Study and Analysis of Unmanned Solar Powered Vehicles Thite
Exploring the Potential of Unmanned Solar Powered Vehicles in Earth Observation and Telecommunication Systems
by Anil Bhausaheb*,
- Published in Journal of Advances and Scholarly Researches in Allied Education, E-ISSN: 2230-7540
Volume 2, Issue No. 1, Jul 2011, Pages 0 - 0 (0)
Published by: Ignited Minds Journals
ABSTRACT
Stratosphericplatforms, geostationary located at altitudes of 17 – 25 km, offer the possibility of becoming a new generation of infrastructural elements for future Earth observation and telecommunication systems. They can act as pseudo- satellites, but with the advantage of being much cheaper and closer to the ground and they can per- form missions that offer greater flexibility. They could be self-launched, easily recovered for maintenance, whenevernecessary, and moved to cover different regions, if desired. They allow a more detailed land vision, due totheir relative closeness to the Earth, at a much lower cost than conventional satellites; furthermore they are geostationary locatedand do not suffer from typical satellite revisiting time limits from 12 h up to 20 days. These platforms could cover a wide range of applications: real-time monitoring of seismic-risks or volcanicareas, early forest fire detection, border securitysurveillance, pipeline, and power-linesurveys; telecommunication servicessuch as cellular-telephone networks,photogram- metry, hydrographicmonitoring system, agriculture monitoring, etc.
KEYWORD
unmanned solar powered vehicles, stratospheric platforms, geostationary, Earth observation, telecommunication systems, pseudo-satellites, flexibility, land vision, conventional satellites, real-time monitoring
INTRODUCTION
Unmanned an vehicle (UAVs) have been used for over 40 years by the military services for dangerous missions and surveillance. The technology has been relatively expensive and unreliable, as cost and safety issues were considered of secondary importance to performance. However, technology has advanced sufficiently for this highly technical area of the aeronautical industry to be developed into a new growing UAV civilian industry. The United States has already begun investing in this field and has initiated a massive drive to develop this new industry. Europe also has the necessary technologies and should now also support and encourage industry to take advantage of new technological approaches in order to successfully become a leading participant in this field. In a recent business market study carried out by Frost and Sullivan [1], the global market for UAVs in civil and commercial applications will be close to US$ 2 billion by 2014. The largest market shares are expected to pertain to Coastguard and Maritime Surveillance operations, Border Security, and Forest Fire Management. From a flying altitude of 18 km, an area of about 300 – 400 km in diameter would be covered for communication transmission if the onboard antenna irradiation diagram is properly chosen. This would mean that about seven to eight platforms could cover the entire south Mediterranean Sea, from Spain to Turkey (Fig. 1), creating an electronic illegal immigration barrier as well as a secure border control system.
ISSN-2230-7540
3 www.ignited.in
Compared to the present cost of airborne systems (5000 – 7000 E/flight hour), high altitutde long endurance/unmanned air vehicles (HALE/UAVs) offer clear advantages in monitoring missions, as continuous observations will be performed through- out the year over the area of interest and all the required data will usually be available immediately. The main advantage of the very-long endurance solar-powered autonomous aircraft (VESPAA) is that this system has less climbing and descending events, which is important when considering inter- ference with aviation traffic. Other HALE-UAV configurations have a very limited endurance (24 – 36 h), which would drastically increase any potential collision risk with civil aviation traffic.
Double the number of UAVs would be necessary to continuously guarantee the surveillance service, thus the system total life cycle cost would be increased to a great extent. Other medium altitude long endurance (MALE)-UAVs have, as a further
ISSN-2230-7540
4 www.ignited.in
disadvantage, the fact that a much higher number of UAVs are necessary to continuously cover the entire Mediterranean Sea, since the covered area decreases with the square value of the flying altitude (Fig. 2); the total life cycle cost system would increase remark- ably with a MALE configuration. Very high endurance, in fact, calls for high mission reliability requirements of the air vehicle, its systems and payload. An endurance of several months would only be possible using a solar- and hydrogen-powered platform. The vehicle would climb to 17 – 20 km mainly taking advantage of direct sun radiation. Any electric energy not required for the propulsion and payload operations would be pumped back into the electrolyzer system that would convert the water into hydrogen and oxygen fuel; during the night, the platform would maintain altitude, thanks to the fuel cell system, which would produce electri- city and water as a by-product of the reaction; the geostationary position would be maintained by a level turning flight. Several types of high altitude stratospheric plat- forms have already been
ISSN-2230-7540
5 www.ignited.in
designed [2 – 5]. At the end of 1994, NASA started the Environmental Research Aircraft and Sensor Technology (ERAST) program; one of the four drones is the Pathfinder solar plat- form, which exceeded 24 km of altitude during a 15 h flight. In the summer of 2001, the Helios solar- powered platform set a new world record of 29.3 km. Although a flight of several days was planned for summer 2003, the program suffered a devastating setback when the Helios prototype was lost in June 2003 in a flight mishap during a shake- down mission. The Helios wing bent dramatically and oscillated, and then the wing spar broke. It seems very likely that Helios crashed because of undamped pitch oscillations that led to a partial structural failure of the very flexible Kevlar/carbon spar. In the interim status report, the investigation board stated that the ‘undamped pitch oscillations may be related to the complex interactions between the aerodynamic, structural, stability and control, and propulsion systems on a flexible aircraft.’ The main innovative aspects of the VESPAA are the following. 1. The design of the first European aerodynamic solar-powered platform that would be able to remain continuous in flight for very long periods of time (4 months). 2. Low noise and zero emission aircraft. The advan- tage of zero emissions is particularly important for environmental monitoring. 3. The first European solar-powered platform to vali- date the feasibility and reliability of solar cells, fuel cells and brushless electric motors. All these features lead to: (a) Reduced cost per flight hour (thanks to a large increase in the endurance flight hours);
ISSN-2230-7540
6 www.ignited.in
(b) Potentially increased acquisition cost, while reducing the cost of maintenance and spare parts; (c) reduced cost – larger area coverage per platform, thus, fewer platforms per area are required; (d) improved operational safety – due to the fact that the flight would occur above aviation traffic, resulting in limited interference with it, and above adverse weather; (e) Lower propagation delay compared to satellites. The Department of Aerospace Engineering at the Politecnico di Torino (POLITO/DIASP, Scientific Responsible Prof. Romeo) has acquired a great deal of experience, starting from 1994, in the design of solar-powered UAV as high altitude very long endur- ance platform positioned in the stratosphere at an altitude of 17 – 20 km and with an endurance of about four months [6 – 14]. Started under a grant from the Italian Space Agency (ASI), a great amount of work was carried out within two European funded projects (HeliPlatw and Capecon) whose final task was to fill the European gap in knowledge and feasibility of such kinds of innovative systems. The ESA-STRATOS definition study was also performed for stratospheric platforms, driven by the possibility of replacing or complementing space systems with stratospheric platforms, particularly in the area of telecommunication applications. The main objective of this study was to explore the possi- bility of the development and operation of a Euro- pean stratospheric platform based on a sound analysis of possible service areas, assessment of available and future technologies, and to perform a conceptual design for the
ISSN-2230-7540
7 www.ignited.in
most suitable platform concept that would answer the requirements of future telecommunication markets (Fig. 3). Two reference configurations for stratospheric platforms were selected from a number of studies on stratospheric platforms and some existing designs of stratospheric aircraft: an aerodynamic one and an aerostatic one. Both are electrically driven solar- powered designs. Detailed investigations into the aerodynamic and aerostatic reference design led to the identification of the critical platform technol- ogies. Most of these technologies are common to both platform categories. On the basis of the necess- ary technology development, a stepwise approach was sustained using both types of platforms in the prototype and test phase. This approach indicates that an operable stratospheric platform could be developed within 10 years. There is no clear rule on whether aerostatic or aerodynamic systems are in general the preferable solution for stratospheric platforms. Because of their different characteristics and behaviour, the platform selection very much depends on the applications and the corresponding flight envelope. A comparison of the technical reference designs with the payload requirements from the system architecture showed that the smaller aerodynamic configuration (payload of 150 kg nd available power for payload of 1.5 kW) would be suitable as a preliminary demonstrator of all the key technologies and could also demonstrate some of the service capabilities, mainly for Earth observation, while the larger aerostatic design (payload greater than 1000 kg and power of 20 kW) would be required for an operational telecom service scenario).
