (RAT) could be sub-
stituted due to the independency of the MFFCS from kerosene
[10],[11]. The main possible applications are illustrated in
Figure 3.
Fig. 3: Possible application scenario for the MFFCS [12].
The emission saving effect of the MFFCS is 100 %, because
no pollutants are produced during the reaction of hydro-
gen and air. With the assumption that the combustion of
1 kg kerosene produced 3.15 kg CO2 and a consumption of
kerosene of 800 l/(day·aircraft) is required, leads to approxi-
mately 2000 kg/(day·aircraft) CO2, which can be avoided.
B. Aim of Investigation
The aim of this paper is to present the methodology to confirm
the theoretical concepts for a weight optimized buck converter
based on an optimal fuel cell output voltage. The theoretical
concept will be presented. Simulation as well as measurement
results supporting these theoretical concepts.
II. ELECTRICAL INTEGRATION
A significant impact for increasing the electrical power in
modern aircraft is the application of a full electrical envi-
ronmental control system. The MFFCS has to be designed
for maximum power in order to ensure that all connected
consumers are supplied with electrical energy, even under hot
ambient conditions (ISA hot day (Tamb = 311.15K)). The fuel
cell output voltage strongly depends on the connected load.
DC/DC converters could be used to transform the fuel cell
(FC) voltage into the HVDC grid voltage. Figure 4 shows a
typical polarization curve of a fuel cell system.
0 10.4
1
Fuel cell current (normalized)
Fuel
cel
l vol
tage
(nor
mal
ized
)
Converter PowerMaximum Power
HVDC range
Fig. 4: Fuel cell polarization curve with the allowed HVDC range.The upper limit is set to ±280 VDC and the lower limit to ±250 VDC
according to the aircraft electrical power characteristics (MIL-STD.704F).
To achieve a lightweight electrical FC system one approach is
to use a buck converter structure with additional bypass, based
on an optimal fuel cell output voltage. When the fuel cell volt-
age level is equal to the HVDC grid voltage, it is possible to
connect the FC with a bypass converter directly to the HVDC
grid [13],[14]. Due to the allowed voltage range of the HVDC
grid, the converter can be designed for approximately 30% of
the maximum installed fuel cell power. An overall FC power
between 200 kW and 300 kW is expected, which leads to a
possible weight saving of 35 kg to 52.5 kg, with an assumed
power density of 4 kW/kg based on the characteristic out of
Figure 4. Figure 5 shows a possible electrical architecture
for connecting the MFFCS to the Primary Electrical Power
Distribution Center (PEPDC) of the aircraft. The electrical
aircraft grid could be divided into two sides to isolate the
opposite grid if a failure occurs.
DC
DC
DC
DC
FC FC
HVDC Bus 1
+270V -270V
540V
DC
DC
DC
DC
FC FC
HVDC Bus 2
+270V -270V
540V
PEPDC
Fig. 5: Possible electrical integration of two independent HVDCbuses, both with two FC multistacks.
544
Within this paper the electrical grid sides are named as
HVDC bus 1 and HVDC bus 2. The single fuel cells (FC)
are connected in series. The tap of each sides between the
single FC systems could be based on ground potential to
separate the positive and negative voltage level. The main
advantages of the presented integration can be summarized to
the following:
• connection of different loads (540 VDC, ±270VDC)
• higher efficiency due to the reduce current flow
• two independent single grids increase the availability
• modular construction of the single components
The DC/DC converter could be subdivided into several smaller
DC/DC converter to reduce weight and increase efficiency.
Moreover, the subdivided DC/DC convertes could be designed
as an interleaved converter. Figure 6 presents a 4 level in-
terleaved converter with integrated bypass. Within this paper
the semiconductor switches S1 to S6 are designed as a Metal
Oxide Semiconductor Field Effect Transistor (MOSFET). The
angle delay α has to be addapted for each switch. Therefore,
a period offset of T/4 must be considered [15]. For a buck
converter the single α can be described as follows:
α1 =T4
; α2 =T2
; α3 =3 ·T
4; α4 = T (2)
A detailed describtion of the buck converter design can be
taken from [13],[14].
Vin VoutI1
I2
I3
I4
Iin Iout
Ibypass
D
D2
D3
D1 L1
L2
L3
L4
S1
S2
S3
S
4S
S6
C
4
5
Fig. 6: 4 level interleaved buck converter with integrated bypass path.