ISSN-2230-7540
8 www.ignited.in
Fig. 3 Aerostatic HAVE-UAV for telecom applications On the other hand, for a rigorous station-keeping position throughout the year, a jet stream of up to 40 m/s in the wintertime could be difficult to be con- trasted because of the wind sensitivity of aerostatic platforms. However, because the aerostatic law imposes UAV dimensions, a higher power energy would be possible as the efficiency of the fuel cells and solar cells would increase. The high cost of each airship, in comparison to the aerodynamic platform, is another critical point. Solar-powered stratospheric platforms are also preferable to other HALE/MALE platforms because of: (a) environment-friendly operations (no emission in the lower stratosphere where the highly sensitive ozone layer is located); (b) Similarity of the technologies to space-based systems (power systems, autonomous operations, and payloads); (c) Similarity in operations to space based systems (launching, very-long operations, etc.).
ISSN-2230-7540
9 www.ignited.in
Regenerative power technologies, such as thin film photovoltaic (PV) arrays, fuel cells, electrolyzers, power, and management systems, are the keys to achieve long-endurance regenerative UAV. Since the basic power source, the sun, is not available throughout the whole day, effective designs for managing, collecting, storing, and consuming energy are needed to make the platform a real alternative to satellites for night and day missions. The design of a vehicle that is able to operate solely from the incoming energy of the sun is a fine balance between energy collection and energy consumption. This energy balance is influenced by a number of factors such as the operational environment and the capabilities and efficiencies of the power system components. Considering the solar radiation that is available at 17 km of altitude for a panel surface placed parallel to the Earth’s surface, a maximum specific solar power of 675 and 475 W/m2, respect- ively, at 368 and 458N would be detectible on the worst day (December 21). During the best optimal day, the maximum specific solar power is about 1240 and 1190 W/m2, respectively, at 368 and
458 N.
The energy balance for a HeliPlat configuration flying in June at 17 km of altitude is reported in Fig. 4. A very large amount of electric power would be available from sun radiation, with a peak at 180 kW. However, because of the low solar cell efficiency taken into consideration (21 per cent), just a small amount of power would be available for the platform. With an optimised design of the platform, just a small amount of power would be required by the motors to fly (about 6.5 kW); the extra energy available from the solar cells would be supplied to the electrolyser for the production of hydrogen and oxygen for the night flight.
ISSN-2230-7540
10 www.ignited.in
To accurately determine the feasibility of the high altitude aircraft concept, a detailed model of the wind environment is also necessary. This wind model would provide mean and 99th percentile winds along the area of interest for the analysis. Although the wind does not affect the aircraft’s power generation, it has a significant effect on its drag and power consumption. A wind study was therefore performed at several locations. The upper air data climatic tables recorded by the Italian Air Force from 1963 to 1997 were analysed to obtain the wind profiles as a function of the altitude (from 1000 hPa (111 m) to 10 hPa (31 055 m)) for several latitudes. Analysing the data (Fig. 5(a)), it was clear that the jet-streams are at a minimum between the altitudes of 18 and 22 km, depending on the time of year. An average wind speed of 17.1 m/s was recorded in January at 18 km in altitude. The record- ing frequency of such high jet streams, from 1963 to 1997, was also investigated (Fig. 5(b)). In January, 60 per cent of the events recorded were in a lower speed range than 15 m/s; a higher speed than 35 m/s was recorded just 56 times, in more than 2000 events, over 34 years, although in only a few cases (twice in 34 years), high wind speeds of up to 60 m/s were recorded.
ISSN-2230-7540
11 www.ignited.in
From the educational point of view, design of a solar-powered airplane presents an interesting case to introduce students to the procedures and prac- tices of aircraft design as a means of illustrating the often conflicting requirements of the many involved disciplines. In such kind of advanced aircrafts the dif- ficulties with sun-powered flight make an accurate integration of the structural weight optimisation, aerodynamics, propulsion efficiency, and electronic devices much more critical. In addition students approach the work with present time problems such as non-linear aeroelasticity or design of advanced composite structures.
2 CAPECON PROJECT
Seven potential configurations have been evaluated as part of the EC funded Project ‘CAPECON: Civil UAV Applications and Economic Effectivity of Poten- tial Configuration Solutions’: three HALE (with the Politecnico di Torino – Department of Aerospace Engineering Scientific Responsible: Prof. ROMEO – as work package leader of solar, modular and blended configuration design, and Task leader for solar configuration design), two MALE and two Rotary UAV concepts. In addition, a comprehensive cost model has been developed for the first time to assess the economic advantages and disadvantages of the various configurations. On the basis of these evaluations, some recommendations were made for further critical technology (CT) and technology program (TP) activities within the sixth framework.
ISSN-2230-7540
12 www.ignited.in
The basic requirements for the CAPECON Solar HALE UAV configuration have been first established. The initial starting point requirements for the Solar HALE UAV configuration have been obtained from previous HeliPlat experience know-how. In particu- lar, the platform would accommodate a maximum user payload mass of 130 – 150 kg and consume a maximum electrical power of 1.3 – 1.5 KW. A maximum total mass of 850 – 900 kg is expected for 6-month flight at an altitude of 17 km. The choice of 17 km is a compromise between less wind and low air density – that means very low Reynolds numbers and solar radiation. The following tasks have been carried out by POLITO/DIASP during the HALE UAV solar configur- ation design. 1. Ground rules and assumptions: the solar-powered HALE UAV has been designed, considering the Mediterranean Sea border patrol and forest fire monitoring during summer time as possible applications. The platform would fly for 6 months, starting on the first of April, at an altitude of 17 km for a latitude below 44 8N. 2. Preliminary design: including sizing, geometrical definition (three views and three- dimensional), external layout, aerodynamic definition, structure concept, system
ISSN-2230-7540
13 www.ignited.in
definition, payload integration, internal layout and weight, and balance computation. 3. Aerodynamic analysis (computational fluid dynamics (CFD)). 4. Flight performance analysis: including database establishment (aerodynamic, weight, and propulsion databases) and performance computations (integral performance, point performance-flight envelopes, and ground performance). 5. Structural analyses finite-element method (FEM) of the chosen configuration and aeroelastic con- siderations of the high aspect ratio/low mass wing. 6. Reliability, maintainability, and safety analysis.
3 DESIGN PROCESS
As most applications for stratospheric platforms require continuous operation, solar power seems to be the only adequate option to provide the necessary power for propulsion and for the payload. A power system consisting of solar cells and an energy storage system to bridge the night phases would therefore be required. Solar power electric energy would be used in the project to drive the propellers for the required flight. It would use electric-motor-driven propellers to convert electrical power into thrust. Any electric energy not required for the propulsion and payload operations would be pumped back into the fuel cell energy storage system and, during the night, the plat- form would maintain altitude, thanks to the stored (solar) energy [6 – 8]. The power collected by the PV panels during the day would be absorbed not only by the electric motors in order to drive the platform but also by the control system and by
ISSN-2230-7540
14 www.ignited.in
the payload. The power that remains would feed the electrolyser, which would produce high-pressure hydrogen and oxygen from the stored water. The gases would be stored in separate cylinders and supply the fuel cells during the night, so that the electric power needed by the platform would always be assured. The system would be completed by a pump to feed the electroly- ser with water, the gas tanks, the water tank, and some auxiliaries. The regenerative fuel cell energy storage system would be used to balance the power. Although the power required to fly the aircraft is roughly constant over time, the power available from sunlight changes during the day – from zero at sunrise, to peak power at noon, and back to zero at sunset. The amount of energy that would need to be stored overnight (energy storage system capacity) depends on the location (Earth latitude) and the time of year. In general, winter conditions and higher lati- tudes require more capacity because the nights are longer and there is less sunlight. The key figures of merit are the storage system’s energy density (watt-hours of energy stored per kilo- gram of storage system mass) and its efficiency. The high energy density that would be required to keep a solar airplane flying over most locations and during most times of the year has forced designers to con- sider more complicated forms of energy storage. Chief among these is the hydrogen/oxygen regenera- tive fuel cell (RFC); an energy storage system, based on dedicated proton exchange membrane fuel cells, gives an energy density of 450 – 600 Wh/kg, with respect to 200 – 220 Wh/kg of the best lithium bat- teries, and efficiency of about 60 per cent. No other energy storage method (outside nuclear power) has a higher energy density.
ISSN-2230-7540
15 www.ignited.in
Beginning in the early 1990s, significant invest- ments from the automotive industry resulted in a seven-fold increase over a span of 5 years. Rapidly emerging hydrogen-based technologies, primarily derived from the automotive industry, could be used to start a new era of propulsion systems for light aircraft and small commuters and electrical system replacement for larger transport aircraft. The feasibility of this project depends on several key-enabling technologies such as fuel cell stack, fuel cell system, hydrogen fuel storage, and a safe airport hydrogen-fuelling infrastructure. It is estimated that an almost ten-fold increase in energy density (5 kWh/kg) can be expected within ten years to enable the all-electric flight of small commercial aircraft. Since today’s solar cells only convert a small percentage of the sun’s energy into useful work, any stratospheric platform needs a large surface area for power generation. The solar cell area does not impose a problem on aerostatic platforms due to their large surface provided by the lift gas hull. For aerodynamic configurations, the sun-powered level flight can only be obtained through a suitable design and accurate integration of the highest stan- dards that can be achieved for each involved techno- logical item: structure, aerodynamics, solar cells, energy storage, propulsion efficiency, and avionics The theoretical efficiency limit of solar energy conversion under idealized conditions is 86 per cent. Present technology, however, limits this percentage to about 50 per cent. One of the most fundamental limitations on solar cell efficiency is the band gap of the semiconductor from which the cell is made. In order to obtain improvements, researchers and manufacturers stack different band gap materials in multi-junction cells. The maximum efficiency that can be achieved with a solar cell, made from a single material, when converting light to electrical power is about 30 per cent; the best efficiency that has actually been achieved is
ISSN-2230-7540
16 www.ignited.in
about 25 per cent. Many different layers could be stacked to catch photons at all energies, reaching a better efficiency than 70 per cent (the best efficiency actually achieved with multi-junction solar in only a few research projects is about 35 per cent). The two most common types of semiconductor materials used in PV cell manufacturing are silicon (Si) and gallium arsenide (GaAs). Most commercial solar cells used in terrestrial applications are made from wafers of silicon. About 85 per cent of the PV market consists of Si solar cells. When used in commercial production, they allow power conversion efficiency close to 17 per cent. These thick (200 – 300 mm) single-crystal silicon cells are today available at low prices (about 700 – 1000 E/m2). Higher efficiency (up to 25 per cent) very thin (50 – 70 mm) gallium arsenide cells are also available, although at a higher price (about 25.000 E/m2). Since the solar cell efficiency closely depends on the surface temperature of the PV array, a low oper- ational temperature of the solar cell is beneficial. For this application, the ambient temperature is an important parameter, because the estimated temp- erature at the flying level (17 km) is about 558C, but the solar cells specification are given for the cell temperature of þ288C (standard test conditions). Good efficiency could be obtained through the proper design of the electric brushless motor (95 per cent) and of the propellers (85 per cent), which have a high diameter and a speed of about a 1000 min; these elements should be designed to fulfil the requirements of low mass and high reliability [15]. Particular attention should be paid to the automation of the full propulsive system; fur- thermore, the power that is available from the sun should be properly split between the motors and energy storage system.
ISSN-2230-7540
17 www.ignited.in
A multi-disciplinary optimisation computer pro- gram has been developed to design the platform, taking into account wind speed up to an altitude of 27 km, the solar radiation changes over a period of1 year, altitude, latitude, solar cell efficiency and weight, fuel cell efficiency and energy density, aero- dynamic profile drag, etc. The preliminary design of a Solar HALE Aircraft Multi Payload and Operation (SHAMPO) (Fig. 6) flying at high altitude and low Reynolds numbers, has led to the main features reported in Table 1.