A. Advanced bypass mode
Depending on the electrical power demand the switches S5 and
S6 are closed (bypass mode) or open (converter mode). When
the bypass mode is active, all switches S1 to S6 are closed to
decrease the power dissipation Ploss according to Equation 3,
with the number n of parallel switches and the resistance R.
Ploss =∞
∑n=1
(In
)2
·R (3)
For converter mode the output current Iout can be described as
follows:
Iout1 = I1 + I2 + I3 + I4 (4)
respectively for bypass mode
Iout2 = I1 + I2 + I3 + I4 + Ibypass (5)
The efficiency advantage Δη of the additional closed switches
S1 to S4 during the bypass mode can be calculated with
Equation 6. Ploss(1) describes the power dissipation, if only
the bypass carries the output current Iout and Ploss(2) describes
the power dissipation of the divided current flow:
Δη = 1− ΔPloss(2)
ΔPloss(1)(6)
With the help of the drain source resistance RDS(on) and
the inductance resistance Rind, the power dissipation Ploss(2),
respectively Ploss(1) can be calculated as follows:
ΔPloss(1) = 2 · ( Iout2
)2 ·RDS(on) (7)
respectively
ΔPloss(2) =
4 ·[(
Iout−Ibypass
4
)2 ·RDS(on) +(
Iout−Ibypass
4
)2 ·Rind
]
+2 ·(
Ibypass
2
)2 ·RDS(on)
(8)
According to Equation 6, an increase of the efficiency up
to 35% could be achieved based on the divided current
flow. When the bypass is active, an operation efficiency of
approximately 100% could be assumed, due to the minimal
power dissipation.
B. Current commutation
The operating mode changes from the bypass mode into the
converter mode has to be considered more specifically. The
current commutates from the lower inductance path into the
higher inductance path. Depending on the current rise time
on the inductance L an overvoltage at the output could occur.
To prevent such an overvoltage a soft switching strategy was
created for opening the bypass switches S5 and S6 [16].
Therefore, the maximum power dissipation of the single switch
has to be calculated and must be compared to the term
comprising the junction Tj and ambient temperature Ta, the
heat sink Rth3, the resistance of the thermal pad Rth2 and the
transient thermal resistance ZthJC.
∫Ids ·Vds ≤
Tj −Ta
ZthJC +Rth2 +Rth3(9)
545
C. Fuel cell multistack
As well as the DC/DC converters also each of the FC systems
could be divided into several single stacks. Normally, the
number of single cells n for a stack is limited to approximately
n = 200 due to the mechanical stability and optimize gas
distribution. To create the required fuel cell output voltage
of approximately 600 VDC (3 ·n) a multistack approach could
be integrated. An antiparallel diode for each stack prevents the
total loss of a FC-System, if a single stack is out of operation.
Figure 7 shows the multistack architecture with the integrated
antiparallel diodes.
Stack 1 Stack 2 Stack 3
Fig. 7: Fuel cell multistack with antiparallel diodes.
D. Simulation results
Figure 8 shows the simulation results, which confirm the
theoretical concept. At time t = 40 ms the operating mode
change from the converter into the bypass mode. The bypass
current does not increase immediately to the nominal value
beacause the inductances L1 to L4 have to be discharged first.
0.02 0.04 0.06 0.08 0.10
50100
Output current
0.02 0.04 0.06 0.08 0.10
50
100
Cur
rent
(A)
0.02 0.04 0.06 0.08 0.10
50
Time (s)
Bypass current
One of the parallel currents
Fig. 8: Simulation results of the operating mode change from theconverter mode into the bypass mode.
If the bypass mode is active, it is illustrated that the current
Iout is divided to 2/3 on the bypass (S5,S6) and to 1/3 on the
closed DC/DC path (S1,S2,S3,S4).
III. FUEL CELL INTEGRATION TEST BENCH
To verify the theoretical concepts, a test bench with up to
10 kW was created. Therefore, the essential components can
be described as follows:
• programmable voltage source
• converter with integrated bypass
• programmable electrical load
• hardware in the loop system
• measuring equipment
Figure 9 shows the test bench. Due to the integration of
a programmable voltage source, controlled by the hardware
in the loop system, it is possible to create each type of
polarization curves, see Figure 4. Moreover, also the different
transient impacts like the double layer effect or the diffusion
effect can be simulated.