4 INTERNAL AND EXTERNAL LAYOUT
The power system of a stratospheric platform consists of the three main subsystems: (a) power source; (b) energy storage; (c) electrical propulsion system. which should be managed by an electronic control system to make optimum use of the available energy. The architectural analysis and design of the power conditioning (DC/DC converter) system for the fuel cells, the solar power supply and the propul- sion system (motor and inverter) interface of the platform has been performed with the assistance of numerical simulation [16]. The PV energy source module converts the solar energy into electrical energy and provides it to the DC link in a suitable way. The module consists of the solar cells, the DC/DC converter, and the maxi- mum power point tracker (MPPT) controller. The MPPT controller and the DC/DC are used to obtain the maximum power from the solar cells. The FC energy storage module acts as an energy storage system. It consists of the fuel cell array, the hydrolyser and the hydrogen, oxygen, and water tanks. The gases are stored
ISSN-2230-7540
18 www.ignited.in
at high pressure (120 – 250 bar) and used during the night to feed the fuel cells that supply the motors; the water feeds the electrolyser to close the cycle. The electric motor module, consisting of the electric motor and the inverter, converts electrical energy into mechanical energy. A blended wing body (BWB) configuration with eight brushless electric motors has been chosen as Maximum power available for payload PPL 1300 W a result of the preliminary study. The weight of Avionic mass WAV 32 kg Maximum payload mass WPL 130 kg Structural mass WSTR 430 kg Solar cell mass WSC 127 kg Take-off weight WTO 924 kg Power available for the avionic PAV 325 W each motor is about 6.5 Kg, including the carbon-fibre propeller blade. The BWB solution, compared to the conventional design [6 – 12], seems to be the best compromise between performance, available surface for solar-cells Cruise flight Power supplied to the electric motors PFLY 6700 W and volume for multi-payload purposes; the fuselage blended zone in fact presents a volume of about 38 m3. Sun power (38 8N April) PSUN 11 560 W Efficiency energy storage system (Fuel cell þ A1) Density energy storage system (Fuel cell þ A1) hFC 0.6 WFC 550 Wh/kg The Heliplat propeller blade (blade radius ¼ 1.15 m), [6 – 8], has been used for the preliminary design of SHAMPO. Propeller characteristics are obtained Efficiency solar cells hSC 0.21Density solar cells WSC 0.6 kg/m2 Efficiency electric motor hM 0.95 Efficiency propeller hPROP 0.85 Number of motors N 8 Cruise airspeed TAS 25 m/s The mixed supply System, with solar cells and fuel cells, requires a common DC link in order to adjust the voltage level between the different sources. Solar cells have the additional requirement
ISSN-2230-7540
19 www.ignited.in
of load impedance adjustment to allow the maximum power point to vary according to the ambient con- ditions, like temperature or solar irradiance. The core of the full scale HeliPlat Power Supply Drive (PoSuDri) should be based on a DC link of 360 V. This voltage has been chosen as a balanced value in order to limit the size and weight of the elec- tric cables, which in the present design of the solar aircraft must supply power over a 70 m length of wingspan. Therefore, all electrically powered subsys- tems become part of the electric power distribution system, which unites all the electrical sources and loads of the aircraft by means of the high voltage power distribution bus. A three-dimensional CAD model of the preliminary internal layout has been set up using CATIA V5 (Fig. 6a). using two in-house FORTRAN developed tools. The first tool is able to compute the maximum efficiency propeller geometrical characteristics giving as input the design condition, blade number, and airfoils databases. The output of the first tool are the chord and pitch distributions. The second tool gives per- formances in terms of efficiency, thrust coefficient, and torque coefficient and are used to evaluate the characteristic far from the design point. The thrust supplied by this propeller in cruise con- ditions is sufficient for the SHAMPO design point (Fig. 7), and it is possible to increase the airspeed by using the 5000 W of surplus power available for 2 h. A flight power of about 6700 W supplied to the electric motors have been computed in cruise con- ditions (Z ¼ 17000 m, 1st April 38 8N) flying at 25 m/s; supplying a maximum available power of about 9800 W, to the motors the airplane could reach 31 m/s and in the case of emergency or to con- trast wind jet-streams, it would be able to reach 36 m/s, using 5000 W reserve power.
ISSN-2230-7540
20 www.ignited.in
Rolling control on SHAMPO is accomplished by using ailerons located on the outboard section of the wing. The restrictions imposed by roll control for general aviation aircraft are not severe [17 – 19]. The ailerons are positioned along the wing span at a distance of 18.8 to 30.8 m, and the total surface is sub- divided into three parts (Fig. 6b), each one controlled by an electric motor in order to have a triple redun- dancy system. The control surfaces have been intro- duced in the Vsaero CFD aerodynamic model. The input file has therefore been modified to take into account several rotations of the control surfaces. Preq /Sw ¼ (2/r)0:5 (Wtot /Sw )3=2 (CD /C 3=2 )
ISSN-2230-7540
21 www.ignited.in
The CATIA V5 external layout (Fig. 8) has also been developed and used for aerodynamic and structural analysis models and to estimate the aerodynamic derivatives. The main geometrical characteristics of the final configuration are:
5 AERODYNAMIC ANALYSIS (CFD)
The design procedure that has been followed in the preliminary analysis is based on the energy balance equilibrium between the available solar power and the required power, the former being dependent on the solar cell area installed on the wing and stabil- izer, the latter depending on the velocity and total drag of the platform.
ISSN-2230-7540
22 www.ignited.in
3/2
The power required, per unit wing area, (Preq/Sw) to maintain horizontal flight is given by where the propulsion efficiency hprop includes pro- peller, motor, and inverter efficiency. The endurance parameter has in particular to be satisfied to minimize the power required for a horizontal flight. When minimizing the parameter CD/CL , it has also been preferred to reduce the drag coefficient CD instead of only increasing the lift coefficient CL, because of the lower structural load. The total drag coefficient is obtained from the sum of the wing and tail profile drag, the wing and tail induced drag and the parasite drag (fuselage, booms, hard interaction with wing and tails). Rey- nolds numbers of less than 700 000 should be considered in most cases. The aerodynamic calculations were made using the VSAERO code [20], a computer program used to calculate the non-linear aerodynamic characteristics of arbitrary configurations in a subsonic flow. Non-linear effects of wake shape are treated in an iterative wake relaxation procedure, and the effects of viscosity are treated in an iterative loop, while coupling the potential flow and integral boundary layer calculations.
ISSN-2230-7540
23 www.ignited.in
The aircraft configuration has been changed during the design process. The first unswept blended configuration, which was worked out during the first iteration, presented some problems from the longitudinal stability point of view. In order to move the center of gravity forward, with the constrains of installation volumes, a classical solution with a fuse- lage has been tested. This solution was later dis- carded because it was too penalizing in terms of aerodynamic efficiency. To increase the stability margin without any sig- nificant aerodynamic efficiency reduction, a wing without fuselage and with a small angle of sweep (about 58) has been chosen in order to have a static margin of about 9 – 10 per cent. A second investigation has been then performed, with a wing sweep angle of 58, to optimize the wing airfoils and the shape of the tip, with the aim of redu- cing the contribution of the induced drag. The main factor responsible for total platform coefficient drag (0.0266 at a 68 angle of attack) is the wing and in particular the outer part. Induced drag corresponds to about 63 per cent of the total drag, whereas viscous drag accounts for 24 per cent and pressure drag for 13 per cent.
ISSN-2230-7540
24 www.ignited.in
The use of a round wing tip appears to have a positive role in minimizing tip vortex formation and thus minimizing induced drag. When using the same airfoil DAE21 for the wing and blended fuselage part, a large zone of depression, which was responsible for performances losses, is formed behind the wing. For this reason, new SH118 profiles, which are capable of improving the pressure recovery in the fuselage zone, have been developed; with this airfoil, the wake leaves the body in a more uniform way (Fig. 9), reducing downwash in the blended zone. This configuration presents a maximum efficiency of about 41.6 at CL ¼ 0.85 (Fig. 10) and a maximum endurance parameter of about 43 at CL ¼ 1.2. The lift and pressure distribution along the wing span has also been computed (Fig. 11).
ISSN-2230-7540
25 www.ignited.in
The configuration also presents a good stability margin of about 10 per cent of the mean aerody- namic chord. This configuration has been chosen as a starting point for the structural design.
6 FLIGHT PERFORMANCE
A multidisciplinary design to determine the static and dynamic behaviour of an aircraft in the early stage can lead to significant weight and cost saving and improvement in configuration and performance [6 – 8, 12]. The computational fluid dynamics solver (VSAERO CFD) has been used to directly calculate the stability and control derivatives of the new SHAMPO configuration. The CFD forces and moments have been differentiated with respect to the angle of attack, angle of sideslip, and aircraft shape parameters in order to determine these derivatives. A complete database of the main static and dynamic derivatives were worked out using this method.
ISSN-2230-7540
26 www.ignited.in
The developed VSAERO model has a wing and horizontal tail, but lacks a vertical tail, therefore clas- sical formulas have been used [17 – 19]. The effect of a roll angular velocity on the pressure distribution and wake shape is shown in Fig. 12. Aircraft flying qualities and stability requirements are defined from many sources. The requirements for longitudinal static stability simply require that the pitching moment at zero-lift angle of attack, Cm0, should be positive and that the derivative of the pitching moment with respect to the angle of attack, Cma, must be negative. These two require- ments are mainly determined by the wing configur- ation. The new SHAMPO configuration satisfied both conditions. Similar to the longitudinal stability requirements, lateral-directional stability is based on both static and dynamic requirements. For static stability, the aircraft’s yaw stiffness, Cnb, should be positive and its roll stiffness, Clb, should be negative. These requirements ensure that the aircraft generates a positive yawing moment and a negative rolling moment for a positive sideslip, and it can thus stay in controllable flight conditions. From
ISSN-2230-7540
27 www.ignited.in
a first esti- mation of the SHAMPO derivatives, considering a value of natural dihedral of 2.78, the static condition has been verified with the calculated values Cnb ¼ 0.012 Clb ¼ 20.083. A flight dynamic analysis has been performed, in the preliminary design phase, considering that rigid-body degrees of freedom and elastic degrees of freedom are decoupled; however, this is not always possible. The frequency separation between the rigid-body motions and elastic degrees of free- dom for advanced aircraft (such as solar UAV, very light weight UAV or advanced aircraft with active control systems) may not be sufficient to permit the typical treatment of the vehicle dynamics. In particular for flexible HALE-UAV, it is not always safe to treat rigid body effects and flexibility effects separately as demonstrated by the Helios prototype mishap. The intention of this preliminary stage has been to have a first estimation of the airplane handling qualities and a rigid mathematical model has been therefore used to describe the flight dynamics of the aircraft. MIL-F-8785C contains a number of criteria with which the modes of a piloted aircraft can be com- pared to predict the expected flying quality levels. The closest comparison category, for the SHAMPO- UAV, could be that of a small light aircraft, which is a Class I category aircraft. The approach used to ana- lyse the dynamic behaviour of the airplane has been of using the uncoupled, linearized equations of motion solutions. A Matlab – Simulink [21] flight dynamic software has been used to obtain the equations. All the longitudinal modes are stable for the SHAMPO-UAV cruise condition. With reference to the short period criteria within MIL-F-8785C, for the Category B Flight
ISSN-2230-7540
28 www.ignited.in
phase, a minimum damping ratio of 0.2 is obtained for Level 2 and a limit of 0.15 for Level 3. The SHAMPO UAV longitudinal damping is 0.203. There are two aperiodic modes (one stable and one unstable) and one stable periodic mode for the SHAMPO-UAV cruise condition in the lateral motion. The Dutch roll is a coupled oscillation between yaw/sideslip and roll, a complex mode usually deter- mined by the characteristics of the rolling and yawing moments with sideslip. The Dutch roll mode is stable, in SHAMPO-UAV, with reference to MIL-F- 8785C. The roll-mode flying quality criteria are also well within the specified requirements given in MIL-F-8785C. The remaining mode, the spiral mode, has already been established as being unstable. A certain degree of spiral instability can be accepted for different flying quality levels. For Level 1 Cat B, a time-to- double amplitude greater than 20 s is acceptable according to MIL-F-8785C. SHAMPO-UAV has a value of time-to-double amplitude of about 45 s. It can be concluded that the aircraft is statically stable and that it is able to stabilize longitudinal oscillations on its own; it has a spiral instability with a time-to-double amplitude that is however acceptable.