Controlsystem
MATLAB/Simulink
- Rated Values- Request of Actual Values- Visualization of Measurements
Current
Vol
tage
DC - Source
- Fuel Cell Model- Current and Voltage Characteristics
RS-
232
Current
Vol
tage
Electronic Load
DC/DC - Converter
Am
plitu
de
Period
RS-232
Control
- Simulation of Loadsteps- Request of Actual Values- Constant Output Voltage
Fig. 9: Schematic illustration of the test bench.
For implementation of the hardware in the loop system a
control system from the Bachmann company was selected.
The communication is done by Matlab/Simulink. Moreover, all
the measurement values can be processed by Matlab/Simulink
models. The application of the test bench is not restricted
only for the considered approaches. New concepts to fulfill the
required EMC standards are also investigated on the presented
test bench [17].
A. Measurement results
Figure 10 show the measurement results of the 4 level inter-
leaved converter.
0 1 2 3 4 5 6 7 8 9 1094
100
1 parallel 2 parallel4 parallel
Effiz
ienc
y (%
)
Power (kW)
Fig. 10: Efficiency measurements of 1, 2 and 4 level interleavedconverter.
The highest system efficiency can be reached at part load
operation, when all 4 level are active. However, it must
be considered that the efficiency of the 4 level interleaved
converter in the lower part load operation is below the 2 or
546
1 level interleaved converter. Therefore, a converter control
strategy could be implemented which reduce the number of
parallel DC/DC converter to achieve a high efficiency over
the entire operating mode. Moreover, it is possible to activate
the bypass mode already at lower requested power. That
leads to efficiency improvements up to 3% based on the
bypass mode. According to the simulation results of Figure 8
the measurement results, presented in Figure 11 confirm the
theoretical concept of the current distribution.
0 5 10 15 20 25 30 35 402
4
6
0 5 10 15 20 25 30 35 40-100
1020
Time (ms)
Vol
tage
(V)
Cur
rent
(A)
Fig. 11: Gate source voltage for activating the bypass mode (uppercurve). Current flow of one of the parallel interleaved converters(bottom curve).
At time t = 20 ms the operating mode changes from the
converter mode into the bypass mode. The required gate source
voltage rise immediately while the converter current (1 parallel
path) need some time to reach the new operating value of about
2.5 A due to the discharge effect of the inductance.
IV. CONCLUSION
The aim of the investigation was to present a weight optimized
electrical integration concept of a MFFCS-APU for modern
aircraft. Due to the high efficiency and the multifunctional
application regarding the use of the inert gas, water production
as well as the possibility to substitute the ram air turbine,
a MFFCS could achieve a lot of advantages. The fuel cell
stack as well as the required DC/DC converter are the heaviest
single components from the electrical part of the MFFCS.
Therefore, a weight optimized electrical integration of the
MFFCS is one of the main challanges. When the fuel cell
output voltage is equal to the HVDC grid, it is possible to
connect the FC directly (without DC/DC converter) to the
HVDC grid. However, the fuel cell output voltage is load
dependent, therefore, especially for the part load operation a
DC/DC converter is nessecary. To increase the efficiency a 4
level interleaved buck converter with additional bypass was
presented. Based on the investigated method, it is possible
to reduce the converter weight and increase the efficiency.
Therefore, a fuel cell output voltage above the HVDC voltage
is required to use the buck converter structure. A multistack
approach with a series connection of single stacks is presented.
The overall electrical MFFCS integration to the PEPDC could
be divided into two equal sides to isolate each other if a failure
occurs. For the bypass operation, the advantage bypass mode
to increase the efficiency, as well as the current commutation
from the low inductance path to the high inductance path
is presented. To verify the theoretical concepts a test bench
was built for a prototyp application up to 10 kW. The mea-
surement results confirm the theoretical results. In summary,
the presented method could be a good alternative and is not
restricted only for aircraft application. However, the amount of
the benefits depends on the allowed HVDC range and on the
internal fuel cell resistance (slope of the polarization curve).
ACKNOWLEDGMENT
This work as part of the project cabin technology and mul-
tifunctional fuel cell systems has been supported by Airbus
Operations GmbH and the German Federal Ministry of Edu-
cation and Research. (support code: 03CL03A)
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