7 STRUCTURAL CONCEPTS AND ANALYSES
A preliminary structural concept was defined accord- ing to the estimated inertial and aerodynamic loads. High structural efficiency is required to minimize the airframe weight and increase the payload mass. This is obtained through: (a) Extensive use of high modulus graphite/epoxy material to obtain a very light-high stiffened structure with good aeroelasticity behaviour;
ISSN-2230-7540
29 www.ignited.in
(b) Numerical structural analysis using the FEM. In spite of the weight reduction, in high aspect ratio wings like VESPAA, aeroelastic phenomena play an important role that has to be satisfied and verified. The total platform weight, per wing area, is deter- mined by adding the weight of the propulsion, the solar cells, avionics and payload to the airframe; the weight of the propulsion system includes brushless motors, inverter, conditioning system, and propellers. For the adopted configuration, a good structural wing solution to enhance the bending stiffness could be represented by an opportunely reinforced high modulus carbon fibre leading edge wing-box (Fig. 13). The main spar could be subdivided into five parts, which could be connected to each other by metal fittings. The aero-structural loads, including both manoeuvre and gust, have been defined according to the JAR-VLA 333 airworthiness regulations, with a maximum limit load n ¼ 3 for the diving speed. A computer program has been developed to evaluate and define the structural characteristics of the main wing/tail spars of the platform considering strains under the value of 1000 m1 for all flight limit design structure program. The load distribution has loads. Different materials and layouts have been been determined from an estimated lift and mass distribution according to the preliminary data and considered in order to introduce a level of optimization to the iterative calculations. CFRP data have been introduced referring to a Young’s modulus in the fibre direction of about 275 GPa, ultimate compressive strain limit of about 1500 m1, a lamina thickness of 0.135 mm and a density of 1580 kg/m3. The inertial loads (structural and nonstructural) have been estimated and taken into account accord- ing to the preliminary
ISSN-2230-7540
30 www.ignited.in
configuration design. The ultimate strain behaviour along the wing span is reported in Fig. 14. An FE model of the SHAMPO main spar configuration has been developed at the preliminary stage using the Patran/Nastran code, based on preliminary design structural concept. The model consists of one half-wing, which is considered clamped in the symmetry plane. The leading-edge wing-box was simulated using shell elements (Quad4). The mesh on these surfaces has been made respecting the exact radial and longitudinal position of the ply lay-up, which has been determined with the preliminary aerodynamic calculations in order to obtain an equivalent load condition. The load condition reported in this work only concerns the D point of the flight envelope (n ¼ 3, VEAS ¼ 47 km/h, accord- ing to airworthiness regulation). A comparison between the theoretical and Nastran results is reported in terms of ultimate strains (Fig. 14).
ISSN-2230-7540
31 www.ignited.in
A new and improved FE model of the entire SHAMPO airframe has been developed, in order to evaluate the structural behaviour of the whole optimized SHAMPO configuration (Fig. 15). The structure has been designed to have a very stiff low weight air- frame. Wing and horizontal tail spars have different layup (+208/0n8/+458/core)s along the span in order to minimize the weight of the structure while ribs, for modelling simplicity, are considered all made by the same material with the same lay-up. The conformal fuselage also had a variable lay-up. The results of the FE model showed a wing weight (wing-box and ribs) of about 314 kg; the fuselage weight of about 58 kg, and there was a total airframe weight without skin of 412 kg. These results are in a good agreement with weight estimation formulas for man-powered airplanes, high-altitude airplanes, or ultra-light cantilever twin-boom tails. Some FE results are displayed in Fig. 15; a maximum deflection of about 6 m at the tip of the wing has been determined at point D in the n – V diagram, considering a safety factor of 1.5 (N ¼ 4.5). No particular stress concentration has been revealed.
ISSN-2230-7540
32 www.ignited.in
8 AEROELASTIC CONSIDERATIONS
A preliminary aeroelastic analysis has been carried out on SHAMPO UAV. The first preliminary model consisted of a beam-wise structure of one half-wing considered clamped in the symmetry plane, positioned along wing-box elastic axis as determined in section 8. The stiffness and inertia properties have been introduced, according to the preliminary structural design concepts. The motors, fuel cell system, payload, and vessels have been considered as concentrated masses with estimated properties, according to the preliminary layout. The other non- structural masses have been distributed along a beam wise rear spar with only an inertial effect. No specific structural details have been introduced into the model, such as junctions or rotating propellers. The aerodynamic wing loads have been defined according to the strip theory and the Theodorsen function [22].
ISSN-2230-7540
33 www.ignited.in
In this preliminary analysis, the flutter calculation has been performed considering an undeformed equilibrium condition; typical V-g plots have been obtained and critical velocities have been deter- mined as the damping parameters tend to be posi- tive (Fig. 16(d)). No structural damping or other external damping has been introduced. Some of the linear wing modes considered in its un-deformed equilibrium state are also plotted (Figs 16(a) to (c)). No critical speeds have been detected up to 100 m/s using the linear calculation. Compared to the design diving speed, reported in previous sections, it is possible to conclude that the airworthiness target is satisfied by the proposed configuration. Moreover, when the airplane shows a highly flexible wing, an advanced aeroelastic behaviour should be con- sidered as stated in references [13], [23], and [24]. Moderate-to-large bending deflections, due to aerody- namic loads, cause non-linear coupling between edge-wise bending and torsion. Therefore, the trim condition and the natural frequencies of flight dynamics could be significantly affected by the inherent flexibility and non-linear deformations of the wing structure, leading to an overall change in the wing’s aeroelastic characteristics [23, 25].
ISSN-2230-7540
34 www.ignited.in
A non-linear aeroelastic model has been developed and proposed as a design/diagnostic analysis tool [24, 25]. A geometrically consistent non-linear structural model for large deformations, developed by Hodges and Dowell [26] and modified according to Da Silva’s second-order geometrical non-linear terms [27], has been implemented. The structural model has been coupled to an unsteady aerodynamic model for an incompressible flow field, based on the Wagner aerodynamic indicial function, in order to obtain a non-linear aero- elastic model [28]. Linear and non-linear static and dynamic aeroelastic responses have been considered. The introduction of a small dynamic perturbation about a non-linear static equilibrium has been applied in order to solve the system of governing equations and to study the sub- critical and super- critical aero elastic response and the flutter boundaries. The inplane, out- of-plane, and torsional displacements have been considered to be a summation of the static and dynamic components in the un-deformed reference system. The partial differential equations governing the dynamics of the flexible beam, were reduced to a system of ordinary differential equations [24, 25, 29] using a series discretization technique [30], along with Galerkin’s method, to obtain the aeroelastic governing equations. Galerkin’s shape functions have been chosen from a set of linearly independent and complete functions derived from a clamped-free beam case. The deflected equilibrium condition has also been affected by a change in the overall flight dynamic characteristics of the aircraft due to wing flexibility. It has been possible to implement the procedure in a preliminary aeroelastic evaluation as the nonlinear equilibrium system has been included in the analy- sis: the actual static deflection has to be connected to a specific flight condition. If, for example, we con- sider that at each speed a level flight condition has to be satisfied, the flutter speed and frequency are obtained with the
ISSN-2230-7540
35 www.ignited.in
subsequent main steps: (a) choos- ing a flight speed and the correct angle of attack to satisfy the vertical equilibrium condition, (b) calcu- lating the static equilibrium deformed shape at the flight speed, (c) linearizing around the deformed shape, (d) calculating the eigenvalues of the linear- ized system, and (e) checking for stability. If the flut- ter speed and frequency are stable, increase the flight speed and repeat all the preceding steps until instability speed is reached. The flutter speed and frequency are defined as the lowest airspeed and corresponding frequency at which a given structure flying in a specific atmos- phere will exhibit sustained simple harmonic oscil- lations [22]. The flutter condition is a borderline situation, or neutral stability, due to the fact that small motions must be stable at a speed below flutter speed, whereas divergent oscillations occur in a range of speed above flutter speed. Using the in-house developed tool linear flutter speed can be computed assuming the equilibrium static configuration as zero with no coupling effect. Including equilibrium terms, non-linear flutter speed calculations can be performed. Results on a typical HALE configuration are reported in refer- ences [24], [25], and [29] showing the flutter speed behaviour closely depends on tip deflection. With a static tip displacement of 1 m, the nonlinear flutter speed reduces to 70 per cent of that obtained in the un-deformed equilibrium condition, while for a wtip of 2.5 m a flutter speed reduction of about 42 per cent respect to linear flutter has been obtained. Another design indication that should be taken into account [13, 23, 25] is that the stiffness ratio between in-plane stiffness and out-of-plane stiffness could play an important role in increasing the flutter boundaries; the positive effect of increased flutter speed when a higher value of the stiffness ratio is introduced into the airplane structure design has been pointed out [23, 25].
ISSN-2230-7540
36 www.ignited.in
Stiffness characteristics are determined according to an equivalent Euler-Bernoulli beam. Other extended models [31] are under development in order to have a better structural approximation. The linear flutter results imply that small disturbances will grow exponentially for velocities higher than the flutter speed. However, as the ampli- tude of oscillations grows and additional non-linear stiffness is introduced, the vibrations do not grow to infinity but instead converge to a limit cycle oscil- lation (LCO). The amplitude of the LCO gives an idea of the amount of stress/strain on the structure and its study could be useful for analysis and design. Whether such non-linear effects are favourable or not will greatly depend on the particular circum- stances and physical parameters that are involved. Nevertheless, it is clear that non-linear effects often lead to LCOs. In their absence, the alternative would be a catastrophic flutter and consequently structural failure. The amplitude of the LCO can only be determined by time-marching the non-linear governing equations of the aeroelastic system, while the LCO stability can be done via a Lyapunov- based approach [28]. An example of supercritical aeroelastic behaviour (out-of plane tip-deflection wtip), detected above the non-linear flutter speed has been obtained con- sidering a small initial disturbance and by analysing the response via a time marching integration scheme, as reported in Fig. 17; the non-linear Mathematicaw solver has been used. Traditionally, flying aircraft have been treated within the confines of flight dynamics which, in most cases, deals with rigid aircraft. On the other hand, flexible aircraft fall into the domain of aero- elasticity. Although some attempts have been made to include aircraft rigid body degrees of freedom, aeroelasticity is concerned mostly with the vibration
ISSN-2230-7540
37 www.ignited.in
and flutter instability of wings fixed at the root. In reality, all aircraft possess some measure of flexibility and carry out rigid body manoeuvres, so that the question arises as to whether flexibility can be con- sidered in the real aircraft flight dynamics behaviour and whether it should already be considered in the preliminary design phase [25]. The flight dynamics of a flexible-model similar to SHAMPO has been considered, including the geome- try of the aircraft, aerodynamic data and mass, flex- ural rigidity, and torsional rigidity distributions [31]. The wing of the aircraft consists of a right-half wing and left-half wing modelled as beams under- going bending and torsion. The remaining members are assumed to be rigid. The equations of motion are obtained by means of the Lagrangian equations in quasi-coordinates. The resulting equations are non- linear ordinary differential equations for the rigid body translations and rotations, and the boundary- value problems for the elastic deformations. The dis- tributed variables are discretized in space using the Galerkin’s method. Using a perturbation approach, the resulting set of non-linear
ISSN-2230-7540
38 www.ignited.in
ordinary differential equations are separated into a set of zero-order equations for the rigid body variables and a set of first-order equations for the perturbations in the rigid body variables and elastic deformations. The zero-order equations are used to design the desired manoeuvres. The first-order equations are used to assess the stability of the aircraft on the chosen flight paths and to design feedback controls to main- tain stable flights. In the numerical example, steady level flights at three different forward velocities have been con- sidered [31]. The required control inputs that permit the flight and the resulting static deflections have been computed. The stability of the aircraft about these trims has been dealt with by inspecting the eigenvalues of the first-order (perturbation) equations. The aircraft has been found to be unstable in one of the trims and marginally stable in the other two. These results have been compared with the results of the quasi-rigid aircraft and the restrained aircraft models. Moreover, it has been shown that a control design based on the quasi-rigid aircraft model can destabilize the aircraft and that the full model must be used for a successful feedback control.
9 CONCLUSION
The results of this preliminary study show that it could be possible to obtain a very long endurance high altitude platform for Earth observation and tele- communication applications, at least for low latitude sites in Europe and for several months of continuous operation. A BWB configuration of Solar HALE Aircraft has been obtained as a result of the preliminary design. The BWB solution seems to be the best compromise between performance available surface for solar cells and volume for multi-payload purposes. The numerical aerodynamic results obtained show the availability of suitable airfoils for operation at low Reynolds numbers.
ISSN-2230-7540
39 www.ignited.in
The structural concept layout has been defined and designed according to regulation requirements. The preliminary analytical and FE results showed a good correlation. The assumed structural concept, sandwich wing-box spar, demonstrates low struc- tural mass and satisfactory classical flutter beha- viour. According to airworthiness regulations a preliminary flight dynamic and flutter analysis has been carried out. Moreover, when the airplane shows highly flexible wings an advanced aeroelastic behaviour should be considered. Considering the case of a typical HALE UAV, a flutter speed reduction of up to 42 per cent with respect to classical analysis has been obtained considering a 2.5 m wing tip deflection.
ACKNOWLEDGEMENTS
The authors acknowledge the important contri- bution made by the following funding programmes. 1. HELIPLAT w. ‘Design of High Altitude Solar-pow- ered Platform for Telecommunication and Earth Observation Applications’. ASI (Italian Space Agency). Contracts 1995-99. Coordinator: Prof. G. Romeo 2. HELINET: (Heliplat Network). ‘Network of the Stratospheric Platforms for Traffic Monitoring, Environmental Surveillance and Broadband Ser- vices’. EC 58 FP – Contract IST-1999-11214, 2000-03; Coordinator: Polito. WP Leader of Heli- platw Design and Manufacturing: Prof. G. Romeo 3. CAPECON. ‘Civil UAV Applications and Economic Effectivity of Potential Configuration Solutions’. EC 58 FP – Contract GRD1-2001-40162, 2002-05. Coordinator: IAI. - WP Leader of 3 HALEs Design: Prof. G. Romeo.
ISSN-2230-7540
40 www.ignited.in
4. STRATOS. ‘Stratospheric platform – a definition study for an ESA system’. ESA Contract, 2002 – 2004. Coordinator: Airobotics -WP Leader Aerody- namic Platform Study: Prof. G. Romeo. 5. UAVNET. ‘Civilian UAV Thematic Network: Tech- nologies, Applications, Certification’. EC 58FP, G4RM-CT-2001-05. Coordinator: IAI
REFERENCES
1. Cohen, D. 2005 Global markets for civil and commer- cial UAVs. Frost & Sullivan Interactive Briefing, UAVNET, available from http://www.uavnet.com. 2. Anon. Eternal airplane. The lift-off of unmanned solar- electric wings. Pop. Sci., 1994,
100, 70 – 75.
3. Hall, D. W., Watson, D. A., Tuttle, R. P., and Hall, S. A. Mission analysis of solar powered aircraft. NASA CR-172583, 1985. 4. Hall, D. W. and Hall, S. A. Structural sizing of a solar powered aircraft. NASA CR-
172313, 1984.
5. Youngblood, J. W., Talay, T. A., and Pegg, R. J. Design of long endurance- endurance unmanned airplanes incorporating solar and fuel cell propulsion. AIAA paper 84-1430, 1984. 6. Romeo, G. Design proposal of high altitude very-long endurance solar powered platform for earth obser- vation and telecommunication applications. 48th Inter- national Astronautical Congress, Turin, October 1997, paper no. IAF-97-M.2.05.
ISSN-2230-7540
41 www.ignited.in
7. Romeo, G., Frulla, G., Cestino, E., and Corsino, G. HELIPLAT: design, aerodynamic, structural analysis of long-endurance solar-powered stratospheric platform. J. Aircr.,
2004, 41(6), 1505 – 1520.
8. Romeo, G. and Frulla, G. HELIPLAT: high altitude very- long endurance solar powered UAV for telecommuni- cation and earth observation applications. Aeronaut. J., 2004,
108(1084), 277 – 293.
9. Romeo, G. Manufacturing and testing of graphite- epoxy wing box and fuselage structures for a solar-pow- ered UAV-HAVE. 21st ICAS Congress, Melbourne, Sep- tember 1998, paper A98-31591. 10. Romeo, G. Design of high altitude very-long endurance solar powered platform for earth observation and tele- communication applications. Aerotecnica Missili E Spazio, 1998, 77(3 – 4), 88 – 99. 11. Romeo, G. and Frulla, G. HELIPLAT: aerodynamic and structural analysis of HAVE solar powered platform. 1st AIAA Technical Conference and Workshop on Unmanned aerospace vehicles, systems, technologies and operations, Portsmouth, USA, 20 – 23 May 2002. 12. Romeo, G., Frulla, G., and Fattore, L. HELIPLAT: high altitude very long endurance solar powered UAV for telecommunication application. FEM analysis, manufacturing and testing of 21 m long CFRP wing box. In Proceedings of the Applied Vehicle Technology Panel Symposium on Unmanned vehicle for aerial, ground and naval military operations, NATO, RTO, Ankara, Turkey, October 2000, paper no. 12.
ISSN-2230-7540
42 www.ignited.in
13. Frulla, G. Aeroelastic behaviour of a solar-powered high-altitude long endurance unmanned air vehicle (HALE-UAV) slender wing. Proc. Instn Mech. Engrs, Part G: J. Aerospace Engineering, 2004, 218(G3), 179 – 188. 14. Romeo, G., Frulla, G., Cestino, E., and Corsino, G. HALE-UAV solar configuration: aerodynamic and struc- ture analysis, 2nd Iteration. CAPECON consortium report ID4.2.2/2e, January 2004. 15. Frulla, G. Preliminary reliability design of a solar powered high altitude very long endurance unmanned air vehicle. Proc. Instn Mech. Engrs, Part G: j. Aerospace Engineering, 2002, 216, 189-196. 16. Bojoi, R. Lazzari, M., Profumo, F., and Tenconi, A. Digital Field-oriented control for dual three-phase induction motor driver. IEEE Trans. Ind. Appl., 2003, 39 (3), 752-760. 17. Etkin, B. and Reid, L. Dynamics of flight: stability and control, 1996 (J. Wiley & Sons, New York). 18. Perkins, C. and Hage, R. Airplane performance stability and control, 1949 (John Wiley & Sons, New York). 19. Raymer, D. P. Aircraft design: a conceptual approach, 1999 (AIAA Education Series, New York). 20. Natham, J. K. A code for calculating the nonlinear aero- dynamic characteristic of arbitrary configuration, VSAERO user’s manual version 6.2, 2001 (Analytical Methods, Inc., Washington, USA). 21. Matlab-Simulink User’s Manual, copyright 1984 – 1999 (The MathWorks, Inc., Natick, MA, USA).
ISSN-2230-7540
43 www.ignited.in
22. Bisplinghoff, R. L., Ashley, H., and Halfman, R. L. Aeroelasticity, 1996, p. 880 (Dover Science, New York). 23. Dowell, E., Edwards, J., and Strganac, T. Nonlinear aeroelasticity. J. Aircr., 2003,
40(5), 857 – 874.
24. Romeo, G., Frulla, G., Cestino, E., Marzocca P., and Tuzcu I. Nonlinear aeroelastic modelling and exper- iments of flexible wings. 47th AIAA/ASME/ASCE/ AHS/ASC SDM Conference, Newport, Rhode Island, USA, 2006, p. 15. 25. Cestino, E. Design of very long-endurance solar pow- ered UAV. PhD Thesis, Department of Aerospace Engineering, Politecnico di Torino, 2006. 26. Hodges, D. H. and Dowell, E. H. Non-linear equations of motion for the elastic bending and torsion of twisted non uniform rotor blades. NASA TN D-7818, 1974. 27. Crespo Da Silva, M. R. M. Non-linear flexural-flexural- torsional-extensional dynamics of beams – I. Formu- lation. Int. J. Solids Struct., 1988, 24(12), 1225 – 1234. 28. Sedaghat, A., Cooper, J. E., and Wright, J. R. Prediction of non linear aeroelastic instabilities. ICAS Congress, Harrogate, UK, 2000. 29. Romeo, G., Frulla, G., Cestino, E., and Marzocca, P. Non-linear aeroelastic behavior of highly flexible HALE wings. In Proceedings of 25th ICAS Congress, Hamburg, Germany, 3 – 8 September 2006, p. 11. 30. Meirovitch, L. Fundamentals of vibrations, 2001 (McGraw Hill, New York).
ISSN-2230-7540
44 www.ignited.in
31. Tuzcu, I., Marzocca, P., Cestino, E., Romeo, G., and Frulla, G. Stability, control, and simulation of high- altitude-long-endurance UAVs. 47th AIAA/ASME/ ASCE/AHS/ASC SDM Conference, Newport, Rhode Island, USA, 2006, p. 16.
